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Computational Fluid and Solid Mechanics Series Editor: Klaus-Jürgen Bathe Massachusetts Institute of Technology Cambridge, MA, USA Advisors: Franco Brezzi University of Pavia Pavia, Italy
Olivier Pironneau Université Pierre et Marie Curie Paris, France
Available Volumes
D. Chapelle, K.J. Bathe The Finite Element Analysis of Shells - Fundamentals, 2003 D. Drikakis, W. Rider High-Resolution Methods for Incompressible and Low-Speed Flows 2005 M. Kojic, K.J. Bathe Inelastic Analysis of Solids and Structures 2005 E.N. Dvorkin, M.B. Goldschmit Nonlinear Continua 2005
Eduardo N. Dvorkin · Marcela B. Goldschmit
Nonlinear Continua
With 30 Figures
Authors: Eduardo N. Dvorkin, Ph.D. Marcela B. Goldschmit, Dr. Eng. Engineering School University of Buenos Aires and Center for Industrial Research TENARIS Dr. Simini 250 B2804MHA Campana Argentina
Library of Congress Control Number: 2005929275
ISBN-10 3-540-24985-0 Springer Berlin Heidelberg New York ISBN-13 978-3-540-24985-6 Springer Berlin Heidelberg New York This work is subject to copyright. All rights are reserved, whether the whole or part of the material is concerned, specifically the rights of translation, reprinting, reuse of illustrations, recitation, broadcasting, reproduction on microfilm or in other ways, and storage in data banks. Duplication of this publication or parts thereof is permitted only under the provisions of the German Copyright Law of September 9, 1965, in its current version, and permission for use must always be obtained from Springer. Violations are liable to prosecution under German Copyright Law. Springer is a part of Springer Science+Business Media springeronline.com © Springer-Verlag Berlin Heidelberg 2006 Printed in Germany The use of general descriptive names, registered names, trademarks, etc. in this publication does not imply, even in the absence of a specific statement, that such names are exempt from the relevant protective laws and regulations and therefore free for general use. Typesetting: Dataconversion by authors Final processing by PTP-Berlin Protago-TEX-Production GmbH, Germany Cover-Design: deblik, Berlin Printed on acid-free paper 62/3141/Yu – 5 4 3 2 1 0
To the Argentine system of public education
Preface
This book develops a modern presentation of Continuum Mechanics, oriented towards numerical applications in the fields of nonlinear analysis of solids, structures and fluids. Kinematics of the continuum deformation, including pull-back/push-forward transformations between di erent configurations; stress and strain measures; objective stress rate and strain rate measures; balance principles; constitutive relations, with emphasis on elasto-plasticity of metals and variational principles are developed using general curvilinear coordinates. Being tensor analysis the indispensable tool for the development of the continuum theory in general coordinates, in the appendix an overview of tensor analysis is also presented. Embedded in the theoretical presentation, application examples are developed to deepen the understanding of the discussed concepts. Even though the mathematical presentation of the di erent topics is quite rigorous; an e ort is made to link formal developments with engineering physical intuition. This book is based on two graduate courses that the authors teach at the Engineering School of the University of Buenos Aires and it is intended for graduate engineering students majoring in mechanics and for researchers in the fields of applied mechanics and numerical methods.
VIII
Preface
I am grateful to Klaus-Jürgen Bathe for introducing me to Computational Mechanics, for his enthusiasm, for his encouragement to undertake challenges and for his friendship. I am also grateful to my colleagues, to my past and present students at the University of Buenos Aires and to my past and present research assistants at the Center for Industrial Research of FUDETEC because I have always learnt from them. I want to thank Dr. Manuel Sadosky for inspiring many generations of Argentine scientists. I am very grateful to my late father Israel and to my mother Raquel for their e orts and support. Last but not least I want to thank my dear daughters Cora and Julia, my wife Elena and my friends (the best) for their continuous support. Eduardo N. Dvorkin
I would like to thank Professors Eduardo Dvorkin and Sergio Idelsohn for introducing me to Computational Mechanics. I am also grateful to my students at the University of Buenos Aires and to my research assistants at the Center for Industrial Research of FUDETEC for their willingness and e ort. I want to recognize the permanent support of my mother Esther, of my sister Mónica and of my friends and colleagues. Marcela B. Goldschmit
Contents
1
Introduction = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 1.1 Quantification of physical phenomena . . . . . . . . . . . . . . . . . . . . . . 1.1.1 Observation of physical phenomena . . . . . . . . . . . . . . . . . . 1.1.2 Mathematical model . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 1.1.3 Numerical model . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 1.1.4 Assessment of the numerical results . . . . . . . . . . . . . . . . . . 1.2 Linear and nonlinear mathematical models . . . . . . . . . . . . . . . . . 1.3 The aims of this book . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 1.4 Notation . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .
1 1 1 2 2 2 2 4 5
2
Kinematics of the continuous media = = = = = = = = = = = = = = = = = = = = = = = 2.1 The continuous media and its configurations . . . . . . . . . . . . . . . 2.2 Mass of the continuous media . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.3 Motion of continuous bodies . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.3.1 Displacements . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.3.2 Velocities and accelerations . . . . . . . . . . . . . . . . . . . . . . . . . 2.4 Material and spatial derivatives of a tensor field . . . . . . . . . . . . . 2.5 Convected coordinates . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.6 The deformation gradient tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.7 The polar decomposition . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.7.1 The Green deformation tensor . . . . . . . . . . . . . . . . . . . . . . 2.7.2 The right polar decomposition . . . . . . . . . . . . . . . . . . . . . . 2.7.3 The Finger deformation tensor . . . . . . . . . . . . . . . . . . . . . 2.7.4 The left polar decomposition . . . . . . . . . . . . . . . . . . . . . . . . 2.7.5 Physical interpretation of the tensors w R > w U and w V 2.7.6 Numerical algorithm for the polar decomposition . . . . . . 2.8 Strain measures . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.8.1 The Green deformation tensor . . . . . . . . . . . . . . . . . . . . . . 2.8.2 The Finger deformation tensor . . . . . . . . . . . . . . . . . . . . . . 2.8.3 The Green-Lagrange deformation tensor . . . . . . . . . . . . . . 2.8.4 The Almansi deformation tensor . . . . . . . . . . . . . . . . . . . .
7 7 9 9 9 10 12 13 13 21 21 22 25 25 26 28 33 33 33 34 35
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2.8.5 The Hencky deformation tensor . . . . . . . . . . . . . . . . . . . . . 2.9 Representation of spatial tensors in the reference configuration (“pull-back”) . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.9.1 Pull-back of vector components . . . . . . . . . . . . . . . . . . . . . 2.9.2 Pull-back of tensor components . . . . . . . . . . . . . . . . . . . . . 2.10 Tensors in the spatial configuration from representations in the reference configuration (“push-forward”) . . . . . . . . . . . . . . . . 2.11 Pull-back/push-forward relations between strain measures . . . . 2.12 Objectivity . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.12.1 Reference frame and isometric transformations . . . . . . . 2.12.2 Objectivity or material-frame indi erence . . . . . . . . . . . . 2.12.3 Covariance . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.13 Strain rates . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.13.1 The velocity gradient tensor . . . . . . . . . . . . . . . . . . . . . . . . 2.13.2 The Eulerian strain rate tensor and the spin (vorticity) tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.13.3 Relations between di erent rate tensors . . . . . . . . . . . . . . 2.14 The Lie derivative . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 2.14.1 Objective rates and Lie derivatives . . . . . . . . . . . . . . . . . . 2.15 Compatibility . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 3
4
35 36 36 40 42 43 44 45 47 49 50 50 51 53 56 58 61
Stress Tensor = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 3.1 External forces . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 3.2 The Cauchy stress tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 3.2.1 Symmetry of the Cauchy stress tensor (Cauchy Theorem) . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 3.3 Conjugate stress/strain rate measures . . . . . . . . . . . . . . . . . . . . . . 3.3.1 The Kirchho stress tensor . . . . . . . . . . . . . . . . . . . . . . . . . 3.3.2 The first Piola-Kirchho stress tensor . . . . . . . . . . . . . . . 3.3.3 The second Piola-Kirchho stress tensor . . . . . . . . . . . . . 3.3.4 A stress tensor energy conjugate to the time derivative of the Hencky strain tensor . . . . . . . . . . . . . . . . . . . . . . . . 3.4 Objective stress rates . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .
67 67 69
Balance principles = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 4.1 Reynolds’ transport theorem . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 4.1.1 Generalized Reynolds’ transport theorem . . . . . . . . . . . . . 4.1.2 The transport theorem and discontinuity surfaces . . . . . 4.2 Mass-conservation principle . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 4.2.1 Eulerian (spatial) formulation of the mass-conservation principle . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 4.2.2 Lagrangian (material) formulation of the mass conservation principle . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 4.3 Balance of momentum principle (Equilibrium) . . . . . . . . . . . . . .
85 85 88 90 93
71 72 74 74 76 79 81
93 95 95
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XI
4.3.1 Eulerian (spatial) formulation of the balance of momentum principle . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 96 4.3.2 Lagrangian (material) formulation of the balance of momentum principle . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 103 4.4 Balance of moment of momentum principle (Equilibrium) . . . . 105 4.4.1 Eulerian (spatial) formulation of the balance of moment of momentum principle . . . . . . . . . . . . . . . . . . . . 105 4.4.2 Symmetry of Eulerian and Lagrangian stress measures 107 4.5 Energy balance (First Law of Thermodynamics) . . . . . . . . . . . . 109 4.5.1 Eulerian (spatial) formulation of the energy balance . . . 109 4.5.2 Lagrangian (material) formulation of the energy balance 112 5
Constitutive relations = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 115 5.1 Fundamentals for formulating constitutive relations . . . . . . . . . . 116 5.1.1 Principle of equipresence . . . . . . . . . . . . . . . . . . . . . . . . . . . 116 5.1.2 Principle of material-frame indi erence . . . . . . . . . . . . . . 116 5.1.3 Application to the case of a continuum theory restricted to mechanical variables . . . . . . . . . . . . . . . . . . . . 116 5.2 Constitutive relations in solid mechanics: purely mechanical formulations . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 120 5.2.1 Hyperelastic material models . . . . . . . . . . . . . . . . . . . . . . . 121 5.2.2 A simple hyperelastic material model . . . . . . . . . . . . . . . . 122 5.2.3 Other simple hyperelastic material models . . . . . . . . . . . . 128 5.2.4 Ogden hyperelastic material models . . . . . . . . . . . . . . . . . . 129 5.2.5 Elastoplastic material model under infinitesimal strains 135 5.2.6 Elastoplastic material model under finite strains . . . . . . 155 5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 167 5.3.1 The isotropic thermoelastic constitutive model . . . . . . . 167 5.3.2 A thermoelastoplastic constitutive model . . . . . . . . . . . . 170 5.4 Viscoplasticity . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 176 5.5 Newtonian fluids . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 180 5.5.1 The no-slip condition . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 181
6
Variational methods = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 183 6.1 The Principle of Virtual Work . . . . . . . . . . . . . . . . . . . . . . . . . . . . 183 6.2 The Principle of Virtual Work in geometrically nonlinear problems . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 186 6.2.1 Incremental Formulations . . . . . . . . . . . . . . . . . . . . . . . . . . 189 6.3 The Principle of Virtual Power . . . . . . . . . . . . . . . . . . . . . . . . . . . . 194 6.4 The Principle of Stationary Potential Energy . . . . . . . . . . . . . . . 195 6.5 Kinematic constraints . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 207 6.6 Veubeke-Hu-Washizu variational principles . . . . . . . . . . . . . . . . . 209 6.6.1 Kinematic constraints via the V-H-W principles . . . . . . 209 6.6.2 Constitutive constraints via the V-H-W principles . . . . 211
XII
A
Contents
Introduction to tensor analysis = = = = = = = = = = = = = = = = = = = = = = = = = = = = 213 A.1 Coordinates transformation . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 213 A.1.1 Contravariant transformation rule . . . . . . . . . . . . . . . . . . . 214 A.1.2 Covariant transformation rule . . . . . . . . . . . . . . . . . . . . . . . 215 A.2 Vectors . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 215 A.2.1 Base vectors . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 216 A.2.2 Covariant base vectors . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 216 A.2.3 Contravariant base vectors . . . . . . . . . . . . . . . . . . . . . . . . . . 218 A.3 Metric of a coordinates system . . . . . . . . . . . . . . . . . . . . . . . . . . . . 219 A.3.1 Cartesian coordinates . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 219 A.3.2 Curvilinear coordinates. Covariant metric components . 220 A.3.3 Curvilinear coordinates. Contravariant metric components . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 220 A.3.4 Curvilinear coordinates. Mixed metric components . . . . . 221 A.4 Tensors . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 222 A.4.1 Second-order tensors . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 223 A.4.2 n-order tensors . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 227 A.4.3 The metric tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 228 A.4.4 The Levi-Civita tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . 229 A.5 The quotient rule . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 232 A.6 Covariant derivatives . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 233 A.6.1 Covariant derivatives of a vector . . . . . . . . . . . . . . . . . . . . 233 A.6.2 Covariant derivatives of a general tensor . . . . . . . . . . . . . 236 A.7 Gradient of a tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 237 A.8 Divergence of a tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 238 A.9 Laplacian of a tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 239 A.10 Rotor of a tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 240 A.11 The Riemann-Christo el tensor . . . . . . . . . . . . . . . . . . . . . . . . . . . 240 A.12 The Bianchi identity . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 243 A.13 Physical components . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 244
References = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 247 Index = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = = 255
1 Introduction
The quantitative description of the deformation of continuum bodies, either solids or fluids subjected to mechanical and thermal loadings, is a challenging scientific field with very relevant technological applications.
1.1 Quantification of physical phenomena The quantification of a physical phenomenon is performed through four different consecutive steps: 1. Observation of the physical phenomenon under study. Identification of its most relevant variables. 2. Formulation of a mathematical model that describes, in the framework of the assumptions derived from the previous step, the physical phenomenon. 3. Formulation of the numerical model that solves, within the required accuracy, the above-formulated mathematical model. 4. Assessment of the adequacy of the numerical results to describe the phenomenon under study.
1.1.1 Observation of physical phenomena This is a crucial step that conditions the next three. Making an educated observation of a physical phenomenon means establishing a set of concepts and relations that will govern the further development of the mathematical model. At this stage we also need to decide on the quantitative output that we shall require from the model.
2
Nonlinear continua
1.1.2 Mathematical model Considering the assumptions derived from the previous step and our knowledge on the physics of the phenomenon under study, we can establish the mathematical model that simulates it. This mathematical model, at least for the cases that fall within the field that this book intends to cover, is normally a system of partial di erential equations (PDE) with established boundary and initial conditions.
1.1.3 Numerical model Usually the PDE system that constitutes the mathematical model cannot be solved in closed form and the analyst needs to resort to a numerical model in order to arrive at the actual quantification of the phenomenon under study.
1.1.4 Assessment of the numerical results The analyst has to judge if the numerical results are acceptable. This is a very important step and it involves: • Verification of the mathematical model, that is to say, checking that the numerical results do not contradict any of the assumptions introduced for the formulation of the mathematical model and verification that the numerical results “make sense” by comparing them with the results of a “back-of-an-envelope” calculation (here, of course, we only compare orders of magnitude). • Verification of the numerical model, the analyst has to assess if the numerical model can assure convergence to the unknown exact solution of the mathematical model when the numerical degrees of freedom are increased. The analyst must also check the stability of the numerical results when small perturbations are introduced in the data. If the results are not stable the analyst has to assess if the unstable numerical results represent an unstable physical phenomenon or if they are the result of an unacceptable numerical deficiency. • Validation of the mathematical/numerical model comparing its predictions with experimental observations.
1.2 Linear and nonlinear mathematical models When deriving the PDE system that constitutes the mathematical model of a physical phenomenon there are normally a number of nonlinear terms that appear in those equations. Considering always all the nonlinear terms, even if
1.2 Linear and nonlinear mathematical models
3
their influence is negligible on the final numerical results, is mathematically correct; however, it may not be always practical. The scientist or engineer facing the development of the mathematical model of a physical phenomenon has to decide which nonlinearities have to be kept in the model and which ones can be neglected. This is the main contribution of an analyst: formulating a model that is as simple as possible while keeping all the relevant aspects of the problem under analysis (Bathe 1996). In many problems it is not possible to neglect all nonlinearities because the main features of the phenomenon under study lie in their consideration (Hodge, Bathe & Dvorkin 1986); in these cases the analyst must have enough physical insight into the problem so as to incorporate all the fundamental nonlinear aspects but only the fundamental ones. The more nonlinearities are introduced in the mathematical model, the more computational resources will be necessary to solve the numerical model and in many cases it may happen that the necessary computational resources are much larger than the available ones, making the analysis impossible. Example 1.1. JJJJJ In the analysis of a solid under mechanical and thermal loads some of the nonlinearities that we may encounter when formulating the mathematical model are: • Geometrical nonlinearities: they are introduced by the fact that the equilibrium equations have to be satisfied in the unknown deformed configuration of the solid rather than in the known unloaded configuration. When the analyst expects that for her/his practical purposes the di erence between the deformed and unloaded configurations is negligible she/he may neglect this source of nonlinearity obtaining an important simplification in the mathematical model. An intermediate step would be to consider the equilibrium in the deformed configuration but to assume that the strains are very small (infinitesimal strains assumption). This also produces an important simplification in the mathematical model. Of course, all the simplifications introduced in the mathematical model have to be checked for their properness when examining the obtained numerical results. • Contact-type boundary conditions: these are unilateral constraints in which the contact loads are distributed over an area that is a priori unknown to the analyst. • Material nonlinearities: elastoplastic materials (e.g. metals); creep behavior of metals in high-temperature environments; nonlinear elastic materials (e.g. polymers); fracturing materials (e.g. concrete); etc. JJJJJ
4
Nonlinear continua
Example 1.2. JJJJJ In the analysis of a fluid flow under mechanical and thermal loads some of the nonlinearities that we may encounter when formulating the mathematical model are: • Non-constant viscosity/compressibility (e.g. rheological materials and turbulent flows modeled using turbulence models). • Convective acceleration terms for flows with ReA0 when the mathematical model is developed using an Eulerian formulation, which is the standard case. JJJJJ
JJJJJ Example 1.3. In the analysis of a heat transfer problem some of the nonlinearities that we may encounter when formulating the mathematical model are: • Temperature dependent thermal properties (e.g. phase changes). • Radiation boundary conditions
JJJJJ
There are mathematical models in which the e ects (outputs) are proportional to the causes (inputs); these are linear models. Examples of linear models are: • linear elasticity problems, • constant viscosity creeping flows, • heat transfer problems in materials in which constant thermal properties are assumed and radiative boundary conditions are not considered, • etc. Deciding that the model that simulates a physical phenomenon is going to be linear is an analyst decision, after first considering and afterwards carefully neglecting, in the formulation of the mathematical model, all the sources of nonlinearity.
1.3 The aims of this book This book intends to provide a modern and rigorous exposition of nonlinear continuum mechanics and even though it does not deal with computational implementations it is intended to provide the basis for them. In the second chapter of the book we present a consistent description of the kinematics of the continuous media. In that chapter we introduce the concepts of pull-back, push-forward and Lie derivative requiring only from the reader
1.4 Notation
5
a previous knowledge of tensor analysis. Objective and covariant strain and strain rate measures are derived. In the third chapter we discuss di erent stress measures that are energy conjugate to the strain rate measures presented in the previous chapter. Objective stress rate measures are derived. In the fourth chapter we present the Reynolds transport theorem and then we use it to develop Eulerian and Lagrangian formulations for expressing the balance (conservation) of mass, momentum, moment of momentum and energy. In the fifth chapter we develop an extensive presentation of constitutive relations for solids and fluids, with special focus on the elastoplasticity of metals. Finally, in the sixth chapter we develop the variational approach to continuum mechanics, centering our presentation on the principle of virtual work and discussing also the principle of stationary potential energy and the VeubekeHu-Washizu variational principles. The basic mathematical tool in the book is tensor calculus; in order to assure a common basis for all the readers, in the Appendix we present a review of this topic.
1.4 Notation Throughout the book we shall use the summation convention; that is to say, in a Cartesian coordinate system d e = d e =
3 X
=1 3 X
d e d e
i ru
= 1> 2> 3 >
=1
and in a general curvilinear system dl el =
3 X
dl el
l=1
dlm em =
3 X
dlm em
i ru
l = 1> 2> 3 =
m=1
Also, our notation is compatible with the notation introduced in continuum mechanics by Bathe (Bathe 1996). We shall define all notation at the point where we incorporate it.
2 Kinematics of the continuous media
In this chapter we are going to present a kinematic description of the deformation of continuous media. That is to say, we are going to describe the deformation without considering the loads that cause it and without introducing into the analysis the behavior of the material. Some reference books for this chapter are: (Truesdell & Noll 1965, Truesdell 1966, Malvern 1969, Marsden & Hughes 1983).
2.1 The continuous media and its configurations Continuum mechanics is the branch of mechanics that studies the motion of solids, liquids and gases under the hypothesis of continuous media. This hypothesis is an idealization of matter that disregards its atomic or molecular structure. A ¡continuous body is an open subset of the three-dimensional Euclidean ¢ space D = 1> 2> 3}: the material coordinates. For the reference configuration Eqs.(2.1) are D { = {D (") ; " = "( {D ) = (2.3) From Eqs.(2.1) and (2.3) we obtain the bijective mapping w ! between the configuration at time w and the reference configuration, w d
{
= w !d ( {D > w)
;
D
{
=
£w
w 1
!1
¤D
(w {d ) = w
(2.4) u
In a regular motion the inverse mapping ! exists and if ! 5 F also ! 5 F u (Marsden & Hughes 1983), where F u is the set of all functions with continuous derivatives up to the order “u”. The formal concept of regular motion agrees with the intuitive concept of a motion without material interpenetration. From Eqs. (2.2) and (2.4) we get i h w d ˜ d ( {D ) = { ˜ = w{ ˜d (w {e ) = w { ˜d w !e ( {D ) = w ! (2.5) w 1
The mapping w ! is a function of:
• • • •
the the the the
reference configuration, configuration at w, material coordinate system, spatial coordinate system.
Since we restrict our presentation to the Euclidean space (2.6) wY
w
where, p: mass of body B, Y : volume of B in the configuration at time w. Equation (2.6) incorporates an important postulate of Newtonian mechanics: the mass of a body is constant in time.
2.3 Motion of continuous bodies 2.3.1 Displacements In the mapping w ! ( w) e =
(2.8)
The displacement vector of the particle " from the reference configuration to the spatial configuration is, 1
See Appendix.
10
Nonlinear continua
Fig. 2.1. Motion of continuous body w
u("> w) = w x("> w)
x(")
(2.9a)
and the Cartesian components of this vector are, w
x ("> w) = w } ("> w)
} (") =
(2.9b)
2.3.2 Velocities and accelerations During the motion w !, the material velocity of a particle " in the w-configuration is C w x("> w) C w u("> w) = (2.10) Cw Cw assuming that the time derivatives in Eq. (2.10) exist. The material velocity vector is defined in the spatial configuration (see Fig. 2.2). We can have, alternatively, the following functional dependencies: w
v("> w) =
v = w v( {D > w) > w v = w v(w {d > w) = w
(2.11a) (2.11b)
Equation (2.11a) corresponds to a Lagrangian (material) description of motion, while Eq. (2.11b) corresponds to a Eulerian (spatial) description of
2.3 Motion of continuous bodies
11
Fig. 2.2. Material velocity of a particle "
motion. In general, the motion of solids is studied using Lagrangian descriptions while the motion of fluids is studied using Eulerian descriptions; however, this classification is by no means mandatory and combined descriptions have also been used in the literature (Belytschko, Lui & Moran 2000). In any case, we can refer the velocity vector either to the spatial coordinates or to the fixed Cartesian coordinates, w
v = w yd
w
gd >
(2.12a)
w
v = w y e =
(2.12b)
Assuming an arbitrary tensor field w = w ("> w) = w ( x> w) we define its temporal material derivative (Gw @Gw) as the time rate of the tensor w when we keep constant the particle " or, equivalently, when we keep constant the position vector x in the reference configuration. We call the material acceleration of a particle ", Gw v = (2.13) Gw In what follows, we determine the material acceleration vector considering the di erent combinations of: < ; < ; Vsdwldo @ ? ? Odjudqjldq @ + coordinates description > = > = I l{hg Fduwhvldq Hxohuldq w
a =
• Lagrangian description + spatial coordinates
12
Nonlinear continua
w
a =
C w yd d + w ef Cw
w e
y
w f
y
¸
w
gd >
(2.14a)
d where the w ef are the Christo el symbols of the second kind of the spatial coordinates {w {d } 2 . • Lagrangian description + fixed Cartesian coordinates w
a =
C wy e = Cw
(2.14b)
• Eulerian description + spatial coordinates The material particle that at time w is at the spatial location {w {d }, at time w + gw will be at {w {d + w yd dw}. Hence, Cwv Cwv dw + w e w y e dw Cw C { Considering that the base vectors, in a general coordinate system, are functions of the position, we have w+gw
w
a =
v = wv +
C w yd C w yd + w e Cw C {
w e
y +
w
d ef
w e
w f
y
y
¸
w
gd =
(2.15a)
• Eulerian description + fixed Cartesian coordinates w
a =
C w y C wy + w Cw C }
w
y
¸
e =
(2.15b)
2.4 Material and spatial derivatives of a tensor field Let w be an arbitrary tensor field, a function of time, and using a Lagrangian description of motion we get, w
= w ( {D > w) =
(2.16a)
Now, using an Eulerian description of motion, we get w
= w (w {d > w) =
(2.16b)
We indicate the first material time derivative (following the particle) as w
2
See Appendix.
˙ =
Gw C w ( {D > w) = | {D = Gw Cw
(2.17)
2.6 The deformation gradient tensor
13
The first spatial time derivative of a tensor w defined using a Eulerian w w d description is simply indicated as C (Cw{ >w) |w {d . Let us now calculate the material time derivative of a tensor w defined using an Eulerian description, w
= w d···e f···g (w {d > w) w gd = = = w ge w gf = = = w gg
(2.18)
it is easy to derive the following relation (Truesdell & Noll 1965, Slattery 1972), Cw Cw w ˙ = (2.19) + wys w s = Cw C { Using the spatial gradient of the tensor w 3 : u w = w gs =[
Cw C w {s
(2.20a)
C w d···e f···g w n···e w d w d···n w e + f···g ns + = = = + f···g ns C w {s
n n w d···e n···g w sf = = = w d···e f···n w sg ]
w s w
g
gd = = = w ge w gf = = = w gg
we can rewrite Eq. (2.19) as, w
˙ =
Cw + Cw
w
v · (uw ) =
(2.20b)
2.5 Convected coordinates Let us consider a body B and define in its reference configuration a system of curvilinear coordinates {l > l = 1> 2> 3}. The curvilinear coordinate system {l } is a convected coordinate system (Flügge 1972) if, when the body B undergoes a deformation process, for each configuration, the triad {l } that defines a particle ", is the same as in the reference configuration.
2.6 The deformation gradient tensor Let us consider the motion of the body B represented in Fig. 2.1. For the reference configuration (w = 0) we can write at the point (particle) ": 3
See Appendix.
dx =
d{D gD
(2.21a)
14
Nonlinear continua
where the vector dx at the point " in the reference configuration is called a material line element or fiber (Ogden 1984). Due to the motion w ! , the above defined fiber is transformed into a fibre in the spatial configuration, w
dx = w d{d w gd =
(2.21b)
We now define a second-order tensor: w X , the deformation gradient tensor at ", w
w X
dx =
· dx =
(2.22)
w
(2.23)
From the above equation, w X
C w {d C {D
=
gd
D
g =
Using the first of Eqs. (2.4) we get the following functional relation, w d [ D
=
w d E [ D ( { > w)
=
(2.24)
From Eq.(2.23), we see that the tensor w X has one base vector in the reference configuration and the other in the spatial configuration. Hence, it is a two-point tensor , (Marsden & Hughes 1983, Lubliner 1985). It is important to note that w [ d D is a function of, • the motion of the body (w !), • the material coordinate system, • the spatial coordinate system. For a regular motion, the tensor that is the inverse of
w 1 X
dx =
w X
at w x is,
· w dx
(2.25)
where, C {D gD w gd = (2.26) C w {d Using the second of Eqs. (2.4), we get the following functional relation, w 1 X
(w [
=
1 D )d
= (w [
1 D )d
(w {e > w) =
(2.27)
We define the transpose of w X at " using the following relation (Marsden & Hughes 1983, Strang 1980), (w X · dx) · w dx = if we now define w XW = (w [ W )Dd
gD
dx · (w XW · w dx) > w d
(2.28a)
g , we get from Eq.(2=28d),
2.6 The deformation gradient tensor w d [ D
d{D
w e
d {
w
jde =
d{D
jDE (w [ W )Ee
w d [ D
w
ED
w
e
d{
15
(2.28b)
hence, W
(w [ )Ee =
jde
j
=
(2.28c)
and therefore, W
(w [ )Ee = w
w
w E [e
=
(2.28d)
w
In the above equations, jde = gd · ge are the covariant components of the D
metric tensor in the spatial configuration at {w { } and j DE = gD · gE are the contravariant components of the metric tensor in the reference configuration at { {d } 4 . Referring the body B to a fixed Cartesian system, and using Eqs. (2.9a2.9b), = +
C w x > C}
(2.29a)
(w [ 1 ) =
C w x > C w }
(2.29b)
>
(2.29c)
w [
(w [ W ) =
w [
where : components of the Kronecker-delta. It is important to remember that when a problem is referred to a Cartesian system we do not need to make the distinction between covariant and contravariant tensorial components (Green & Zerna 1968). Example 2.1. JJJJJ In a fixed Cartesian system, a rigid translation is represented by a deformation gradient tensor with components w [ = . JJJJJ
Example 2.2. In the rigid rotation represented in the following figure, 4
See Appendix.
JJJJJ
16
Nonlinear continua
Rigid rotation We can directly calculate the components w [ using Eq. (2.29a) but it may be simpler to consider the following sequence: Step 1: Transformation from Cartesian coordinates to cylindrical coordinates in the reference configuration. q 1 = ( } 1 )2 + ( } 2 )2 µ 2 ¶ } C o 2 1 o ; ([ = tan ) = 1 }1 C } = }3 =
3
Without any motion, the change of the coordinate system in the reference configuration produces a deformation gradient tensor. Step 2: Rigid rotation. w 1
1
w 2
2
= =
+
;
([2 )s o =
C w s C o
w 3
= 3 =
Step 3: Transformation from cylindrical coordinates to Cartesian coordinates in the spatial configuration. w 1
} = w 1 frv w 2 } = w 1 sin w 2
w 2
;
([3 ) s =
C w } C w s
} = w 3 =
w 3
Without any further motion, the change of the coordinate system in the spatial configuration produces a deformation gradient tensor. Using the chain rule,
2.6 The deformation gradient tensor w [ w [
17
Cw} C w } C w s C o = C w s C o C } C } = ([3 ) s ([2 )s o ([1 )o =
For step 1, the derivation of ([11 ) o can be done by inspection. The array of these components is, 6 5 cos 2 1 sin 2 0 £ 1 ¤ [1 = 7 sin 2 1 cos 2 0 8 > 0 0 1 inverting
5
cos 2 1 [[1 ] = 7 1 sin 2 0 For step 2,
6 sin 2 0 1 2 8 = 0 1 cos 0 1
5
6 100 [[2 ] = 7 0 1 0 8 = 001
For step 3,
5
cos w 2 w 1 sin w 2 7 [[3 ] = sin w 2 w 1 cos w 2 0 0 Finally,
5
cos sin 7 sin frv [ = 0 0
£w
¤
6 0 08 = 1
6 0 08 = 1 W
[w [] = [L] , where An important feature of the above matrix is that [w [] w [L] is the unit matrix. That is to say, the matrix [ [] is orthogonal.JJJJJ
Example 2.3. JJJJJ For the motion represented in the following figure, we can derive the deformation gradient tensor directly by inspection,
18
Nonlinear continua
Simple deformation process 5
6 2=0 0=0 0=0 7 0=0 0=5 0=0 8 = [ = 0=0 0=0 0=6 ¤
£w
JJJJJ
Example 2.4. For the motion represented in the following figure,
JJJJJ
Shear deformation
}1 = } 1 + } 2 tan w 2 } = }2 w 3 } = }3 > w
therefore,
5
6 1 tan 0 70 1 08 = [ = 0 0 1
£w
¤
JJJJJ
2.6 The deformation gradient tensor
19
When there is a sequence of motions (some of them can be just a change of coordinate system) like the sequence depicted in Fig. 2.3, we can generalize the result in Example 2.2,
Fig. 2.3. Sequence of motions
qw d [ S
=
C qw {d C qw {d C w {o = (q1)w e · · · · · · S = S C { C { C {
(2.30a)
Therefore, qw X
=
qw (q1)w X
·
(q1)w (q2)w X
···
2w w X
·
w X
=
Example 2.5. It is easy to show that when using a convected coordinate system w d [ e
where the sor.
de
(2.30b)
JJJJJ
= de
are the mixed components of the Kronecker delta tenJJJJJ
For a motion w ! we define at a point " the Jacobian of the transformation (Truesdell & Noll 1965), w
w
M("> w) =
dY
dY
>
(2.31)
where dY is a di erential volume in the reference configuration and w dY is the corresponding di erential volume in the spatial configuration. Since in a regular motion, a nonzero volume in the reference configuration cannot be
20
Nonlinear continua
collapsed into a point in the spatial configuration and vice versa (Aris 1962), w M and w M 1 cannot be zero. In a fixed Cartesian system we can define, for a motion w !, } = w } ( } > w) =
w
(2.32)
The vectors (Hildebrand 1976) w
t =
C w } C}
w
( = 1> 2> 3)
e
(2.33)
are the base vectors, in the spatial configuration, of a convected coordinate system { } } and
dY = w dY =
Therefore,
d} 1 d} 2 d} 3 d} 1 d} 2 d} 3 [ w t1 · ( w t2 × w t3 )] = 5
C w }1 C }1
C w }2 C }1
Cw }3 C }1
C w }2 C }2
Cw }3 C }2
C w }2 C }3
Cw }3 C }3
(2.34a) (2.34b)
6 : : : : dY = : 8
(2.34c)
Since transpose matrices have the same determinant, ¯ ¯ w dY = ¯w [ ¯ dY
(2.34d)
w
9 9 9 w 1 dY = det 9 CC}}2 9 7 C w }1 C }3
where |w [| = det [w [] = When the motion of a body B is referred to a fixed Cartesian coordinate system (Malvern 1969), ¯ ¯ w M("> w) = ¯w [ ¯ = (2.34e) When in the reference configuration we use a curvilinear system { {D } and in the spatial configuration a system {w {d } , (Marsden & Hughes 1983): # " w ¸ w w d D C } } C { C { C w M = det = det w d D = (2.34f) C { C { C } C }
Following the reference (Green & Zerna 1968) and doing some algebra we can show that: w ¸¸2 ¯w ¯ £ ¤ ¯ jde ¯ = det w jde = det C } (2.34g) C w {d and
"
"
C {D | jDE | = det [ jDE ] = det C }
##2
=
(2.34h)
2.7 The polar decomposition
21
Finally, ¯ ¯ w M("> w) = ¯w [ ¯
s
|w jde | = | jDE |
Example 2.6. In a isocoric deformation (without change of volume) p ¯w ¯ p ¯ [ ¯ |w jde | = | jDE | =
(2.34i)
w
JJJJJ M = 1 , hence
When in the problem we use a fixed Cartesian coordinate system, we have ¯w ¯ ¯ [ ¯ = 1 = When we use convective coordinates ¯w ¯ ¯ jde ¯ = | jDE | =
JJJJJ
2.7 The polar decomposition The polar decomposition theorem (Truesdell & Noll 1965, Truesdell 1966, Malvern 1969, Marsden & Hughes 1983) is a fundamental step in the development of the kinematic description of continuous body motions. It allows us to locally (at a point ") decompose any motion into a pure deformation motion followed by a pure rotation motion or vice versa.
2.7.1 The Green deformation tensor The Green deformation tensor is defined at a point " as w C
=
w W X
·
w X
=
(2.35)
In some references, e.g. (Truesdell & Noll 1965, Truesdell 1966), the above tensor is referred to as right Cauchy-Green deformation tensor . Using Eq. (2.28c), we get h i h i w w d w w g w DE G gE w ge · > (2.36a) C = [ D jde j [ G gg g
and therefore,
22
Nonlinear continua w C
£w
DE d w e w [ D [ G jde j
=
¤
gE gG =
(2.36b)
It is important to note that the Green deformation tensor is defined in the reference configuration. Using an equivalent definition of transposed tensor to that given in Eq.(2.28a), we can write (w C · dx1 ) · dx2 =
dx1 · (w CT · dx2 )
(2.37a)
where dx1 and dx2 are two arbitrary vectors defined in the reference configuration at the point under study; after some algebra Eq. (2.37a) leads to w D w W D w D (2.37b) F E = ( F ) E = FE = The above equation indicates that the Green deformation tensor is symmetric. For an arbitrary vector w dx defined in the spatial configuration we can write the following equalities: w w
dx = w d{d w gd = w
w e
dx = d{e g
=
w d D w gd [ D d{ w g EU d{U w jge w ge [ E j
(2.38a) =
(2.38b)
=
(2.38c)
Hence, w
dx · w dx =
w d w g w EU d{D d{U [ D [ E jgd j
Using Eq. (2.36b), we write w
dx · w dx =
w U D d{U F D d{
=
dx · w C · dx =
(2.38d)
Considering that: • w dx · w dx 0 = • w dx · w dx = 0 +, |w dx| = 0 = • If w ! is a regular motion, |w dx| = 0 +, | dx| = 0 we w conclude that C is a positive-definite tensor (Strang 1980). 2.7.2 The right polar decomposition We define, in the reference configuration at the point under study, the right stretch tensor as w U
=
£w ¤1@2 C
(2.39)
and it follows immediately that the tensor w U inherits from w C the properties of symmetry and positive-definiteness (Malvern 1969).
2.7 The polar decomposition
23
We define the right polar decomposition as a multiplicative decomposition of the tensor w X into a symmetric tensor (w U) premultiplied by a tensor that we will show is orthogonal : the rotation tensor (w R) . Hence, w X w R
In order to show that
w W R w R
(ll)
and
w
w R
· w U =
(2.40)
is an orthogonal tensor we have to show that:
(l)
where
=
· ·
w R
w W R
=
g
= wg
g = DE gD gE is the unit tensor of the reference configuration
g = de w gd w ge is the unit tensor of the spatial configuration ( DE
and de are Kronecker deltas 5 ). To prove the first equality (l)> we start from Eq. (2.40) and get w R
w X
=
w X
· w U1 =
w d [ D
(w X 1 )DE w gd gE
=
(2.41)
The tensor w R defined by the above equation is, in the same sense as , a two-point tensor . The components of w R are: w d U D
=
w d [ O
(w X 1 )OD >
(2.42a)
and using an similar equation to (2.28c) we have (w UW )Ee =
w d [ O
(w X 1 )OD w jde j ED >
(2.42b)
hence, w W R
=
w d [ O
(w X 1 )OD w jde j ED gE w ge =
(2.42c)
Considering that w W X
and
=
w W U w W U
and since
·
G
g
w W U
·
w W X
=
w W X
>
U O
w g [ U
w
jge
(2.42e)
G w e
g
See Appendix.
g >
(2.42f)
gE we write
= (w X 1 )GO
w g [ O
w
jge
GE
j
gE w ge =
Comparing Eqs. (2.42g) and (2.42c) it is obvious that: 5
(2.42d)
= (w X 1 )GO gG gO >
= (w X 1 )GO
GE
j
UE w g w gE w g e [ U jge j
(2.42g)
24
Nonlinear continua W
w W R
= w U symmetry of Hence,
w 1 U
· w XW = w U). w W R
w R
·
=
·
w W X
w 1 U
(the last equality follows from the
w W X
·
·
w X
·
w 1 U
=
(2.42h)
Using also Eqs. (2.35) and (2.39), we obtain w W R
·
w R
=
w 1 U
·
w C
·
w 1 U
=
(2.42i)
g
and the first equality (l) is shown to be correct. To prove the second equality (ll)> we write (Marsden & Hughes 1983): w R
·
w W R
=
w R
·
³
w W R
w R
·
´
·
w W R
=
³
w R
·
w W R
´2
> (2.43)
and since w R cannot be a singular matrix, the second equality (ll) is shown to be correct. We will now show that the right polar decomposition is unique. Assuming that it is not unique, we can have, together with Eq. (2.40), another decomposition, for example: w X
˜ · w U ˜ > = w R
(2.44a)
˜ is an orthogonal tensor and w U ˜ is a symmetric tensor. where w R We can write w w W w w ˜ w ˜ (2.44b) C = X · X = U · U > and therefore, w ˜ U
=
£w ¤1@2 = C
(2.44c)
However, comparing the above with Eq. (2.39), we conclude that: w ˜ U
= w U =
(2.44d)
Then, from Eq. (2.44a), w ˜ R
= w X ·
w 1 U
>
(2.44e)
and comparing the above with Eq. (2.41), we conclude that: w ˜ R
= w R =
(2.44f)
Equations (2.44d) and (2.44f) show that the right polar decomposition is unique.
2.7 The polar decomposition
25
2.7.3 The Finger deformation tensor The Finger deformation tensor, also known in the literature as the left Cauchy-Green deformation tensor, is defined at a point " as: w
· w XW =
w X
b =
(2.45a)
Using Eq. (2.28c), we have h i h i w b = w [ gG w gg gG · w [ dD w jde j ED gE w ge
(2.45b)
and therefore,
w
b =
w g w d w ED w g g w ge [ E [ D jde j
=
(2.45c)
It is important to note that the Finger deformation tensor is defined in the spatial configuration. Proceeding in the same way as in Sect. 2.7.1, we can show that: • •
w w
b is a symmetric tensor. b is a positive-definite tensor.
2.7.4 The left polar decomposition We define the left polar decomposition as a multiplicative decomposition of the tensor w X into a symmetric tensor (w V) postmultiplied by the orthogonal tensor w R. Therefore, w w w (2.46) X = V · R = From the above equation, w V
=
w X
w U
and taking into account that w W V
· w RW =
=
w R
· w U · w RW
is symmetric, we get
w R
· w U · w RW =
The above equation shows that the tensor tensor , is symmetric. From Eq. (2.45a), we get w
b =
w X
· w XW =
and therefore, w V
(2.47a)
=
£
w
b
w V
w V
¤1@2
=
w V
=
(2.47b)
, known as the left stretch
· w V
(2.48a) (2.48b)
From the above equation we conclude that the left stretch tensor is defined in the spatial configuration and that it inherits from w b the positive definiteness. Proceeding in the same way as in Sect. 2.7.2 we can show that the left polar decomposition is unique.
26
Nonlinear continua t R
2.7.5 Physical interpretation of the tensors
t U
,
and
t V
In this Section, we will discuss a physical interpretation of the second-order tensors introduced by the polar decomposition. The rotation tensor w U
Assuming a motion in which
=
w X
g and therefore
=
w V
= w g ,we get
w R
(2.49)
and considering in the reference configuration, at the point under analysis, two arbitrary vectors dx1 and dx2 we have, in the spatial configuration: w
dx1 =
w R
· dx1
(2.50a)
w
dx2 =
w R
· dx2
(2.50b)
hence, in the spatial configuration we can write w
dx1 · w dx2 =
w d U D
w e U E
w
jde
d{D 1
d{E 2 =
(2.50c)
Using Eqs. (2.42a) and (2.42b) we can rewrite the above equation as w
and since
w R w
dx1 · w dx2 =
w d U D
(w UW )Fd
d{D 1
d{2F >
(2.50d)
is an orthogonal tensor, dx1 · w dx2 = FD d{D 1 d{2F =
The above equation shows that when
w X
=
dx1 · dx2 =
w R
(2.51)
:
• The corresponding vectors in the spatial and reference configuration have the same modulus. • The angle between two vectors in the spatial configuration equals the angle between the corresponding two vectors in the reference configuration. Hence, the motion can be characterized, at the point under analysis, as a rigid body rotation. We can generalize Eqs.(2.50a-2.50d) for any vector Y that in the reference configuration is associated to the point under analysis. For the particular motion described by w X = w R , we get w
y =
w R
·Y>
(2.52a)
and since the rotation tensor is orthogonal, Y =
w W R
· wy =
(2.52b)
If in the reference configuration there is a relation of the form: Y = A·W> where,
(2.53a)
2.7 The polar decomposition
27
Y > W : vectors defined in the reference configuration, A : second order tensor defined in the reference configuration, it is easy to show that: w
y =
h
w R
· A · w RW
i
· ww =
(2.53b)
In the above equation, the term between brackets is the result (in the spatial configuration) of the rotation of the material tensor A. If A is a symmetric second-order tensor we can write it using its eigenvalues and eigenvectors, A = DE D E >
(2.54a)
where, DE = 0
if D 6= E >
and the set of vectors D form an orthogonal basis in the reference configuration. In the spatial configuration we get, from the rotation of A: w
a =
w R
· A · w RW >
(2.54b)
and therefore, w
a = DE ( w R · D ) ( E · w RW ) =
(2.54c)
We now define in the spatial configuration the set of vectors w *d = w R · D , which obviously constitute an orthogonal basis; using Eq. (2.28a) we obtain ³ ´ ¡ ¢ (2.54d) E · w RW · w *e = w R · E · w *e >
and therefore,
w
a = DE ( w R · D ) ( w R · E ) =
(2.54e)
Comparing Eqs. (2.54a) and (2.54e), we conclude that: • The material tensor A and the spatial tensor w a have the same eigenvalues. • The eigenvectors of w a are obtained by rotating with w R the eigenvectors of A . Since, according to Eq. (2.47a) that:
w V
=
w R
·
w U
·
w W R
, we can assess
• The material tensor w U and the spatial tensor w V have the same eigenvalues. • The eigenvectors of w V (and w b ) are obtained by rotating with w R the eigenvectors of w U (and w C ).
28
Nonlinear continua
The right stretch tensor To study the physical interpretation of the right stretch tensor we consider, in the reference configuration, at the point " under analysis, two vectors dx1 and dx2 that in the spatial configuration are transformed into w dx1 and w dx2 w
dx1 =
w X
·
dx1
(2.55a)
w
dx2 =
w X
·
dx2 =
(2.55b)
After some algebra, w
dx1 · w dx2 =
dx1 · ( w XW ·
w X
)·
dx2 >
(2.56a)
and using Eqs. (2.35) and (2.39), we write w
dx1 · w dx2 =
dx1 · w C · dx2 =
dx1 · ( w U · w U ) · dx2 = (2.56b)
It follows from the above equation that the changes in lengths and angles, produced by the motion, are directly associated to the right stretch tensor w U . In the previous subsection we showed that these changes are nil when w g. U = The left stretch tensor Starting from Eqs. (2.55a-2.55b) and using a left polar decomposition, we get
dx1 ·
dx2 = w dx1 · ( w V1 ·
w 1 V
) · w dx2 =
(2.57)
It is obvious from the above equation that changes in lengths and angles, produced by the motion, are directly associated to the left stretch tensor w V . Above we showed that those changes are nil when w V = w g . 2.7.6 Numerical algorithm for the polar decomposition When analyzing finite element models of nonlinear solid mechanics problems, we usually know the numerical value of the deformation gradient tensor at a point and we need to use a numerical algorithm for performing the polar decomposition. In what follows, we present an algorithm that can be used for the right polar decomposition when we refer the problem to a fixed Cartesian system. s Starting from the matrix [w [] that is a (3 × 3)-matrix in the general case, we calculate the symmetric matrix, £w ¤ £ ¤W £w ¤ = w [ F [ =
(2.58a)
2.7 The polar decomposition
29
s
Using a numerical algorithm (Bathe 1996), we calculate the eigenvalues 2 w s D and eigenvectors [ D ] ; D = 1> 2> 3 of the matrix [ F]. From the above step,
where
£w ¤ = [ ] [] [ ]W F [ ] = [[ 1 ] [ 2 ] [ 3 ]]
(2.58b)
(2.58c)
and 5
6 2 (1 ) 0 0 [] = 7 0 (2 )2 0 8 = 0 0 (3 )2 s
(2.58d)
Using Eq. (2.39), we obtain (Strang 1980)
where
£w ¤ = [ ] []1@2 [ ]W X 6 1 0 0 [] = 7 0 2 0 8 = 0 0 3
(2.58e)
5
1 2
s
(2.58f)
Finally, using Eq. (2.40) we get
And [w U]
£w ¤ £ ¤ £w ¤1 = w [ = U X
(2.58g)
is now also completely determined.
JJJJJ Example 2.7. For the case analyzed in Example 2.4, and for = 15 we can write 5 6 1=0 0=26795 0=0 £w ¤ = 7 0=0 1=0 0=0 8 = [ 0=0 0=0 1=0 Hence,
30
Nonlinear continua
5 6 1=0 0=26795 0=0 £w W ¤ £w ¤ £w ¤ = [ = 7 0=26795 1=0718 0=0 8 = F [ 0=0 0=0 1=0
Solving for the eigenvalues and eigenvectors of [w F], we get 5 6 0=76556 0=0 0=0 [] = 7 0=0 1=30624 0=0 8 > 0=0 0=0 1=0 and,
5
[ ]
6 0=75259 0=65849 0=0 = 7 0=65849 0=75259 0=0 8 = 0=0 0=0 1=0
Using Eq. (2.58e), we write 5 6 0=99114 0=13279 0=0 £w ¤ 1@2 W = [ ] [] [ ] = 7 0=13279 1=02672 0=0 8 > X 0=0 0=0 1=0 and finally, using Eq. (2.58g), 5 6 0=99114 0=13279 0=0 £w ¤ £w ¤ £w ¤1 = 7 0=13279 0=99114 0=0 8 = U = [ X 0=0 0=0 1=0 We urge the reader to verify that: W [w U] [w U] = [L] w [ [] = [w U] [w X ] within the numerical accuracy used in the above calculations.
JJJJJ
Example 2.8. JJJJJ For the case analyzed in the previous example, we are now going to describe the deformation of a material fiber that in the reference configuration contains £ ¤ the (0> 0> 0) point and has the direction [ q]W = 0=0 1=0 0=0 . In the reference configuration, dx = dV n
dx ·
dx = ( dV)2
=
In the spatial configuration, w
dx = w dV w n w
Using Eq. (2.56b),
;
kw nk = 1
dx · w dx = (w dV)2 =
2.7 The polar decomposition
(w dV)2 = ( dV)2
£
w C
n ·
·
31
¤ n
and therefore, in the fixed Cartesian system that we are using, w
dV
dV
£
=
[ q]W [w F] [ q]
¤1@2
and using the numerical values calculated in the previous example, w
dV
= 1=03528 =
dV
The reader can check the above numerical values using very simple geometrical considerations. In the case of n = l , it is easy to show that w
dV
= l =
dV
For [ p]W =
£
1=0 0=0 0=0
¤
> we get w
dV
= 1=0 =
dV
The vectors m and n, which are orthogonal in the reference configuration, form an angle w in the spatial configuration, w
dxp = w dVp w m
;
kw mk = 1
dxq = w dVq w n
;
kw nk = 1
w w
dxp · w dxq = (w dVp ) (w dVq ) cos w = ( dV p ) ( dV q ) [ p]W [w F] [ q] µw ¶ µw ¶ dV dV cos w = [ p]W [w F] [ q] dV dV p q
hence, w
= cos
1
"
[ p]W [w F] [ q] ¡ w dV ¢ ¡ w dV ¢ dV
p
dV
q
#
and using the calculated numerical values, we get w
= 75 =
Once again, it is very simple for the reader to check the above numerical result. JJJJJ In the above examples we have numerically calculated the eigenvalues and eigenvectors of the tensor w C ; however, in some problems it is necessary to
32
Nonlinear continua
di erentiate those eigenvalues and eigenvectors and it is therefore necessary to use an analytical expression of them. As is wellknown the eigenvalues of w C are given by the roots of the following polynomial (Strang 1980), s(2l ) = 6l + L1F 4l L2F 2l + L3F = 0
(l = 1> 2> 3)
(2.59a)
where, (McConnell 1957) L1F = wu(w C) L2F =
(2.59b)
¤ 1 £ F 2 (L1 ) wu(w C2 ) 2
(2.59c)
L3F = ghw(w C) >
(2.59d)
and it is easy to verify the Serrin representation (Simo & Taylor 1991): w w
*d w *d = w 2d
D D = w 2D
w 1 b (L1F 2d ) w g + L3F 2 b d
2 4d L1F 2d + L3F 2 d w C
>
w 1 (L1F 2D ) g + L3F 2 D C
2 4D L1F 2D + L3F 2 D
(2.60a)
>
(2.60b)
with no addition in “a”or “A”in the above equations. According to what we showed in Sect. 2.7.5, d = D for d = D .
JJJJJ
Example 2.9. To verify Eq. (2.60a)we start from, w
b = 2l w *l w *l
w 1
b
w = 2 *l w *l l
L1F = 21 + 22 + 23 L2F = 21 22 + 21 23 + 22 23 L3F = 21 22 23 = For d = 1 w
w 1 b (L1F 21 )w g + L3F 2 = 1 b
241 L1F 21 +L3F 2 1 w *1 w *1 = 21
The above verifies Eq. (2.60a) for the case d = 1; the demonstrations for d = 2> 3 are identical.
2.8 Strain measures
33
To verify Eq. (2.60b) we start from, w C 1
w C
= L 2 L L = L 2 L L JJJJJ
and proceed as before.
It is important to note that Eqs. (2.60a-2.60b) are only valid if the denominator of the r.h.s. is not zero. The denominator is zero if we have repeated eigenvalues.
2.8 Strain measures In the literature we can find a large number of strain measures that have been proposed to characterize a deformation process. There are di erent approaches for analyzing the deformation of continuum bodies and we usually find that, for a given approach, one particular strain measure may be more suitable than others. In this section we will present a number of these strain measures without making any claim of completeness.
2.8.1 The Green deformation tensor We have already presented the Green deformation tensor in Sect. 2.7.1. It is important to remember that this second-order tensor is defined in the reference configuration and that for two vectors dx1 and dx2 defined at a point " in the reference configuration, the corresponding vectors in the spatial configuration satisfy the relation, w
dx1 · w dx2 =
dx1 ·
w C
·
dx2 =
(2.61)
2.8.2 The Finger deformation tensor We have already presented the Finger deformation tensor in Sect. 2.7.3. It is important to remember that this second-order tensor is defined in the spatial configuration. Using Eq. (2.45a), w 1
b
and for two vectors w dx1 and configuration we can write,
= w
w W X
·
w 1 X
>
dx2 defined at a point
(2.62) w
x in the spatial
34
Nonlinear continua w
dx1 · w b1 · w dx2 = w dx1 ·
w W X
·
dx2
(2.63a)
using Eq. (2.28a), we get w
dx1 · w b1 · w dx2 =
dx1 ·
dx2 =
(2.63b)
2.8.3 The Green-Lagrange deformation tensor From Eq.(2.61),
w
w
dx1 · dx2
dx1 ·
1 = 2 dx1 · (w C 2
dx2
g)
¸
·
dx2 = (2.64)
The Green-Lagrange strain tensor is defined in the reference configuration as
1 w (2.65) ( C g) = 2 The second order tensor w % describes the deformation corresponding to the w-configuration (spatial configuration) referred to the configuration at w = 0 (reference configuration). w %
=
Example 2.10. JJJJJ © ª Considering a convected coordinate system l with covariant base vectors we el in the reference one, we can write, gl in the spatial configuration and g w %
=
and it is easy to show that, w %op e
=
w %op e
o
p
e g
1 hw eo · w g ep g 2
e g
eo · g
ep g
i
= JJJJJ
At the point " under study, we now evolve from the w-configuration to a R. Hence, w + w-configuration by means of a rotation w+w w w+w X w+w C
= =
w+w R w w W X
·
·
w X
>
w+w W R w
(2.66a) ·
w+w R w
·
w X
>
(2.66b)
and taking into account that the rotation tensor is orthogonal, we get
2.8 Strain measures
35
w+w C
w C
(2.66c)
w+w %
w %
(2.66d)
and therefore, =
From the above, we conclude that the Green deformation tensor and the Green -Lagrange strain tensor are not a ected by rigid body rotations: that is to say they are indi erent to rotations. 2.8.4 The Almansi deformation tensor From Eq. (2.63b), we get w
dx1 · w dx2 dx1 · dx2 = 2 w dx1 ·
1 w ( g w b1 ) 2
¸
· w dx2 = (2.67)
The Almansi strain tensor is defined in the spatial configuration as 1 w (2.68) ( g w b1 ) = 2 At the point " under study, we now evolve from the w-configuration to the w + w-configuration by means of a rotation w+w R. Hence, w w
e =
w+w 1 X
=
w 1 X
·
w+w W R w
>
(2.69a)
w W X
>
(2.69b)
and, w+w W X
=
w+w R w
using Eq. (2.62), w+w 1
b
·
=
w+w R w
· w b1 ·
e =
w+w R w
· we ·
w+w W R w
>
(2.69c)
and therefore, w+w
w+w W R w
=
(2.69d)
Hence, the Finger and Almansi tensors are a ected by rigid-body rotations. 2.8.5 The Hencky deformation tensor The Hencky or logarithmic strain tensor is defined in the reference configuration as w w (2.70) H = ln U = When the problem is referred to a fixed Cartesian system using Eq. (2.58e), we get 6 5 ln 1 0=0 0=0 [w K] = [ ] 7 0=0 ln 2 0=0 8 [ ]W = (2.71) 0=0 0=0 ln 3 Obviously, the Hencky deformation tensor is indi erent to rotations, since from the polar decomposition, we can see that w U does not incorporate the e ect of rigid-body rotations.
36
Nonlinear continua
2.9 Representation of spatial tensors in the reference configuration (“pull-back”) For the regular motion depicted in Fig. 2.1, we can define: • An arbitrary curvilinear coordinate system {w {d } in the spatial configuration. At a point " (w {d > d = 1> 2> 3) we can determine the covariant base vectors w gd and the contravariant base vectors w gd . • An arbitrary curvilinear coordinate system { {D } in the reference configuration. At the point " ( {D > D = 1> 2> 3) we can determine the covariant base vectors gD and the contravariant base vectors gD . • A convected curvilinear coordinate system {l }. At the point " in the ˜ d and spatial configuration we can determine the covariant base vectors w g w ˜d the contravariant base vectors g > while in the reference configuration ˜ d and the contravariant we can determine the covariant base vectors g ˜d base vectors g 2.9.1 Pull-back of vector components Let us consider in the spatial configuration at the point " a vector, w
el = w˜el w g el = b = w el w gl = w el w gl = w˜el w g
(2.72)
We define in the reference configuration the following vectors (Dvorkin, Goldschmit, Pantuso & Repetto 1994): w
B` = w˜el
w
el = [ w B^ ]D gD = B^ = w˜el g
After some algebra,
el = [ w B` ]D gD g
(2.73a) (2.73b)
[w B` ]D = w em (w [ 1 )Dm
(2.74a)
[w B^ ]D = w em w [ mD =
(2.74b)
Adopting the notation used in manifolds analysis (Lang 1972, Marsden & Hughes 1983) we define the pull-back of the contravariant components w em as £w
! (w em )
¤D
= [w B` ]D
and the pull-back of the covariant components £w
! (w em )
¤
D
w
(2.75a)
em as:
= [w B^ ]D =
We can therefore rewrite Eqs. (2.73a-2.73b) and (2.74a-2.74b),
(2.75b)
2.9 Representation of spatial tensors in the reference configuration (“pull-back”) w
B` = w em (w [ 1 )Dm gD = w em (w [ 1 )Dm
w
B^ = w em w [ mD gD = w em
m w [ D
DF
j
jDF
F
g
gF =
(2.76a) (2.76b)
For two vectors w b and w w , defined in the spatial configuration at " , using Eqs. (2.74a-2.74b), it is easy to show that: w
B` · w W^ = w B^ · w W` = w b · w w =
(2.77)
Also, using Eqs.(2.74a-2.74b) and (2.36a-2.36b), we get [w B` ]E w FDE = [w B^ ]D =
(2.78)
Using Eqs. (2.73a-2.73b), we can write ed )` = (w g
ed )^ = (w g
ed g
(2.79a)
d
e = g
(2.79b)
Hence, we use the following notation (Moran, Ortiz & Shih 1990): w w
ed ) = (w g e d )` = ! (g
w w d
e ) = ( wg ed )^ = ! (g
ed g
d
e = g
(2.79c) (2.79d)
From the above equations, we can get by inspection the geometrical interpretation of the vectors w B` and w B^ : • If w b, in the spatial configuration, is the tangent to a curve w c() at a point ", then w B` is the tangent, in the reference configuration, to the curve C() = w !1 [w c()] , at the point ". • In the transformation w B` $ w b the modulus of the original vector gets stretched as the material fiber to which they are tangent. In convected coordinates we have
w
el dx = dl w g
dx = dl
that is to say, w
dX` =
(2.80a)
el g
(2.80b)
dx =
(2.80c)
• For two vectors w b and w w that are orthogonal in the spatial configuration it is obvious that:
37
38
Nonlinear continua
Fig. 2.4. Mappings
w
B` · w W^ = w B^ · w W` = w b · w w = 0 =
(2.81)
Hence, the orthogonality of w b and w w implies the orthogonality of B and w W^ and the orthogonality of w B^ and w W` in the reference configuration. w
`
It is important to take into account that in Eqs. (2.74a-2.74b) the terms on the r.h.s. must be written as a function of the coordinates in the reference configuration. We can indicate this using a more formal nomenclature (e.g. Marsden & Hughes 1983), [w B` ]D = [w B^ ]D =
£w £w
! (w ed ) ! (w ed )
¤D ¤
D
= =
£ w 1 D ¤ ( [ ) d w ! (w ed w !)
w d [ D
(w ed w !) =
(2.82a) (2.82b)
In order to understand the above equations we use Fig. 2.4 (Marsden & Hughes 1983). In this figure we indicate with “i j” the composition of the mapping “j” followed by the mapping “i ”.
Example 2.11. JJJJJ For a function i (w {d ) defined in the spatial configuration, we can write:
2.9 Representation of spatial tensors in the reference configuration (“pull-back”)
Ci w d d{ = C w {d In the above equation, we use a formal analogy with vector calculus in which (Marsden & Hughes 1983): di is a vector; CCi w {d are its covariant components (did ) and gw {d are contravariant base vectors. Hence we can do a pull-back operation, di =
£w
¤ ! (did ) D =
w d [ D
did =
C w {d Ci Ci = D = C {D C w {d C {
Using a more formal nomenclature and the mappings in Fig. 2.7, we get £w
¤ C(i w !) ! (did ) D = = C {D
JJJJJ
Example 2.12. JJJJJ Equation (2.11b) defines, in the spatial configuration, the velocity of a material point, w v = w y d w gd = Using the expressions for the pull-back of contravariant components, we write £w
! (w y d )
¤D
= (w [ 1 )Dd w yd =
If the coordinate system { {D }, defined in the reference configuration, is a convected system with covariant base vectors, w g ˜D , in the spatial configuration, we can write eD = w d{d w gd d{D w g hence,
w
and therefore, w
eD gd = (w [ 1 )Dd w g
eD = v = w yd (w [ 1 )Dd w g
The components of the material velocity vector in the convected system { {D } are, w D y˜ = w y d (w [ 1 )Dd and therefore
£w
¤D ! (w y d ) = w y˜D =
JJJJJ
39
40
Nonlinear continua
2.9.2 Pull-back of tensor components Let us consider in the spatial configuration at the point " (w {d > d = 1> 2> 3) a second-order tensor, w
w
l
t = w wlm gl w gm = w wlm w gl w gm = w w w
m
w
gl w gm
l
el w g em = w w˜lm w g el w g em = w w˜ m w g el w g em = w w˜lm g
=
(2.83)
We define in the reference configuration the following second-order tensors (Dvorkin, Goldschmit, Pantuso & Repetto 1994): w
T` = w w˜lm
w
el g em = [ w T_ ]DE gD gE > T_ = w w˜l m g
w
el g em = [ w T` ]DE gD gE > g
(2.84a) (2.84b)
el g em = [ w T^ ]DE gD gE = T^ = w w˜lm g
(2.84c)
[w T` ]DE = w wde (w [ 1 )Dd (w [ 1 )Ee >
(2.85a)
[w T_ ]DE = w wde (w [ 1 )Dd (w [)eE >
(2.85b)
[w T^ ]DE = w wde (w [)dD (w [)eE =
(2.85c)
After some algebra we get
We define: • Pull-back of the contravariant components of £w
! (w wlm )
¤DE
• Pull-back of the mixed components of £w
! (w wl m )
¤D
E
! (w wlm )
¤
t,
= [w T` ]DE = w
= [w T_ ]DE =
DE
(2.86a)
t,
• Pull-back of the covariant components of £w
w
w
(2.86b)
t,
= [w T^ ]DE =
From Eqs. (2.84a-2.84c) and (2.85a-2.85c) we can write,
(2.86c)
2.9 Representation of spatial tensors in the reference configuration (“pull-back”) w
T` =
w de
w
(w [ 1 )Dd (w [ 1 )Ee
gD gE
= w wde (w [ 1 )Dd (w [ 1 )Ee jDO jEP gO gP = w wde (w [ 1 )Dd (w [ 1 )Ee jDO gO w
T_ =
w d
w
e
(w [ 1 )Dd (w [)eE
EO
j
= w wd e (w [ 1 )Dd (w [)eE
= w wd e (w [ 1 )Dd (w [)eE w
T^ =
w
wde (w [)dD (w [)eE
gE >
gD gO
O E
jDO
g
g
gD gE >
DO
j
= w wde (w [)dD (w [)eE
D E
= w wde (w [)dD (w [)eE
EO D
g j
(2.87b)
EP
j
(2.87a)
g O gP
g
g
gO =
(2.87c)
For two tensors w t and w w defined in the spatial configuration at " ( w {d > d = 1> 2> 3) , using Eqs. (2.84a-2.84c), it is easy to show that: w
T^ :
w
W` = w T` :
w
W^ = w t :
w
w
(2.88)
and also, using Eqs.(2.87a-2.87c), we can show that
w
[w T^ ]DE = [w T_ ]SE w FS D
(2.89a)
[w T^ ]DE = [w T` ]S T w FS D w FTE =
(2.89b)
If in the spatial configuration, at the point " (w {d > d = 1> 2> 3) , two vectors b and w w are related by the second order tensor w t, via the equation, w
b = wt · ww
(2.90)
in the reference configuration, we can easily verify that the following relations are fulfilled: `
w
B` = w T · w W^
w
B^ = w T · w W`
w
B` = w T · w W` =
^ _
(2.91a) (2.91b) (2.91c)
41
42
Nonlinear continua
Example 2.13. JJJJJ Instead of using the mixed components w wl m , it is possible to use the components w wml , hence w
˜m wg ˜l t = w wml w gm w gl = w w˜ml w g
we can then define in the reference configuration the second order tensor, w
˜m g ˜ l = [w T ]DE gD gE T = w w˜ml g
after some algebra we then get, [w T ]DE = w wde (w [ 1 )Ee (w [)dD
=
Therefore, [w ! (w wml )]DE = [w T ]DE = Starting from Eq.(2.90), we can also show that, w
B^ = w T · w W^ = JJJJJ
2.10 Tensors in the spatial configuration from representations in the reference configuration (“push-forward”) In the previous section we obtained representations in the reference configuration of tensors defined in the spatial configuration (pull-back). The inverse operation is named, in the manifold analysis literature (Lang 1972, Marsden & Hughes 1983), push-forward . For a second-order tensor, from Eqs.(2.85a-2.85c), we can write: w de
w
w
=
wde =
w d we
=
h h h
`
w
! [w T ]DE
w
! [w T ]DE
w
^
_
! [w T ]DE
ide i
de
id
e
=
w d w e w ` DE [ D [ E [ T ]
(2.92a) ^
= (w [ 1 )Dd (w [ 1 )Ee [w T ]DE =
w d [ D
_
(w [ 1 )Ee [w T ]DE =
(2.92b) (2.92c)
2.11 Pull-back/push-forward relations between strain measures
JJJJJ
Example 2.14. Using Eqs. (2.92a-2.92c) we can show that, £w
43
¤ ¤o £ ! (ZD ) d = (w e1 )do w ! (Z D ) =
JJJJJ
2.11 Pull-back/push-forward relations between strain measures In the two previous Sections we defined representations of the types known as pull-back and push-forward. As we will see later on, these kinds of representations are extremely useful in nonlinear continuum mechanics. In Sect. 2.8 we defined a number of strain measures, some of them in the spatial configuration (e.g. the Finger and Almansi tensors) and some of them in the reference configuration (e.g. the Green, Green-Lagrange and Hencky tensors). In the present section we will establish relations of the pull-back/pushforward type between those strain measures. We define, as usual, at the material point ": In the spatial configuration a coordinate system {w {d } with covariant base vectors w gd . In the reference configuration a coordinate system { {D } with covariant base vectors gD . We can therefore calculate at " the deformation tensor w X . • The pull-backs of the spatial metric tensor are: £w
£w
¤ ! (w jde ) DE
¤DE ! (w j de )
D E
g
g
= w g^ =
w C
>
(2.93a)
w 1 C
gD gE = w g` =
=
(2.93b)
• The pull-back of the Almansi strain tensor is: £w
! (w hde )
¤
DE
D
g
E
g
= w E^ =
w %
=
(2.94a)
From Eqs. (2.77)>(2.80a-2.80c) and (2.91a-2.91c), we get w
dx · w e · w dx =
dx ·
• The pull-back of the left stretch tensor is:
w %
·
dx =
(2.94b)
44
Nonlinear continua w _ V
=
w U
=
(2.95)
• In many problems related to metallurgy (e.g. metal-forming problems) the usual practice is to use a logarithmic strain measure (Hill 1978). Therefore, in the spatial configuration the following strain measure is defined w
The pull-back of the tensor
h = ln w V = w
h is:
_
= w H = ln w V_ = ln w U =
w H
(2.96a)
(2.96b)
The above tensor is known as the Hencky deformation tensor. In following Chapters we will see the importance of the Hencky strain tensor for the analysis of finite strain problems (Anand 1979). Some recent finite element formulations, developed for the analysis of finite strain elastoplastic problems use this strain measure (e.g. Rolph & Bathe 1984, Weber & Anand 1990, Eterovic & Bathe 1990, Simo 1991, Dvorkin, Pantuso & Repetto 1992\1993 \1994\1995, Dvorkin 1995a\1995b \1995c, Pèric, Owen & Honnor 1992). It is useful to note that we also get Eqs. (2.95) and (2.96a-2.96b) when instead of searching for a representation in the reference configuration, we W search for a representation in a configuration rotated by w R from the spatial configuration: corotational representation. • The push-forward of the reference configuration metric tensor is: £
£
w
w
! ( jDE ) ! ( j DE )
¤
w d w e
g
de
¤de
g
= (w [ 1 )Dd (w [ 1 )Ee jDE w gd w ge = w b1
w
g d w ge =
w d w e DE w gd w ge [ D [ E j w
= b=
(2.97a)
(2.97b)
In Chap. 3 we will study relations of the pull-back/push-forward type between stress measures.
2.12 Objectivity The description of physical phenomena using objective formulations is a central topic in continuum mechanics. We will first present the classical concept of objectivity under rotations and translations (isometries) (Truesdell & Noll 1965). Next, we will present the concept of objectivity under general changes of the reference frame (Marsden & Hughes 1983), we will use the word covariance to refer to this concept.
2.12 Objectivity
45
2.12.1 Reference frame and isometric transformations We call an event the pair {w x> w} formed by a vector w x that defines a point in the Euclidean space and a time w. A reference or observation frame is a way of relating the physical world to the points in an 0> 0) (origin of the fixed Cartesian frame) to w z = (0> 0> 0) (origin of the moving Cartesian frame). An observer on the moving frame defines an event with the vector w z and the time w . An observer on the fixed frame defines the same event with the vector w z and the time w. Let us assume that the two observers are observing a lab experiment, e.g. the measurement of the stretching of a spring when it is loaded with a weight of 1 kg. Let us also assume that the lab is moving with the moving frame; for the observer on this frame w z is the position vector of the spring-end. The observer on the fixed frame will see the spring-end moving: w
z(w) = c(w) + Q(w) · w z =
(2.99a)
Since we are considering now isometric transformations, the following condition holds:
46
Nonlinear continua
w = w d >
(2.99b)
where d is a constant. For simplicity, from here on, we will consider d = 0 (w = w ). If we include the possibility that Q(w) represents not only rotations but also reflections (transformations between left-handed and right-handed systems), Eqs. (2.99a-2.99b) represent the most general isometric transformation (Truesdell & Noll 1965, Truesdell 1966). We should not confuse the concept of change of reference frame with the concept of change of coordinates system, the latter being an instant concept does not incorporate the frame velocity. An isometric change of reference frame may induce changes in scalars, vectors and tensors. • Scalars do not change during an isometric transformation. • Vectors defined in the spatial configuration can always be considered as proportional to the di erence between two position vectors in that configuration (Truesdell & Noll 1965); hence, using Eq. (2.99a) we get w
v = Q(w) · w v =
(2.100)
The above is the transformation law for spatial vectors under an isometric transformation of reference frame. • Second-order tensors defined in the spatial configuration relate vectors defined in the same configuration (quotient rule)6 . In the moving frame, we can write for an arbitrary second-order tensor w s w
v
= w s · w w =
(2.101a)
Using Eq.(2.100), w
v =
h i Q(w) · w s · QW (w) · w w =
(2.101b)
Therefore, the transformation law for spatial second-order tensors under an isometric transformation of reference frame is w
s = Q(w) · w s · QW (w) =
(2.101c)
• For spatial tensors of higher order, the transformation laws can be derived in an identical way. 6
See Appendix.
2.12 Objectivity
47
2.12.2 Objectivity or material-frame indi erence Let us assume a deformation process taking place in the moving reference frame. This deformation process can be referred to a fixed reference configuration. There are general tensors (including scalars and vectors) defined in the reference configuration (e.g. the Green-Lagrange strain tensor), they are called material or Lagrangian tensors. There are general tensors defined in the spatial configuration (e.g. the Almansi strain tensor, the material velocity), they are called spatial or Eulerian tensors. There are general tensors defined in both configurations (e.g. the deformation gradient tensor), they are called two-point tensors. Following (Lubliner 1985) we define the following objectivity criteria under isometric transformations of a reference frame (classical objectivity): A Lagrangian tensor is objective if it is not a ected by changes of the reference frame. An Eulerian tensor is objective if, under a change of reference frame, transforms according to Eqs. (2.100) and (2.101c). A two points second order tensor is objective if, when operating on a Eulerian objective vector, produces a Lagrangian objective vector.
Example 2.15. If we di erentiate Eq. (2.99a) with respect to time we get, w
˙ z˙ (w) = w c˙ (w) + Q(w) · w zB + Q(w) · w z˙ B =
Hence, the velocity is not an objective vector.
JJJJJ
JJJJJ
In the same way we can show that the acceleration vector is not objective. Therefore, even though forces are spatial objective tensors, Newton’s second law (w F = p w x ¨) is not objective and is only applicable in inertial frames (Truesdell & Noll 1965). In what follows, we will analyze the objectivity of some of the tensors previously defined: • The deformation gradient tensor , in the moving frame, satisfies the following relation: w
dx =
w X
·
dx =
(2.102a)
48
Nonlinear continua
• The vector dx is an objective Lagrangian vector and w dx is an objective Eulerian vector, hence w X fulfills the objectivity definition. In the fixed frame, QW (w) · w dx =
w X
·
dx >
(2.102b)
=
(2.102c)
and finally, w X
w X
= Q(w) ·
Equation (2.102c) is the transformation law for objective two-point secondorder tensors. • Performing a right polar decomposition on both sides of Eq. (2.102c), we get w R
·
w U
= Q(w) ·
w R
·
w U
=
(2.103a)
Taking into account that: The inner (dot) product of two orthogonal second-order tensors is an orthogonal second order tensor. The polar decomposition is unique. We get
w R
= Q(w) ·
w U
=
w U
w R
=
(2.103b) (2.103c)
Hence, the rotation tensor (two-point tensor) and the right stretch tensor (Lagrangian tensor) are objective under isometric transformations. • From Eq. (2.47b), we can write w V
=
w R
·
w U
·w RW =
(2.104a)
and using Eqs. (2.103a-2.103c), we obtain w V
= Q(w) ·
w V
· QW (w) =
(2.104b)
The above equation shows that the left stretch tensor (Eulerian tensor) is objective under isometric transformations. • The Green-Lagrange strain tensor (Lagrangian tensor) is (Eq. (2.65))
2.12 Objectivity
w %
=
1 hw W X · 2
w X
and using Eq. (2.102c), we get
w %
=
g
i
49
(2.105a)
w B %
(2.105b)
The above equation depicts an objective behavior under isometric transformations. • The Almansi strain tensor (Eulerian tensor) is (Eq. (2.68)): w
e =
1 hw g 2
w W X
·
w 1 X
and using Eq. (2.102c), we get w
e = Q(w) · w e
i
· QW (w) =
=
(2.106a)
(2.106b)
The above equation depicts an objective behavior under isometric transformations. 2.12.3 Covariance Let us assume a body that remains undeformed, referred to a spatial coordinate system that keeps changing (e.g. at a time w we have the spatial system {w {d } and at a time wˆ the system {wˆ{ ˆd }). For a spatial second order tensor w a , using the usual tensor transformations, we can write (Truesdell & Noll 1965):
=
C wˆ{ ˆd C wˆ{ ˆe w op d > C w {o C w {p
(2.107a)
d ˆde =
C w {o C w {p w dop > C wˆ{ ˆd C wˆ{ ˆe
(2.107b)
ˆd C w {p w o C wˆ{ dp= C w {o C wˆ{ ˆe
(2.107c)
wˆ de
d ˆ
wˆ
wˆ d d ˆe
=
Between the spatial coordinates of the material particles at w and the spatial coordinates of the same particles at wˆ we can define a mapping (wwˆ!) (see Eq. (2.4)). Hence, we can also define a deformation gradient tensor, wwˆX , and we can rewrite Eqs. (2.107a-2.107c) as
50
Nonlinear continua w de
d
w
dde
w d de
h ide ˆ op ˆ ˆ ˆ ˆ op = (ww [ 1 )do (ww [ 1 )ep w d ˆ = ww ! (w d ˆ ) > h i ˆ ˆ ˆ ˆ ˆ = ww [ od ww [ pe w d ˆop = ww ! (w d ˆop ) > ˆ
ˆ
ˆ
= (ww [ 1 )do ww [ pe w d ˆo p =
de
h
wˆ wˆ o ˆp w! ( d
)
id
e
=
(2.108a) (2.108b) (2.108c)
If we consider now general transformations between the spatial configurations at w and wˆ (not necessarily restricted to simple changes of coordinate system) the spatial tensor w a is defined as covariant or objective (in a more general way than the above defined objectivity under isometric transformations) if under the mapping (wwˆ!) it transforms following Eqs.(2.108a-2.108c) (Marsden & Hughes 1983). For a two-point tensor , the covariance criterion is only applied to the indices associated to the spatial basis (Lubliner 1985). A Lagrangian tensor is always covariant if it is not a ected by changes of the reference frame. The reader can easily check that for the case of isometric transformations the concept of covariance is coincident with the classical concept of objectivity presented in the previous section. A physical law is objective (either in the classical or in the covariant sense) if all the tensors in its mathematical formulation are objective.
2.13 Strain rates In the previous sections we presented a static description of the kinematics of continuous media: given a spatial and a reference configuration we developed tools to relate both configurations (deformation gradient tensor, strain measures, etc.) In the present section we will study the kinematic evolution of the spatial configuration. For this purpose we will introduce the time rates of the di erent tensors described above. 2.13.1 The velocity gradient tensor The time rate of Eq. (2.23) is w d C y w ˙ + X = C {D
w o w d w e [ D oe y
where w yd was defined in Eq. (2.10).
¸
w
gd g D >
(2.109a)
2.13 Strain rates
51
It is important to remember that the functional dependence is w ˙d [ D
=
w ˙d E [ D ( { > w)
=
(2.109b)
Using the chain rule in Eq. (2.109a), w ˙d [ D
= w yd |o w [ oD =
(2.109c)
We define in the spatial configuration the velocity gradient tensor, w
l = w y d |o w gd w go >
(2.110a)
we can write the above as w
l = wv u >
w W
l
(2.110b)
= uw v =
(2.110c)
= w od o w [ o D
(2.111a)
Hence, we can write Eq.(2.109c) as w ˙d [ D
and therefore, w ˙ X
= wl ·
w X
=
(2.111b)
It is important to realize that the above is the material time derivate of w ˙ = G X . the deformation gradient tensor, w X Gw 2.13.2 The Eulerian strain rate tensor and the spin (vorticity) tensor We can decompose the velocity gradient tensor into its symmetric and skewsymmetric components: w l = wd + w$ (2.112a) where, 1 w W (2.112b) ( l + wl ) 2 is the Eulerian strain rate tensor (defined in the spatial configuration) and, w
w
d = w dW =
$ = w $W =
1 w W ( l wl ) 2
(2.112c)
is the spin or vorticity tensor , also defined in the spatial configuration. Let us assume a deformation process referred to a fixed Cartesian system. The principal directions of w U form, in the reference configuration, a Cartesian system known as Lagrangian system. The principal directions of w V form, in the spatial configuration, a Cartesian system known as a Eulerian system (Hill 1978).
52
Nonlinear continua
Fig. 2.5. Rotations
We can go from one of the above-defined coordinate systems to another one using the rotation tensors sketched in Fig. 2.5. From Fig. 2.5, we get w
RH =
w R
w RO
·
=
(2.113)
For two consecutive rotations, w+w R
=
w+w R w
w R
·
(2.114a)
and therefore, w ˙ R
= lim w $ 0
" w+w w
R wg w
#
·
w R
=
(2.114b)
We can define a rotation rate w
U = lim w $ 0
" w+w w
R wg w
#
(2.114c)
and using it in Eq. (2.114b) (Hill 1978), we get w ˙ R
= w U · w R
(2.115a)
= w O · w RO >
(2.115b)
˙ = w · wR = R H H H
(2.115c)
in the same way, w ˙ RO w
2.13 Strain rates
53
Since the rotation tensors are orthogonal we can write w W R
w R
·
=
g>
(2.116a)
taking the time derivative of the above equation and using Eq. (2.115a), we have w
U + w WU = 0 (2.116b) in the same way, w O w
w W O
= 0>
(2.116c)
H + w WH = 0 =
(2.116d)
+
The above equations indicate that w U , symmetric tensors.
w O
and w H are skew-
2.13.3 Relations between di erent rate tensors The time derivative of Eq. (2.113) leads to w
H · w RH = w U ·
w R
·
w RO
w R
+
w O
·
·
w RO
>
(2.117a)
and therefore, w W R
· (w H w U ) ·
w R
=
w O
=
(2.117b)
Using Eqs. (2.111b) and (2.40), w
l =
w ˙ R
·
w W R
+
w R
·
w ˙ U
w 1 U
·
·
w W R
>
(2.118a)
splitting the above equation into its symmetric and skew-symmetric components, we get w W R
· wd ·
w R
=
1 w ˙ ( U · 2
w 1 U
+
w 1 U
·
w ˙ U)
(2.118b)
and w W R
· (w $ w U ) ·
w R
=
1 w ˙ ( U · 2
w 1 U
w 1 U
·
w ˙ U)
= (2.118c)
It is very important to recognize that (Hill 1978): w U
=
g =, w $ = w U =
(2.118d)
An example of the above situation is the beginning of the deformation process (w = 0). In the deformation process depicted in Fig. 2.6 (Truesdell & Noll 1965, Malvern 1969) we can write, using Eqs. (2.30a-2.30b):
54
Nonlinear continua
Fig. 2.6. Relative deformation gradients X
=
wX
·
w X
=
(2.119a)
For a fixed w-configuration, we can write d d X = X · d d w
w X
=
(2.119b)
Using Eq. (2.111b) and the polar decomposition in the above equation, we get d d R · w U + w R · U) · w X > (2.119c) d w d w for = w it is obvious that w U = w R = g , and since the above equation has to hold for any w X,
l ·
X
= (
d d U | =w = w l = w R | =w + d d w
(2.119d)
It is easy to show that the first tensor on the l.h.s. of the above equation is skew-symmetric and the second one is symmetric; hence, d 1 w ( l w lW ) = w $ w R | =w = d 2 d 1 w ( l + w lW ) = w d = w U | =w = d 2
(2.120a) (2.120b)
We can obtain an interesting picture of the deformation process by referring the Lagrangian tensors to the Lagrangian coordinate system (principal directions of w U) and the Eulerian tensors to the Eulerian coordinate system (principal directions of w V). Hence (Hill 1978):
2.13 Strain rates
55
• In the Lagrangian system the components of w U are w u (we assume them ˙ are w ˙ uv and the components of to be di erent); the components of w U w w O O are uv . • In the Eulerian system the components of w V are of course also w u ; the components of w d are w guv ; the components of w $ are w $ uv ; the components H U of w H are w uv and the components of w U are w uv . From Eq. (2.117b) we have w
H U
uv w uv =
w O uv
>
(2.121a)
w u + w v guv = w ˙ uv 2w u w v
(2.121b)
from Eq. (2.118b) we get w
and from Eq. (2.118c) we get w
w u w v U $ uv w uv = w ˙ uv ; 2w u w v
(2.121c)
(in Eqs. (2.121b) and (2.121c) we do not use the summation convention). In the fixed Cartesian system the components of w U form the matrix [w X ]; hence, [w X ] = [w UO ] [w ] [w UO ]W > (2.122a) where,
5w
6 1 0 0 [w ] = 7 0 w 2 0 8 = 0 0 w 3
(2.122b)
Taking the time derivative of Eq. (2.122a), we obtain ˙ [w UO ]W + [w O ] [w UO ] [w ] [w UO ]W [w X˙ ] = [w UO ] [w ] [w UO ] [w ] [w UO ]W [w O ]
(2.122c)
hence, ˙ + [w UO ]W [w O ] [w UO ] [w ] [w UO ]W [w X˙ ] [w UO ] = [w ] [w ] [w UO ]W [w O ][w UO ] =
(2.122d)
The above equation shows that: w˙
uv = w ˙ u w ˙ uv = ( w v w u )w O uv
(u = v) = (u 6= v)
(2.123)
From Eq. (2.121b) for the case u = v (diagonal components), we get w
guu =
w˙
u w u
=
d (ln w u ) = dw
(2.124)
56
Nonlinear continua
JJJJJ
Example 2.16.
Using Eqs. (2.65), (2.35), (2.111b) and (2.112b) we can show that: w ˙ %
=
1w ˙ C = w XW · w d · 2
w X
= JJJJJ
Example 2.17. JJJJJ The Hencky strain tensor components in the fixed Cartesian system are, [w K] = [w UO ] ln [w ] [w UO ]W > hence, ˙ = [w UO ] [w ]1 [w ] ˙ [w UO ]W + [w O ] [w UO ] ln [w ] [w UO ]W [w K] = w [ UO ] ln [w ] [w UO ]W [w O ] JJJJJ
2.14 The Lie derivative In the deformation process represented in Fig. 2.2 we can define, for a Eulerian tensor w t, its Lie derivative associated to the flow of the spatial configuration (Simo 1988, Marsden & Hughes 1983): ¾ ½ d £w w ¤ ! ( t) = (2.125) Lw v (w t) = w ! dw
As we already know (see Sect. 2.9) the operation of pull-back is not a tensor operation since it operates on components. Hence, for calculating a Lie derivative using Eq. (2.125) it is important to identify the components of w t that we are using. The Lie derivative of a scalar is Lw v =
d C C = + w d wyd = dw Cw C {
(2.126)
The covariant components of the Lie derivative of a spatial vector w w are ¾ ½ ¢ ¡ d w m w w w 1 D (2.127a) Lw v w l = ( [ ) l [( [) D zm ] > dw
after some algebra,
2.14 The Lie derivative
Since,
¡ ¢ C w zl C wyd C w zl Lw v w w l = + w d w y d + w l w zd = Cw C { C { w
57
(2.127b)
zl w zl = w
(2.128a)
we can write ¡ ¢l ¡ ¢ Lw v w w w zl + w zl Lw v w w l =
µ
dw l z dw
¶
w
zl + w zl
µ
dw zl dw
¶
(2.128b)
and from the above we get the contravariant components of the Lie derivative of a spatial vector w w, ¡ ¢l C w zl C wyl C w zl Lw v w w = + w d w y d w zd w d = Cw C { C {
(2.128c)
Following the above procedure we can show that the mixed components of the Lie derivative of a general Eulerian tensor w t are ¢d===e ¡ Lw v (w t)
f===g
=
C w wd===e Cw
f===g
+
C w wd===e f===g w s y C w {s
(2.129)
C w yd w s===e w C w {s
f===g
···
C w ye w d===s w C w {s
f===g
+
C w ys w d===e w C w {f
s===g
+ ··· +
C w ys w d===e w C w {g
f===s
JJJJJ
Example 2.18.
To calculate the Lie derivative of the spatial metric tensor w g we can directly use Eq. (2.125) ¸ ³ ´ d hw w i Lw v w g = w ! ! ( g) > dw lm LM using now Eq. (2.93a), we get ³ ´ Lw v w g
=
lm
h
w
˙ ! (w C)
i
lm
Using the result in Example 2.16, we get ³ ´ ¡ ¢ Lw v w g = 2 w d lm =
=
lm
JJJJJ
58
Nonlinear continua
JJJJJ
Example 2.19.
To calculate the Lie derivative of the Almansi deformation tensor we use Eq. (2.125) and get ¸ ¡ ¢ d £w w ¤ w w w L v e lm = ! ! ( e) LM dw and resorting to Eq.(2.94a), ¢ £ ¤ ¡ ˙ lm = Lw v w e lm = w ! (w %)
Taking into account the result obtained in Example 2.16 we can finally write ¡ ¡ ¢ ¢ Lw v w e lm = w d lm = JJJJJ
JJJJJ
Example 2.20. The Lie derivative of the Finger deformation tensor is ¸ ¡ ¢lm d £w w ¤LM w w Lw v b = ! ! ( b) = dw
Using Eq. (2.97b) we get
and since
£w
! (w b)
¤LM
=
we get
h
w
B`
iLM
=
LM
j
g˙ = 0
¢lm ¡ = 0= Lw v w b
JJJJJ
2.14.1 Objective rates and Lie derivatives In this Section we will show that the Lie derivative is the adequate mathematical tool for deriving covariant (objective) rates from covariant (objective) Eulerian tensors. Let us consider the deformation processes schematized in Fig. 2.7. It is obvious that
2.14 The Lie derivative
59
Fig. 2.7. Deformation processes between three configurations wˆ X
ˆ
= ww X ·
w X
=
(2.130a)
For a covariant Eulerian tensor w t, that without losing generality we take as a second-order tensor: ~ˆ wˆ ˆ
w
ˆ
ˆ
= ww [ ˆ~d ww [ ˆe w wde >
¯ ¯ ¯wˆ wˆ ˆ~ˆ¯DE ˆ ˆ ˆ ˆ = (w [ 1 )Dˆ~ (w [ 1 )Eˆ ww [ ˆ~d ww [ ˆe w wde = ¯ ! w ¯
(2.130b) (2.130c)
Using Eq. (2.130a) in the above, we get
¯ ¯ ¯wˆ wˆ ˆ~ˆ¯DE = (w [ 1 )Do (w [ 1 )En w won > ¯ ! w ¯
¯ ¯ ¯DE ¯ ¯wˆ wˆ ˆ~ˆ¯DE = ¯w ! w won ¯ = ¯ ! w ¯
(2.130d) (2.130e)
From the above and from Eq. (2.125) it follows that: ½ iop iop ¾dˆˆe h h w w ˆ ˆ ˆ ˆ ˆ ˆ Lw vˆ (w t)dˆe = ww [ dˆo ww [ ep Lw v ( t) = ww ! Lw v ( t) = (2.130f) The above equality shows that the Lie derivative of a covariant Eulerian tensor is also a covariant Eulerian tensor.
60
Nonlinear continua
Example 2.21. JJJJJ Considering again the case of a moving Cartesian frame and a fixed one from Example 2.15, we get = f˙ + T˙ (w } ) + T (w y ) >
w
y
˙ for the case under therefore taking into account that c > Q(w) and Q(w), consideration, are constant in space, w o
hence, w o
C (w } ) C (w } ) = T˙ + T (w o ) w C } C w} = T˙ (TW ) + T (w o ) (TW ) =
Comparing with Eq. (2.101c) it is obvious that w l is not an objective tensor. Since the velocity gradient tensor is not objective in the classical sense we know that it is not a covariant tensor. JJJJJ JJJJJ Example 2.22. From Example 2.19, we know that w d is the result of a Lie derivative; hence we can assess that the Eulerian strain rate tensor is a covariant (objective) tensor. JJJJJ JJJJJ Example 2.23. For a Eulerian tensor w t, we define in the reference configuration the tensor: w
T` =
[
which can be written as w
Since,
w 1 X
·
w X
=
¡w
T` =
¢ 1 D d
¡w
[
w 1 X
¢ 1 E w de w gD gE e
· wt ·
we can write d ³ w
dw
w 1 X
d ³w W ´ X = w lW · dw T`
´
=
=
g we can derive that,
d ¡w 1 ¢ X = dw
and
w W X
w 1 X
· w t˙ ·
w W X
w X1 · w t ·w lW ·
· wl
w W X
w 1 X
w W X
=
· w l ·w t ·
w W X
2.15 Compatibility
61
Also, from Eqs. (2.110c) w W
l
= u w v = w ys |q w gq w gs
=
Considering that the time derivative of the reference configuration base vectors is zero and using the above together with the Lie derivative definition in Eq. (2.125), we get £ ¤de Ow v (w t) = w w˙de w wqe w yd |q w wdo w ye |o =
The above equation is going to be used in Sect. 3.4 for deriving objective stress rates. JJJJJ
2.15 Compatibility In our previous description of the kinematics of continuous media we went through the following path: Assume the existence of a regular mapping w ! . Calculate the tensorial components of di erent deformation measures If, instead of the above, we want to start by defining the tensorial components of a given deformation measure, our freedom to define them is limited by the fact that they should guarantee the existence of a regular mapping from which they could be derived. The conditions that the tensorial components of a deformation measure should fulfill in order to assure the existence of a regular mapping are called their compatibility conditions. In what follows we will derive the compatibility conditions for the Green deformation tensor. From Eqs. (2.61), (2.80c) and (2.93a) we have, Eulerian tensor
Spatial configuration w
Length di erential Coordinate di erential
w
Metric tensor
w
Pull-back space w
do
d{d jde
do
[(w d{d )` ]D = [(w jde )^ ]DE =
d{D
w FDE
Hence, w
d{d w jde w d{e =
d{D w FDE d{E =
(2.131)
From the above equation it is obvious that the covariant components of the Green deformation tensor are the covariant components of the metric tensor
62
Nonlinear continua
of the pull-back space. Note that the pull-back space is by no means coincident with the reference configuration, whose metric tensor has the covariant components jDE . Since we restrict our study of the kinematics of continuous media to the Euclidean space, we can assess that the Riemann-Christo el tensor is zero in the spatial configuration (McConnell 1957). Hence, w
Usuvt = 0 =
(2.132)
The above equation represents 81 compatibility conditions to be fulfilled in the spatial configuration. However, the covariant components of the RiemannChristo el tensor satisfy the following relations (Aris 1962)7 : w
Usuvt = w Uusvt >
(2.133a)
w
Usuvt = w Usutv >
(2.133b)
w
Usuvt = w Uvtsu =
(2.133c)
We must also consider that w Ullll = 0 ; w Ulllm = 0 ; w Ullmm = 0 can be easily transformed into a trivial identity of the form 0 = 0. Hence we are left with only 6 significant equations, namely: w
U1212 = 0
;
w
U1213 = 0
;
w
U1223 = 0 ;
w
U1313 = 0
;
w
U1323 = 0
;
w
U2323 = 0 =
(2.134)
From Eqs. (A.79a-A.79e), ¶ µ 2w 1 C 2 w juv C 2 w jsv C 2 w jut C jst w Usuvt = + w s w t w u w t w s w v 2 C w {u C w {v C { C { C { C { C { C { ¡ ¢ + w j pq w uvp w stq w utp w svq (2.135a)
where the w lmn are the Christo el symbols of the first kind corresponding to the coordinate system {w {d }. Hence, using Eq. (A.79b) ¶ µ 2w 1 C 2 w juv C 2 w jsv C 2 w jut C jst w Usuvt = + w u w t w s w v 2 C w {u C w {v C w {s C w {t C { C { C{ C { (2.135b) µ w ¶ µ ¶ 1 C jvp C w jpu C w jtq C w juv C w jqs C w jst w pq + w v w p + w t w q + j 4 C w {u C { C { C w {s C { C{ ¶ µ ¶¸ µ w w w w w w C jvq C jqs 1 C jtp C jpu C jut C jsv + w t w p + w v w q =0= 4 C w {u C { C { C w {s C{ C { 7
See Appendix.
2.15 Compatibility
Doing a pull-back operation on Eq. (2.132) we obtain, ¢¤ £w ¡w ! Usuvt S UVT = w [ sS w [ uU w [ vV w [ tT w Usuvt = 0 =
63
(2.136a)
JJJJJ Example 2.24. Equation (2.135b) represents the components of the tensorial equation w
R = 0 =
If in the spatial configuration we change from the {w {l } coordinate system to the {w { ˜l } system, we write Eq. (2.135b) using, w
j˜st = w jop
w st
j˜
= w j op
C w {o C w {p Cw{ ˜s C w { ˜t Cw{ ˜s C w { ˜t C w {o C w {p
and the equation would look like ¶ ¶¸ µ w µ 2w 1 1 C j˜vp C j˜st w˜ w pq + · · · + j˜ + ··· = 0 = Usuvt = 2 Cw{ ˜u C w { ˜v 4 Cw{ ˜u If we now want to do a pull-back of Eq.(2.135b) the algebra can get quite lengthy, but we can use an analogy with the above tensor transformations: £w
£w
! (w jop )S T
¤
= w jop
¤S T ! (w j op ) = w j op
C w {o C {S C {S C w {o
C w {p = w FS T C {T ¡ ¢ C {T = w F 1 S T C w {p
=
Using this formal analogy we can easily write:
2w ¤ 1 C 2 w FUV C 2 w FS V C FS T ! (w Usuvt ) S UVT = + U V S T 2 C{ C{ C{ C{ C {U C {T ¸ ¡ ¢PQ C 2 w FUT S V + w F 1 C { C { ¶µ w ¶ µ C w FPU C w FUV C w FQS C w FS T 1 C w FVP C FTQ + P + Q 4 C {U C {V C { C {S C {T C { ¶ µ ¶¸ µ w w w w w C FPU C FUT C FQ S C w FS V 1 C FTP C FVQ + P + Q 4 C {U C {T C { C {S C {V C { £w
JJJJJ
64
Nonlinear continua
Hence, ¸ 2w ¡w 1 ¢PQ C 2 w FUV C 2 w FS V C 2 w FUT C FS T 1 + + F U V S T U T S V 2 C{ C{ C{ C{ C{ C{ C{ C{ (2.136b) ¶ µ ¶ µ w C w FPU C w FUV C w FQS C w FS T C w FTQ 1 C FVP + P + Q 4 C {U C {V C { C {S C {T C { ¶µ w ¶¸ µ w w w w w C FVQ C FPU C FUT C FQ S C FS V 1 C FTP + P + Q = 0= 4 C {U C {T C { C {S C {V C { We can now define in the pull-back space, with metric w FDE , the Christoffel symbols of the first kind: ¶ µ w 1 C w FPU C w FUV C FVP (2.136c) UVP = + 2 C {U C {V C {P therefore we obtain the following 6 compatibility conditions for the covariant components of the Green deformation tensor:
! (w Usuvt ) = +
¡w
F
1 2
¢ 1 PQ
µ
C 2 w FUV C 2 w FS V C 2 w FUT C 2 w FS T + U V S T U T C{ C{ C{ C{ C{ C{ C {S C {V ( UVP S TQ
UTP S VQ ) = 0 =
(2.136d)
The above equation indicates that w FDE is a metric of the Euclidean space. Taking into account the Bianchi identities in Eq. (A.82d) (Synge & Schild 1949) and Eqs.(2.135a), we get w
U1212|3 + w U1213|1 + w U1213|2 = 0 >
w
U1313|2 + w U1323|1 w U1213|3 = 0 >
w
w
(2.137)
w
U2323|1 U1323|2 + U1223|3 = 0 >
and we reduce the number of independent compatibility conditions to 3. JJJJJ Example 2.25. Using as a metric the Green tensor, we can define an analog to Eq.(A.59): w ^ ¸ C DL w ^ G L D D g g GRADw C (w A^ ) = G LD C {D where for the Eulerian vector w a, ³ ´ w ^ D
L
=
w l [ L
dl >
¶
2.15 Compatibility
and,
G LD =
1 ¡w 1 ¢GN F 2
Cw FDN Cw FLD Cw FLN + C {D C {L C {N
¸
65
=
Taking into account that
w FLN
¡w
F
it is easy to show that:
¢ 1 GN
C w {u C {L C {G = C w {u =
C w {v w juv > C {N C {N w uv j > C w {v
h ³ ´i £ ¡ w ¢ ¤ ! u a ld LD = GRADw C w A^
LD
= JJJJJ
Example 2.26. JJJJJ In a Cartesian coordinate system, from Eqs. (2.9a-2.9b), (2.29a-2.29c), (2.65) and (2.68) we get ¶ µ 1 C w x C w x C w x C w x w + + > % = 2 C } C } C } C } ¶ µ w w w 1 C C C x x x C w x w h = + w w w = 2 C w } C } C } C } For linear kinematics,
C w x ?? 1 > C }
and also
C(=) C(=) = = w C } C} Therefore, for linear kinematics ¶ µ C w x 1 C w x w = w % > % + = 2 C } C} where we call w % the components of the infinitesimal strain tensor. From Eq. (2.65) we know that: w %
=
¢ 1 ¡w F = 2
Introducing the above in Eq. (2.135b) and linearizing (neglecting the higher powers of w % ) we get the compatibility equations corresponding to the assumption of linear kinematics:
66
Nonlinear continua
C 2 w % C 2 w % C 2 w % C 2 w % + = 0= C } C } C } C } C } C } C } C } The above represents a set of 6 equations, that proceeding as in Eqs. (2.137), can be reduced to 3 independent compatibility conditions. The above result was obtained for a Cartesian system. Generalizing for an arbitrary coordinate system we get w
%DE|FG + w %FG|DE w %DG|EF w %EF|DG = 0 = JJJJJ
3 Stress Tensor
To deform a continuous body the exterior medium has to produce a loading on that body; therefore we get external forces acting on it. Also, during the deformation of a continuous body, neighboring particles exert forces on each other, they are the internal forces in the body. The study of the internal forces in a body leads to the notion of stresses, that we are going to develop in this chapter. Some reference books for this chapter are: (Truesdell & Noll 1965, Truesdell 1966, Malvern 1969, Marsden & Hughes 1983).
3.1 External forces When studying the deformation of a continuous body, to classify a force as either external or internal, we have to carefully take into account our definition of the body under consideration. For example, in Fig. 3.1 d, we study the spatial configuration at w of the body (w D ^ w E ) with the external forces w FD and w FE and in Fig. 3.1 e, to study the same physical problem, we choose to consider w D and w E as free bodies. Obviously both analyses will lead to the same conclusions but, it is clear that in the first case w FDE and w FED have to be considered as internal forces and in the second case as external forces. We can find di erent types of external forces, for example: • External forces acting on the elements of volume or mass inside the body (they are defined per unit volume or per unit mass). Theses forces are called body forces and some examples are: gravitational forces, inertia forces, electromagnetic forces, etc. (in general they are “action-at-a-distance” forces (Malvern 1969). Let us define in the w-configuration of a body a Cartesian system {w }ˆ > = 1> 2> 3} with base vectors wˆ e and an arbitrary curvilinear system {w {l > l = 1> 2> 3} with covariant base vectors w gl . We consider the vector
68
Nonlinear continua
Fig. 3.1. External and internal forces in a bar
field w b(w x) to define the forces per unit mass acting on the body at w . We can write w b = wˆe wˆ e = w el w gl = (3.1) The resultant of the forces per unit mass is: Z Z Z w w w w wˆ w b dY = e ˆ e w dY = wY
wY
wY
w
w el w gl w dY
(3.2)
where, w : density of the body in w-configuration and w Y : volume of the body in the w-configuration. • External forces acting on the elements of the body’s surface (they are defined per unit surface). These forces are called surface forces and some examples are: pressure forces, contact forces, friction forces, etc. We consider the vector field w t(w x) to define the forces per unit surface acting on the region w V , a subset of the surface of the body at w . We can write
3.2 The Cauchy stress tensor w
t = w wˆ wˆ e = w wl w gl =
The resultant of the forces per unit surface is: Z Z Z w w w ˆ w w ˆ t dV = e w dV = wV
wV
(3.3)
w l w
w
wV
69
gl w dV =
(3.4)
It is important to point out that our description of the external forces acting on a body excludes the possibility of considering distributed torques per unit volume, mass or surface. Therefore, the moment with respect to a point S of the considered external forces in the w-configuration is: Z Z ¡w ¢ w ¡w ¢ w w w MS = r × b dY + r × w t w dV (3.5) wY
wV
w
where r is the vector that in the w-configuration goes from the moment center S to a point inside the body (first term on the r.h.s.) or to a point on the body surface (second term on the r.h.s.).
3.2 The Cauchy stress tensor In Fig. 3.2 d we represent the spatial configuration of a body B corresponding to a time w, and we identify a particle S .
Fig. 3.2. Internal forces at a point inside a continuum
w
The external forces acting on B per unit mass are given by the vector field b and the external forces per unit surface are given by the vector field w t .
70
Nonlinear continua
We now section the body B, in the w-configuration, with a surface w Vf passing through S . The normal to the surface w Vf at S is w n (see Fig. 3.2 e). If we now analyze in Fig. 3.2 e the left part, w O , as a free body, we have to consider as external forces the internal forces at S in Fig. 3.2 d. Considering on the surface w Vf an area w V around S , the set of external forces acting on w V can be reduced to a force w F through S and a moment w MS . When w V $ 0: w
lim
w
lim
w V$0
F
= wt
(3.6a)
MS = 0 w V
(3.6b)
w V$0
w V
The vector w t is known in the literature as traction. Equations(3.6a-3.6b) incorporate two fundamental hypotheses: • The limit in Eq. (3.6a) exists. Therefore we exclude from the continuum mechanics field the consideration of concentrated forces (concentrated forces are also not physically possible). • The condition in Eq. (3.6b) is a strong requirement in the classical formulation of continuum mechanics. There are alternative formulations that do not require the fulfillment of Eq. (3.6b) (e.g. the theory of polar media (Truesdell & Noll 1965, Malvern 1969). In this book we limit our study to the classical case of non-polar media. It is interesting to note that from Eq. (3.6a) we can assess that, if we consider di erent surfaces through S , which share the external normal w n (tangent surfaces), we will arrive at the same traction vector w t (see Fig. 3.3). We can define, in the w-configuration at the point S> a second-order tensor w , the Cauchy stress tensor, via the following equation: w
t = wn · w =
(3.7)
Since w t and w n are vectors, using the quotient rule (Sect. A.5), it is evident that w is a second-order tensor. We can consider Eq. (3.7) to be a condition of equivalence between external forces and stresses inside a continuum.
3.2 The Cauchy stress tensor
71
Fig. 3.3. Tangent surfaces at P have the same traction vector
3.2.1 Symmetry of the Cauchy stress tensor (Cauchy Theorem) In Sect. 4.4.2 we will prove that from the equilibrium equations of a nonpolar continuum we get w
= w W >
(3.8)
that is to say, the Cauchy stress tensor is symmetric. JJJJJ Example 3.1. In the following figure, at the point S , inside the w-configuration of a continuum body, the stress tensor is w . Cutting the continuum with the surface w V1 , we get at S the traction vector w
if we cut with
w
t1 = w n1 · w >
V2 , the traction vector at S is: w
t2 = w n2 · w =
72
Nonlinear continua
Secant surfaces at a point inside a continuum In an arbitrary coordinate system {w {l } we can write w w
and since from Eq. (3.8)
t1 · w n2 = w q1l w lm w q2m > t2 · w n1 = w q2l w lm w q1m > w lm
w
= w ml we get
t1 · w n2 = w t2 · w n1 =
The above result, a direct consequence of the Cauchy Theorem, is known as the projection theorem or reciprocal theorem of Cauchy (Malvern 1969).JJJJJ
3.3 Conjugate stress/strain rate measures Let us assume, at an instant (load level) w, a continuum body B in equilibrium under the action of external body forces w b and external surface forces w t. Assuming a velocity field w v(w x) on B, the power provided by the external forces is: Z Z w w w w Sh{w = b · w v w dY + t · w v w dV = (3.9a) wY
wV
Using Eq. (3.7) we can rewrite Eq.(3.9a) as
3.3 Conjugate stress/strain rate measures w
Sh{w =
Z
w
wY
w b · w v w dY
Z
+
¡w
wV
n · w
¢
· w v w dV =
From the Divergence Theorem (Hildebrand 1976), Z ¡ £w w ¢ ¤w w Sh{w = b · wv + u · w · wv dY
73
(3.9b)
(3.9c)
wY
introducing Eq. (2.110a-2.110c) and after some algebra, Z ¡w w £w ¢ ¤ w Sh{w = : wl + b + u · w · w v w dY =
(3.9d)
wY
Since the w-configuration is an equilibrium configuration, the following equation (to be proved in Chap. 4, Eq.(4.27b)) holds Gw v > Gw
(3.9e)
and an obvious result that we also need is: ¸ G 1 w Gw v w w v · v = · v = Gw Gw 2
(3.9f)
w
wb + u · w = w
The kinetic energy of the body B, at the instant w, is defined as Z Z w w 1 w w w w N = v · v dY = v · w v dp = 2 wY p 2
(3.9g)
In the second integral of the above equation we integrate over the mass of the body B. Since the mass of the body is invariant, Z Gw v Gw N (3.9h) = · w v dp = Gw Gw p Finally, using the decomposition of the velocity gradient tensor in Eq. (2.112a) and considering that since (w ) is a symmetric tensor and (w $) is a skew-symmetric one, w : w$ = 0 (3.9i) we get w
Sh{w =
Gw N Gw
We define w
S =
Z
+
w
: w d w dY =
(3.9j)
wY
Z
w
: w d w dY
(3.10)
wY
as the stresses power . Obviously w S is the fraction of w Sh{w that is not transformed into kinetic energy and that is either stored in the body material or dissipated by the body material, depending on its properties (see Chapter 5). From Eq. (3.10) we define the spatial tensors w and w d to be energy conjugate (Atluri 1984). In what follows we will define other pairs of energy conjugate stress/strain rate measures.
74
Nonlinear continua
3.3.1 The Kirchho stress tensor From Eqs. (3.10) and (2.34d) and the mass-conservation principle (to be discussed in Chapter 4, Eq.(4.20d)) we get Z Z w w w S = : w d w dY = : w d dY = (3.11) w wY Y The Kirchho stress tensor is defined as w
=
w
w
(3.12)
where, : density in the reference configuration and Y : volume of the reference configuration. It is important to note that although the Kirchho stress tensor was introduced by calculating w S via an integral defined over the reference volume, Eq. (3.12) clearly shows that w is defined in the same space where w is defined: the spatial configuration. Hence, using in the w-configuration an arbitrary curvilinear coordinate system {w {d } with covariant base vectors w gd we obtain w w
= w de w gd w ge
(3.13a)
= w de w gd w ge
(3.13b)
and w de
=
w
w de
=
(3.13c)
3.3.2 The first Piola-Kirchho stress tensor From Eqs. (3.11) and (3.9i) we can write Z w w S = : w l dY =
(3.14)
Y
In Chap. 2 we learned how to derive representations in the reference configuration of tensors defined in the spatial configuration via pull-back operations. We will now obtain a representation of the Kirchho stress tensor in the form of a two-point tensor . In the reference configuration we define an arbitrary coordinate system { {D } with covariant base vectors gD ; and in the spatial configuration a system {w {d } with covariant base vectors w gd . We also define a convected el system {l } with covariant base vectors in the reference configuration g el . and covariant base vectors in the spatial configuration w g In the spatial configuration we can write the Kirchho stress tensor as
3.3 Conjugate stress/strain rate measures w
= w ˜lm
w
el w g em g
75
(3.15a)
a pull-back of the above tensor to the reference configuration is: w
T` = w ˜lm
h
el g em = g
w
T`
iLM
gL gM =
(3.15b)
We define a two-point representation of w as = w ˜lm
w P
After some algebra, w Lm S
w op
= ˜
= w sm
£w ¤Lm P
el w g em = g
C {L C w {m p = Co C ¡w 1 ¢L = [ s
"
w st
gL w gm =
Co Cp C w {s C w {t
#
(3.15c)
C {L C w {m p Co C (3.15d)
The second-order two-point tensor w P is the first Piola-Kirchho stress tensor. It is apparent from Eq. (3.15d) that it is a non-symmetric tensor. We can write, due to the symmetry of the Kirchho stress tensor: Z Z w de w w ed w S = ode dY = ode dY = (3.16a) Y
Y
Hence, using Eq.(3.15d): S =
Z
Y
w Ed w e w S [ E ode dY
Using Eq. (2.111a) we have Z Z w Ed w ˙ S = S dY = [ dE Y
Y
w P
· ·
=
(3.16b)
w ˙ X dY
We can also write the above as (Malvern 1969): Z w W ˙ dY = S = : w X P
=
(3.17)
(3.18)
Y
W
˙ as energy The above equation defines the two-point tensors w P and w X conjugates. We will not try to force a so-called “physical interpretation” of the first Piola-Kirchho stress tensor; instead we will regard it only as a useful mathematical tool.
76
Nonlinear continua
3.3.3 The second Piola-Kirchho stress tensor The pull-back configuration of w to the reference configuration is: w
T` =
h
w lm
¡w
[
¢ 1 L l
¡w
[
¢ 1 M m
i
gL gM =
(3.19)
The tensor w T` , defined by the above equation, is the second PiolaKirchho stress tensor and it is a symmetric tensor. Using Bathe’s notation (Bathe 1996), we identify the second Piola-Kirchho stress tensor, corresponding to the w-configuration and referred to the configuration in w = 0 as w S. JJJJJ
Example 3.2. From Eqs. (3.15d) and (3.19) we get w LM V
that is to say, w LM V
¡w
¢ 1 M w Lm S m
£w
¡w
[
=
=
!
S
Lm
¢¤LM
= JJJJJ
From Example 2.16: w ˙ DE %
=
w DE V
=
and since from Eq. (3.19),
using Eqs. (3.11) and (2.88), we get Z w S =
£w
Y
!
£w
!
w S
¡w
gde
¡w :
¢¤
de
(3.20a)
DE
¢¤DE
w ˙ dY %
(3.20b)
=
(3.20c)
From Eq. (3.20c) we define the tensors w S and w %˙ to be energy conjugate (Atluri 1984). Here, we will also not try to force a “physical interpretation” of the second Piola-Kirchho stress tensor. An important point to be analyzed is the transformation of w S under rigidbody rotations. • Let us first consider the w-configuration of a certain body B. At an arbitrary point S the Cauchy stress tensor is w .
3.3 Conjugate stress/strain rate measures
77
• Let us now assume that we evolve from the w-configuration to a (w + w)configuration imposing on B and on its external loads a rigid body rotation. At the point S we can write: w+w X w
w+w R w
>
(3.21a)
w+w R w
· w dx =
(3.21b)
t =
w+w R w
· wt >
(3.22a)
w+w
b =
w+w R w
· wb =
(3.22b)
w+w
v =
w+w R w
· wv =
(3.22c)
w+w R w
· wn =
(3.22d)
=
and therefore, w+w
dx =
For the external loads,
w+w
For a velocity vector,
For the external normal vector, w+w
n =
Example 3.3. JJJJJ For an arbitrary force vector w f (it can be a force per unit surface, per unit volume, etc.) and considering the evolution described above, w+w
f ·
w+w
v = = =
w+w R · wf w w f · w+w RW w w f · w+w RW w
· w+w v · ·
w+w
v
w+w R w
· wv
and since the rotation tensor is orthogonal, w+w
f ·
w+w
v = wf · wv =
The above equation states the intuitive notion that a rigid-body rotation cannot a ect the value of the deformation power performed by the external forces. JJJJJ
78
Nonlinear continua
At w we can write
w
and at (w + w),
w+w
t = wn · w
t =
w+w
n ·
(3.23a)
w+w
Introducing Eq. (3.22d) in the above, ¡ ¢ w+w t = w+w R · wn · w
=
(3.23b)
w+w
=
(3.23c)
And with Eq. (2.28a) and (3.22a), we finally have h i w t = w n · w+w RW · w+w · w+w R = w w For deriving the above equation, we used that
w+w R w
(3.23d)
· wt = wt ·
w+w W R w
=
Hence, w+w
w+w R w
=
w+w W R w
· w ·
=
(3.23e)
The above equation indicates that the Cauchy stress tensor fulfills the criterion for objectivity under isometric transformations, established for Eulerian tensors in Sect. 2.12.2. 0 We define an arbitrary system {w {d } in the w-configuration and a system w+w d { { } in the (w + w)-configuration. Hence, from Eq. (3.23e), w+w d e
¡w+w
w+w d w f0 U f0 g0 w
=
w
and using Eq. (2.28c), we get w+w d e
=
w+w d U f0 w
w f0 g0
therefore, w+w do
0
w+w o U p0 w
0
w+w
w+w d U f0 w
= w f p
UW
¢g0
joe
(3.24a)
e
w p0 g0
j
w+w o U p0 w
(3.24b)
=
(3.24c)
It is easy to show that for the Kirchho stress tensor we can also write w+w
=
w+w R w
· w ·
w+w W R w
=
(3.25)
From Eq. (3.19), we obtain w+w LM V
=
w+w lm
but since, w+w d [D ¡w+w 1 ¢D [ d
= =
¡w+w
[ 1
¢L ¡w+w l
[ 1
0 w+w d w U d0 [ dD w ¡w 1 ¢D ¡w+w W ¢d0 U d [ w d0
using Eqs. (3.24c) and (3.26c) in Eq. (3.26a), we get
¢M
m
(3.26a)
(3.26b) (3.26c)
3.3 Conjugate stress/strain rate measures w+w LM V
=
w LM V
79
(3.27a)
therefore, w+w S
=
w S
=
(3.27b)
The above equation indicates that the second Piola-Kirchho stress tensor fulfills the criterion for objectivity under isometric transformations, established for Lagrangian tensors in Sect. 2.12.2. 3.3.4 A stress tensor energy conjugate to the time derivative of the Hencky strain tensor In Sect. 2.8.5 we defined the logarithmic or Hencky strain tensor. Let us now define, via a pull-back operation, the following stress tensor: w
=
w U
(w ) =
(3.28)
With the notation w U (·) we define the pull-back of the components of the tensor (·) using the tensor w R (Simo & Marsden 1984), that is to say, w is an unrotated representation of w . From the symmetry of w , the above definition implies the symmetry of w = We will now demonstrate, following (Atluri 1984), that for an isotropic ˙ are energy conjugate. material w and w H We can write Eq. (3.14) as Z £ ¡ ¢¤ w w DE w w S = gde DE dY (3.29a) U Y
therefore,
w
S =
From Eq. (2.28c),
Z
w Y
w d U D
DE w UdD w gde w UeE dY =
=
¡w
U
(3.29b)
¢ W O w do j jDO o
(3.29c)
and using the above, the integrand in Eq. (3.29b) is: w
DE
¡w
U
¢ W O w do j jDO w gde w UeE o
=
(3.29d)
It is also easy to show that h¡ i ¢ w w e w W w w w W O w do D E R · d · R = U j j g U g g = DO de E o Hence, using Eq. (2.118b), Z ³ 1 w w ˙ · S = : w U 2 Y
w 1 U
+
w 1 U
·
´
w ˙ U
dY =
(3.29e)
(3.29f)
80
Nonlinear continua
In order to simplify the algebra, in what follows we will work in a Cartesian system; [D] will be the matrix formed with the Cartesian components of a second-order tensor A. From Eqs. (2.122a-2.122d), we get ˙ [w ]1 [w UO ]W + [w O ] [w X˙ ] [w X ]1 = [w UO ] [w ]
[w UO ] [w ] [w UO ]W
(3.30a)
[w O ] [w UO ] [w ]1 [w UO ]W
and ˙ [w UO ]W [w X ]1 [w X˙ ] = [w UO ] [w ]1 [w ]
(3.30b)
+ [w UO ] [w ]1 [w UO ]W [w O ] [w UO ] [w ] [w UO ]W [w O ] it follows from the above two equations that o 1 n w ˙ w 1 ˙ [w UO ]W + [w X ]1 [w X˙ ] = [w UO ] [w ]1 [w ] [ X ] [ X ] 2 1 + [w UO ] [w ]1 [w UO ]W [w O ] [w UO ] [w ] [w UO ]W 2 1 w [ UO ] [w ] [w UO ]W [w O ] [w UO ] [w ]1 [w UO ]W > 2 and using once again Eqs. (2.122a-2.122d), we get o 1 n w ˙ w 1 ˙ [w UO ]W + [w X ]1 [w X˙ ] = [w UO ] [w ]1 [w ] [ X ] [ X ] 2 1 w 1 + [w X ]1 [w O ] [w X ] [ X ] [w O ] [w X ]1 = 2 2
(3.30c)
(3.30d)
Using the result in Example 2.17, we can write o 1 n w ˙ w 1 ˙ [w O ] [oqw X ] + [w X ]1 [w X˙ ] = [w K] (3.30e) [ X ] [ X ] 2 1 1 w + [oqw X ] [w O ] + [w X ]1 [w O ] [w X ] [ X ] [w O ] [w X ]1 = 2 2 Using the above in Eq. (3.29f) and working with the matrix components, Z n w ˙ [w O ] [oqw X ] S = [w ] [w K] (3.31a) Y
1 w 1 [ X ] [w O ] [w X ] 2 ¾ [w X 1 ] dY =
+ [oqw X ] [w O ] +
1 w [ X ] [w O ] 2
Since [w ] and [w X ] are symmetric and [w O ] is skew-symmetric, we can rewrite the above equation as
3.4 Objective stress rates w
Z
S =
1 + 2
w
˙ dY [w ] [w K]
Y
Z
n £ ¤ £ ¤ o w [w ] [w K] [w K] [w ] [ O ]
Y
Z
Y
81
dY
n £ ¤ £ ¤ o w [w X ]1 [w ] [w X ] [w X ] [w ] [w X ]1 [ O ] dY =
(3.31b)
We will show in Chap. 5 that for isotropic materials the Eulerian tensors (w ) and w V have coincident eigenvectors (they are coaxial). Taking into account that w U
=
w w U ( V)
(3.32)
and the definition of w in Eq. (3.28) we conclude that the Lagrangian tensors w , w U and w H are also coaxial for isotropic materials. Obviously, the coaxiality of w and w H implies that [w ] [w K] [w K] [w ] = [0] w
and the coaxiality of
and
w U
(3.33a)
implies that
[w X ]1 [w ] [w X ] [w X ] [w ] [w X ]1 = [0] =
(3.33b)
Finally, for isotropic materials, w
S Lvrw=P dw=
=
Z
Y
w
:
w ˙ H dY
(3.34)
˙ are energy conjugates. and therefore in this case w and w H
3.4 Objective stress rates In Sect. 2.14.1 we show that the adequate tool for deriving objective rates of Eulerian tensors is the Lie derivative. The Lie derivative of the Cauchy stress tensor is: ³
w
´de
=
£
Ow v (w )
¤de
= w ˙ de w fe w odf w df w oef
(3.35)
the above stress rate is known as Oldroyd stress rate (Marsden & Hughes 1983).
82
Nonlinear continua
Example 3.4. JJJJJ To derive the expression of Oldroyd’s stress rate we start from Eq. (2.129), ¡ ¢de ¢S C w de C w yd ¡ C w de Ow v w = + w s w ys S w [ 1 s w se Cw C{ C { C w ye ¡w 1 ¢S w ds S [ = s C {
From Eq. (2.109a)
w ˙ X
=
C w yd + C {D
¸
s w d w o w w gd gD [ D so y
>
and Eq. (2.111b) w ˙ X
= wl ·
w X
>
we get, C wyd d w v w = w odp w [ pD w uv y [ uD = C {D Then, from w
= w de w gd w ge >
we get, w
˙ =
C w de C w de w o d w o e w o y + w pe w po y + w dp w po y + Cw C w {o
¸
w
gd w ge =
Replacing in the first equation, after some algebra, we finally get ¡
Ow v w
¢de
= w ˙ de w ods w se w oes w ds = JJJJJ
• The Lie derivative of the Kirchho stress tensor is: h ide £ ¤de w = Ow v (w ) = w ˙ de w fe w odf w df w oef
(3.36)
the above rate is known as the Truesdell stress rate (Marsden & Hughes 1983). JJJJJ
Example 3.5. From Eq. (3.19), w lm
hence,
=
w LM w l V [ L
m w [ M
>
3.4 Objective stress rates
C w lm C w lm + w s w ys = Cw C {
but
h
w
w ˙ LM V
w l [ L
m w [M
+
+ w V LM
w l [ L
C w ym C {M
ilm ! (w V˙ LM ) =
w ˙ LM V
w l [ L
C w yl C {L
w LM V
m w [M
83
m w [ M
=
Therefore, h
w
ilm C w lm C w lm + w s wys ! (w V˙ LM ) = Cw C {
C wyl w m [ C {L M C w ym (w [ 1 )Lo (w [ 1 )Mp M w [ lL = C {
w op (w [ 1 )Lo (w [ 1 )Mp
w op
Using algebra along the lines of Example 3.4 and Eq.(3.36) we finally get, h ilm lm w = w ! (w V˙ LM ) =
JJJJJ
The above example shows that the necessary and su!cient condition for the second Piola-Kirchho stress tensor to remain constant is that the Truesdell stress rate is zero (Eringen 1967). We can also perform pull-back and push-forward operations using the rotation tensor w R (Simo & Marsden 1984). Let us consider an arbitrary Eulerian stress tensor w t ( e.g. w or w ), and perform on its components a w U-pullback: £w w ¤DE = w wde (w UW )Dd (w UW )Ee = (3.37a) U ( t) In order to simplify our calculations we will now work in a Cartesian system; hence, £w w ¤ = [w U]W [w w] [w U] = (3.37b) U ( t) ª © ª © W d d Taking into account that dw [U] > we get [U]W = dw
d £w w ¤ ˙ W [w w] [w U] + [w U]W [w w] [w U] ˙ (3.37c) ˙ [w U] + [w U] U ( t) = [w U]W [w w] dw
and using Eqs. (2.115a) and (2.116a) we get
d £w w ¤ ˙ [w U] [w U]W [w U ] [w w] [w U] U ( t) = [w U]W [w w] dw + [w U]W [w w] [w U ] [w U] =
(3.37d)
84
Nonlinear continua
Since,
i h d £w w ¤ w W U ( t) [ U] Ow R (w t) = [w U] dw
we finally arrive at i h ˙ [w U ] [w w] + [w w] [w U ] Ow R (w t) = [w w]
(3.37e)
(3.37f)
that in an arbitrary spatial coordinate system leads to
ide h = w w˙de w U df w wfe + w wdf w U ef = Ow R (w t)
(3.38)
$ = w U =
(3.39)
The above Lie derivative is the well-known Green-Naghdi stress rate (Dienes 1979, Marsden & Hughes 1983, Pinsky, Ortiz & Pister 1983, Simo & Pister 1984, Cheng & Tsui 1990). From its derivation it is apparent that the Green-Naghdi stress rate is objective under isometric transformations, therefore it is known as a corotational stress rate. In the case of the Kirchho stress tensor, its Green-Naghdi rate is the w U-push-forward of the rate of w . If as a reference configuration we use the w-configuration (Dienes 1979), we will fulfill Eq. (2.118d), that is to say, t
Using the above in Eq. (3.38) we obtain the Jaumann stress rate (Truesdell & Noll 1965). It is important to realize that (Dienes 1979): • The Jaumann stress rate is only coincident with the corotational stress rate when w U g. • When formulating a corotational constitutive relation, we will only be able to use the Jaumann stress rate when the spatial and reference configurations are coincident.
4 Balance principles
In this chapter we are going to present a set of basic equations (balance of mass, momentum, angular momentum and energy) that govern the behavior of the continuous media in the framework of Newtonian mechanics. We are going to present these basic principles in an integral form and also in the form of partial di erential equations (localized form). On presenting the basic principles we are going to use both, the Eulerian (spatial) and Lagrangian (material) descriptions of motion. Some reference books for this chapter are: (Truesdell & Toupin 1960, Fung 1965, Eringen 1967, Malvern 1969, Slaterry 1972, Oden & Reddy 1976, Marsden & Hughes 1983, Panton 1984, Lubliner 1985, Fung & Tong 2001).
4.1 Reynolds’ transport theorem We begin this chapter by presenting Reynolds’ transport theorem; which will be used in what follows as a tool for calculating material derivatives of integrals defined in a spatial domain. Let us define in the spatial configuration of a continuum body B an arbitrary coordinate system {w {l > l = 1> 2> 3} and let us assume a continuous Eulerian tensor field t #(w {l > w) to be a single-valued function of the coordinates {w {l } and of time w. Also, we define in the reference configuration an arbitrary coordinate system { {L > L = 1> 2> 3}. We define w Y as a volume in the spatial configuration and Z G w # (w {l > w) w dY (4.1) Gw w Y to be the material time derivative of a spatial volume integral ; that is to say, Eq. (4.1) measures the rate of change of the total amount of the tensorial property t # carried by the particles that at time w are inside the volume w Y . Using Eq.(2.31) we can write,
86
Nonlinear continua
G Gw
Z
w wY
d # ( { > w) dY = dw w l
w
Z
w
# ( {L > w) w M dY
(4.2a)
Y
hence, Z Z Z dw M dw # ( {L > w) w G w w # (w {l > w) w dY = M dY + # ( {L > w) dY = Gw w Y dw dw Y Y (4.2b) JJJJJ Example 4.1. Working in Cartesian coordinates we can write, from Eq. (2.34e) (Fung 1965): w
M = h w [1 w [2 w [3 =
Using Eqs.(2.111a-2.111b) we can calculate the time rate of w M: w
M˙ = h [w o w [1 w [2 w [3 + w [1 w o w [2 w [3 + w [1 w [2 w o w [3 ] =
After some algebra, the reader can easily verify that, w
M˙ = w o h w [1 w [2 w [3 =
Generalizing the above for any set of curvilinear coordinates in the Euclidean space we can write, w ˙ M = (u · w v) w M
where w v is the velocity vector at the w-configuration. A proof of the above result in general curvilinear coordinates can be found in (Marsden & Hughes 1983). JJJJJ Using the result of Example 4.1 in Eq. (4.2b) we obtain, Z G t # (w {l > w) w dY = (4.3a) Gw w Y " # Z dw # ( {L > w) w L w + # ( { > w) (u · v) w M dY = dw Y Returning to the w-configuration we obtain, Z G t # (w {l > w) w dY = (4.3b) Gw w Y ¸ w Z G # (w {l > w) + w # (w {l > w) (u · w v) w dY = Gw wY
4.1 Reynolds’ transport theorem
87
Equation (4.3b) is one way of expressing Reynolds’ transport theorem. In this Section, we will also discuss other expressions for this theorem. Using Eq. (2.20b) we can rewrite Eq. (4.3b) as, Z Z C t # (w {l > w) G w l w t # ( { > w) dY = [ (4.3c) Gw w Y Cw wY + w v · ut # (w {l > w) + t # (w {l > w)(u · w v)] w dY = JJJJJ
Example 4.2. Let us assume a general tensor field: w
# = w # d===ef===g w gd ===w ge w gf ===w gg
where the w gl are the covariant base vectors of the coordinate system {w {l }. The velocity vector field can be written as, w
v = w y v w gv
therefore we can write, using Eq.(A.59), ¡ ¢ w v · ut # = w y v w gv · w # d===ef===g |q = w y v w # d===ef===g |v
w
w q w
g
gd ===w ge w gf ===w gg
gd ===w ge w gf ===w gg =
Also, using Eq.(A.64), t
#(u · w v) = w # d===ef===g w y v |v w gd ===w ge w gf ===w gg
=
Finally, using Eq. (A.62b), u · (w v w #) = =
³
w v w
³
y
w v w
y
´ # d===ef===g |v
# d===ef===g
gd ===w ge w gf ===w gg ´ |v + w # d===ef===g w y v |v w gd ===w ge w gf ===w gg = w
From the above equations we get, w
v · (u t #) + t # (u · w v) = u · (w v w #) = JJJJJ
Using the above result we can express Reynolds’ transport theorem as,
88
G Gw
Nonlinear continua
Z
w
w l
w
# ( { > w) dY =
wY
Z
wY
C t # (w {l > w) + u · (w v w #(w {l > w)) Cw
The generalized Gauss’ theorem can be stated as (Malvern 1969): Z Z w u · t # w dY = n · t # w gV wY
¸
w
dY =
(4.4)
(4.5)
wV
where w V is the closed surface that bounds the volume w Y and w n is the surface’s outer normal vector. Using Gauss’ theorem in Eq. (4.4) and rearranging terms, we get the following expression of Reynolds’ transport theorem: Z Z Z G C t# w w t t dY = # dY n · w v t # w dV = (4.6) Cw Gw w Y wY wV Following (Malvern 1969) we can state: ; Rate of increase A A A A of the total amount A A ? t of # inside w a volum e Y A A A A in the spatial A A = configuration
; A A A A A A ?
< A A A A A A @ A A A A A A >
=
A A A A A A =
Rate of increase of the total am ount t # p ossessed of by the material instantaneously inside the volume
w
Y
< A A A A A A @ A A A A A A >
; A A A A ?
A A A A =
Net rate of outward t flux of # carried by the material
< A A A A @ A
transp ort through A A A w > the closed surface V
The volume w Y is usually called the control volume and the surface w V is usually called the control surface. 4.1.1 Generalized Reynolds’ transport theorem In the previous section, for deriving Reynolds’ transport theorem we considered a material volume w Y bounded by a material surface w V. In this section, we are going to generalize the previous derivation considering in the spatial wconfiguration an arbitrary volume (w) bounded by a surface (w) that moves with an arbitrary velocity field w w. We can define inside the w-configuration of the body B a surface, w
i (w {l > w) = 0 =
(4.7)
If the surface moves with the particles instantaneously on it, we say that it is a material surface. The Lagrange criterion states (Truesdell & Toupin 1960) that the necessary and su!cient condition for the above-defined surface to be material is that its material time derivative is zero; using Eq.(2.20b), w
C wi C wi w n y = 0= i˙ = + Cw C w {n
(4.8)
4.1 Reynolds’ transport theorem
Fig. 4.1. Body B with the surface w i
¡w
89
¢ {l > w = 0
To prove the Lagrange criterion, let us consider the following general case, In Fig. 4.1, at a point S on w i = 0 we define: - The unit vector w n normal to the surface. - The material velocity w v of the particle instantaneously at S . - The velocity w w of the surface. The condition that the point S (not the particle instantaneously at S ) remains on w i = 0 when the surface moves is given by, C wi w n C wi z = 0= + Cw C w {n From geometrical considerations, w
and we can write,
n = q w
(4.9a)
C wi w n g C w {n
(4.9b)
C wi C w i w op j C w {o C w {p
w = w z s w gs =
(4.9c)
Hence, w
w
w
w
zq = w · n = q
zn
C wi C w {n
C wi C w i w op j C w {o C w {p
(4.9d)
and using in the above Eq.(4.9a), we get w
zq = q
C wi Cw C wi C w i w op j C w {o C w {p
=
(4.9e)
90
Nonlinear continua
We can also define, using the material velocity of the particle instantaneously at S , w w n C i y C w {n w w w yq = v · n = q = (4.9f) C wi C w i w op j w p w o C { C {
Using Eqs. (4.9e), (4.9f) and the first equality in Eq.(4.8), we obtain r C w i C w i w op w w ˙ j ( yq w zq ) = (4.9g) i = C w {o C w {p
If the particle instantaneously at S remains on the surface during the motion, from obvious geometrical considerations w
yq = w zq >
(4.9h)
and using the above in Eq.(4.9g), we have for a material surface w
i˙ = 0 >
(4.10)
which demonstrates the Lagrange criterion. Equation (4.9h) indicates that if we consider in the spatial configuration at time w fictitious particles (Truesdell & Toupin 1960) moving with a velocity field w w, the volume (w) and the surface (w) can be considered material and we can write, using Eq.(4.6) for any Eulerian tensor field w #, Z Z Z Gw w C w# w w w w # dY = dY + n · w w w # w dV = (4.11) Gw (w) Cw
(w) (w) With Gw w (·)@Gw we indicate that when taking the material time derivative, the velocity field w w is considered. Equation (4.11) is the expression of the generalized Reynolds’ transport theorem. An application of this theorem is presented in Example 4.5. 4.1.2 The transport theorem and discontinuity surfaces In Fig. 4.2 we represent a body B in its spatial configuration corresponding to time w. We assume that the Eulerian tensor field w # has a jump discontinuity across a surface w V12 inside the body and we let the material velocity field w v to be also discontinuous across w V12 (Truesdell & Toupin 1960). At any point on the discontinuity surface we define its normal (w n12 ) and its displacement velocity (w w), not necessarily coincident with the material velocity of the particle instantaneously at that point (w v). Considering the region on the negative side of w n12 , we can define fictitious particles with the following velocity field: •
w
v on w V
4.1 Reynolds’ transport theorem
91
Fig. 4.2. Discontinuity surface
•
w
w on w V12
and using the generalized Reynolds’ transport theorem we obtain, Z Z Z Gw w C w# w w w # w dY = dY + n · w v w # w dV Gw w Y Cw wY wV Z w + n12 · w w w # w dV = (4.12a) wV 12
Using the generalized Gauss’ theorem (Eq.(4.5)), Z Z w u · (w v w #) w dY = n · w v w # w dV wY
wV
+
Z
wV 12
w
n12 · w v w # w dV
(4.12b)
hence, Gw w Gw
Z
w wY
w
# dY =
Z
wY
Z
wV 12
Cw# + u · (w v w #) Cw w
¸
w
dY
(4.12c)
# w n12 · (w v w w) w dV =
For the region on the positive side of w n12 , in the same way, we get ¸ w Z Z Gw w C # w w w w # dY = (4.12d) + u · ( v #) w dY Gw w Y + Cw wY + Z w + w + # n12 · (w v+ w w) w dV = wV 12
92
Nonlinear continua
The velocity field of the fictitious particles is coincident with the velocity field of the actual particles everywhere except on w V12 . Therefore: Z Z Z Gw w Gw w G w w w # w dY = # w dY + # w dY = (4.12e) Gw w Y Gw w Y Gw w Y + From Eqs.(4.12c) to (4.12e) we get, ¸ w Z Z C # G w w w w # dY = + u · ( v #) w dY Gw w Y Cw wY Z + [[ w # (w yq w zq )]] w dV
(4.13)
wV 12
where, [[w # (w yq w zq )]] = w # + (w yq+ w zq ) w # (w yq w zq ) > w yq = w n12 · w v > w zq = w n12 · w w =
In order to obtain a localized version of Reynolds’ transport theorem at the discontinuity surface we consider the arbitrary material volume enclosed by the dashed line in Fig. 4.3.
Fig. 4.3. Derivation of the jump discontinuity condition w = w + w 3
For the enclosed material volume, using Eq.(4.13) and the generalized Gauss’ theorem, we write: Z Z Z G Cw# w w w w # dY = dY + n · w v w # w dV (4.14) Gw w Y Cw wY wV Z Z w n · w v w # w dV + [[ w # (w yq w zq )]] w dV> + wV+
wV 12
4.2 Mass-conservation principle
93
+
when w dV $w V12 and w dV $w V12 ; w + $ 0 and w $ 0 we get from Eq.(4.14): Z ¢ ¡w w (4.15) [[ # yq ]] + [[w # (w yq w zq )]] w dV = 0 = wV 12
Therefore, in order for the above integral equation to be valid for any arbitrary part of the discontinuity surface, we must fulfill [[w # w yq ]] + [[w # (w yq w zq )]] = 0
(4.16a)
w
at every point on V12 . Equation (4.16a) is known as the jump discontinuity condition. If we call w U = w zq w yq the discontinuity’s propagation speed, we can write [[w # w U]] = [[w # w yq ]] = (4.16b)
The above equation is known as Kotchine’s theorem (Truesdell & Toupin 1960).
4.2 Mass-conservation principle In Sect. 2.2, Eq.(2.6) introduced the concept of mass of a continuum body B. In the study of continuum media, under the assumptions of Newtonian mechanics, it is postulated that the mass of a continuum is conserved. Hence, Z G w w dY = 0 (4.17) Gw w Y where w = w (w {l > w). 4.2.1 Eulerian (spatial) formulation of the mass-conservation principle Using in Eq.(4.17) the expression of Reynolds’ transport theorem given in Eq.(4.4) we obtain: w ¸ Z Z G C w w dY = (4.18) + u · (w w v) w dY = 0 = Gw w Y Cw wY Since the above equation has to be fulfilled for any control volume inside the continuum, we can write for any point inside the spatial configuration: Cw (4.19) + u · (w w v) = 0 = Cw The above partial di erential equation is the localized spatial form of the mass-conservation principle in a Eulerian formulation and it is called the continuity equation.
94
Nonlinear continua
Example 4.3. JJJJJ Using components in a general curvilinear spatial coordinate system, the continuity equation is written as Cw Cw + w y d w d + w w yd |d = 0 = Cw C { JJJJJ Example 4.4. For an incompressible material
G w Gw
JJJJJ = 0; hence the continuity equation is:
u · wv = 0 > or in components, w d
y |d = 0 =
JJJJJ JJJJJ
Example 4.5.
Let a fluid of density w = w (w {l > w) have a velocity field w v. Let us consider in the spatial configuration a volume (w) bounded by a surface (w) that moves with an arbitrary velocity field w w. Following (Thorpe 1962), we first calculate the fluid mass instantaneously inside the volume (w): Z w
P =
w dY
(w)
and using the expression of the generalized Reynolds’ transport theorem in Eq.(4.11), we get Z Z Z Gw w dP Cw w w w w dY = dY + n · w w w w dV = dw Gw (w)
(w) Cw (w) where w n is the external normal of the surface (w). Using Eq.(4=5) (generalized Gauss’ theorem), we get Z Z ¡ ¢ w u · w w v w dY = n · (w w v) w dV
(w)
(w)
and subtracting the above equation from the previous one, ¸ w Z dP C = + u · (w w v) w dY dw Cw
(w) Z w w + n · (w w w v) w dV = (w)
4.3 Balance of momentum principle (Equilibrium)
95
Using Eq.(4.19), we see that the first integral on the r.h.s. is zero; hence, Z dP w w n · (w w w v) w dV = = dw (w) The above equation is an integral equation of continuity for a control volume JJJJJ in motion in the fluid velocity field (Thorpe 1962).
4.2.2 Lagrangian (material) formulation of the mass conservation principle Equation (4.17) implies that, Z Z D ( { ) dY = Y
w
(w {d > w) w dY
(4.20a)
wY
where ( > Y ) correspond to the reference configuration and (w > w Y ) to the spatial configuration. Using Eq.(2.31) in the r.h.s. of Eq.(4.20a) and changing variables in the expression of w we obtain, Z Z D w ( { ) dY = ( {D > w) w M dY > (4.20b) Y
hence,
Y
Z
( w w M) dY = 0 =
(4.20c)
Y
Since the above equation has to be fulfilled for any control volume that we define inside the continuum, we can write for any point inside the reference configuration: = w wM > (4.20d) and therefore, G w w (4.20e) ( M) = 0 = Gw The above equation is the localized material form of the continuity equation.
4.3 Balance of momentum principle (Equilibrium) The principle of balance of momentum is the expression of Newton’s Second Law for continuum bodies. Quoting (Malvern 1969): “The momentum principle for a collection of particles states that the time rate of change of the total momentum of a given set of particles equals the vector sum of all the external forces acting on the particles of the set, provided Newton’s Third Law of action and reaction governs the internal forces. The continuum form of this principle is a basic postulate of continuum mechanics”.
96
Nonlinear continua
4.3.1 Eulerian (spatial) formulation of the balance of momentum principle For a body B in the w-configuration we define its momentum as, Z w w w v dY
(4.21a)
wY
the resultant of the external forces acting on the elements of mass inside the body are, from Eq.(3.2): Z w w w b dY > (4.21b) wY
and the resultant of the external forces acting on the elements of the body’s surface are, from Eq.(3.4): Z w
t w dV =
(4.21c)
wV
Using Eqs.(4.21a-4.21c), we can state Newton’s Second Law for the body B as, Z Z Z G w w w w w w w w v dY = b dY + t dV = (4.22) Gw w Y wY wV Using the condition of equivalence between external forces and Cauchy stresses inside a continuum, defined in Eq.(3.7), we get: Z Z Z G w w w w w w w v dY = b dY + n · w w dV = (4.23) Gw w Y wY wV Using in the above the expression of Reynolds’ transport theorem given in Eq.(4.4), we get ¸ w w Z Z C( v) w w w w dY = b dY + u · (w w v w v) Cw wY wY Z w + n · w w dV = (4.24) wV
From Example 4.2, we obtain u · (w w v w v) = w v · also, from Eq.(2.20b), we get
£ ¤ u (w w v) + w w v (u · w v)
£ ¤ G (w w v) C (w w v) = + w v · u (w w v) > Gw Cw
and, from Eq.(4.5) (Generalized Gauss’ Theorem), we get
(4.25a)
(4.25b)
4.3 Balance of momentum principle (Equilibrium)
Z
w wV
n · w w dV =
Z
wY
u · (w ) w dY
=
97
(4.25c)
Using Eqs.(4.25a-4.25c) in Eq.(4.24) we arrive at the integral form of the Eulerian formulation of the balance of momentum principle: ¸ Z Z £w w ¤ G w w b + u · w w dY = ( v) + w w v (u · w v) w dY = Gw wY wY (4.26) Since the above equation has to be fulfilled for any control volume that we define inside the continuum, we can write for any point inside the spatial configuration: G w w ( v) + w w v (u · w v) = w w b + u · w Gw
(4.27a)
and using in the above the continuity equation, we have w
G wv = w wb + u · w = Gw
(4.27b)
The above equation is the localized form of the balance of momentum principle in an Eulerian formulation and it is known as the equilibrium equation. Example 4.6. JJJJJ Using Eq.(A.62b), in the general Eulerian curvilinear system {w {d }, we get, u · w = w de |d w ge hence, using Eq.(A.55b), w de ¸ C w w ve w d w dv w e u · = + vd + vd w ge = C w {d From the result in Example A.10, we can easily get ¸ 1 w pm C w jlm C w jmo C w jol w p lo = j + = 2 C w {o C w {l C w {m Therefore, u · w =
¢ C w de 1 ¡w ve w dm + j + w dv w j em w d C { 2 ¶¸ µ w C jvm C w jmd C w jdv w + ge = C w {d C w {v C w {m
JJJJJ
98
Nonlinear continua
Example 4.7. JJJJJ A perfect fluid is defined as a continuum in which, at every point, and for any surface, w n · w = w wn >
where w is a scalar (no shear stresses). Since w is a symmetric second order tensor (to be shown in Sect. 4.4), its eigenvalues are real and its eigenvectors are orthogonal (Appendix, A.4.1). Referring the problem to the Cartesian system defined by the normalized eigenvectors, wˆ e we can write, n = wq ˆ wˆ e 3 X w w = ˆ wˆ e wˆ e = w
=1
Then, for the perfect fluid, w
q ˆ w ˆ = w w q ˆ
( = 1> 2> 3)(qr dgglwlrq rq ) =
The above set of equations is fulfilled only if the three eigenvalues equal (hydrostatic stress tensor ). Hence, w
w
ˆ are
= w s wˆ e wˆ e =
It is easy to show that as the three eigenvalues of w are equal, the above equation is valid in any Cartesian system; hence we can write, w
lm = w s lm >
where w s is the pressure. Generalizing the above to any arbitrary coordinate system w = ws wg = Using Eq. (A.62b) and the result in Example A.11, the equilibrium equation, Eq. (4.27b), can be written as, w
Gw v Cs w lm w j gm = = w wb + Gw C w {l
From Eq. (A.57) we identify the last term on the r.h.s. of the above equation as uw s, hence we can write the equilibrium equation for a perfect fluid as, w
G wv = w w b + uw s = Gw
The above equation is known as the Euler equation for perfect fluids. Many authors get a minus sign for the second term on the r.h.s. because they define w
lm = w s lm = JJJJJ
4.3 Balance of momentum principle (Equilibrium)
99
Example 4.8. JJJJJ Following with the topic discussed in Example 4.5 we consider a fluid, moving with a velocity field w v, and a moving control volume, moving with a velocity field w w. In this example, following (Thorpe 1962), we are going to analyze the momentum balance inside the moving control volume. Using the generalized Reynolds’ transport theorem (Eq.(4.11)) for the fluid momentum, Z Z Gw w C(w w v) w w w w v dY = dY Gw (w) Cw
(w) Z w w + v (w n · w w) w dV = (w)
From the generalized Gauss’ theorem (Eq.(4.5)), Z Z w w w w w u · ( v v) dY = n · (w w v w v) w dV =
(w)
(w)
Subtracting the above equation from the previous one, ¸ w w Z Z Gw w C( v) w w w w w w v dY = + u · ( v v) w dY Gw (w) Cw
(w) Z ¤ £ w w + v w n · (w w w v) w dV = (w)
Using the result in Example 4.2 and Eq.(4.19) (continuity equation), µ w ¶ Z Z Gw w C v w w w w v dY = + w v · u w v w dY Gw (w) Cw
(w) Z ¤ £ w w + v w n · (w w w v) w dV = (w)
On the r.h.s. of the above equation, the term between the brackets in the first integral is the fluid particles material acceleration. We can state, using Newton’s second law, that the external force instantaneously acting on the particles inside (w) is, Z w w w w F = a dY =
(w)
Hence, w
F =
Gw Gw
Z
w
(w)
w v w dY +
Z
w w
v
(w)
£w
n ·
¡w
v w w
¢¤
w
dV = JJJJJ
100
Nonlinear continua
Example 4.9. JJJJJ Let us consider the body B and the particle S on its external surface. We el define at S a convected coordinate system l with covariant base vectors w g el in the material configuration. The conin the spatial configuration and g e1 and w g e2 in the plane tangent to w V vected system is defined so as to have w g w e e at S ; and therefore g1 and g2 define the plane tangent to V at S .
Material and spatial normal vectors (Nanson’s formula) The external unit normals at S are w
n =
and,
n =
we
e2 g1 × w g > e1 × w g e2 | |w g e
g1 × e1 × | g
Also, the surface-area di erentials are w
If we define,
e
g2
g e
2
e1 × w g e2 ) d1 d2 dV w n = (w g
e1 × dV n = ( g w w
1
e2 ) d d g
|
2
e1 > t1 = d1 w g e2 > t2 = d2 w g
e1 > t1 = d1 g e2 > t2 = d2 g
=
(D) > (E) =
4.3 Balance of momentum principle (Equilibrium)
101
it is obvious from the results in Sect. 2.9.1 that
t1 = w T`1
t2 = w T`2 =
We can now define an arbitrary curvilinear system {w {l } in the spatial configuration and another one { {L } in the material configuration, with covariant base vectors w gl and gL respectively. w
t1 = (w w1 )n w gn
w
t2 = (w w2 )n w gn
w
T`1 = (w w1 )n (w [ 1 )Nn gN
w
T`2 = (w w2 )n (w [ 1 )Nn gN w
n = w ql w gl
n =
qL gL
where, C w {l = C {L We write Eqs.(D) and (E) using the above as, w l [ L
=
w
dV w ql = w lmn (w w1 )m (w w2 )n dV qL = LMN (w w1 )m (w w2 )n (w [ 1 )Mm (w [ 1 )Nn = Multiplying both sides of the above equation by (w [ 1 )Ll , we get
dV qL (w [ 1 )Ll =
LMN (w [ 1 )Ll (w [ 1 )Mm (w [ 1 )Nn (w w1 )m (w w2 )n
but, from Eqs.(A.37e) and (2.34g)
LMN = hLMN
Hence, using Eq.(A.37c), we get
dV qL (w [ 1 )Ll =
p | jDE | =
p | jDE | |w [ 1 | hlmn (w w1 )m (w w2 )n
and again using Eq.(A.37e), we get
dV qL (w [ 1 )Ll =
Therefore,
w p lmn (w w1 )m (w w2 )n = | jDE | |w [ 1 | p |w jde |
102
Nonlinear continua
dV qL (w [ 1 )Ll = w dV w ql |w [ 1 |
s
| jDE | |w jde |
and using Eq.(2.34i), we get w
w 1 dV X
n w dV = w M n ·
=
The above equation is called Nanson’s formula (Bathe 1996).
JJJJJ
Example 4.10. For an Eulerian vector w a we define, using Eq.(2.76a),
JJJJJ
w
h¡
¢ w 1 E w e d [ e
A` =
i
gE =
Using the generalized Gauss’ theorem (Eq.(4.5)), Z Z w u · w a w dY = n · w a w dV = wY
wV
In the r.h.s. integral we introduce Nanson’s formula derived in Example 4.9; hence, Z Z w u · w a w dY = M n · w X1 · w a dV wY
V
= =
Z
Z
w
V
V
M n · ³
w
n ·
h¡
¢ w 1 E w e d [ e
M w A`
´
i
gE dV
dV =
Using again the generalized Gauss’ theorem, Z Z ³ ´ w w u · a dY = GLY w M w A` dY = wY
Y
With the notation GLY (·) we indicate a divergence in the reference configuration. Using in the r.h.s. integral Eq.(2.31), we get Z Z ³ ´ ¡ ¢ w w M u · a dY = GLY w M w A` dY = Y
Y
The localized form of the above equation is known as the Piola Identity (Marsden & Hughes 1983), ´ ³ ¡ ¢ w M u · w a = GLY w M w A` =
JJJJJ
4.3 Balance of momentum principle (Equilibrium)
103
Example 4.11. JJJJJ We can write the Piola Identity, derived in the above example, as: w
£w
M w de |e =
¤ M (w [ 1 )Ef w df |E =
After some algebra, we get £ ¤ w w e M d |e = w M (w [ 1 )Ef |E Hence,
£w
that is to say
w f
d + w M w df |f
=
¤ M (w [ 1 )Ef |E = 0
GLY
¡w
M w X1
¢
= 0= JJJJJ
4.3.2 Lagrangian (material) formulation of the balance of momentum principle In the previous section we derived, in the spatial configuration, the integral and localized forms of the balance of momentum principle (equilibrium equations). In this section we are going to derive, in the material configuration, the integral and localized forms of the equilibrium equations. We are going to refer Eq.(4.23) to volumes and surfaces defined in the material configuration, using Eq.(4.20d) and Nanson’s formula (Example 4.9). Z Z Z G w w v dY = b dY + n · w X1 · w dV = w Gw Y Y V (4.28a) In the above equation, all magnitudes are written as functions of ( {L > w). Using the generalized Gauss’ theorem together with the definition of the first Piola-Kirchho stress tensor, we obtain Z Z Z G w w b dY + GLY (w P) dY = (4.28b) ( v) dY = Gw Y Y Y In the above (Malvern 1969), GLY (w P) = =
w Dd |D w gd S w Dd C S D + w S Gd GD D
C {
+
w Dg w l w d S [D lg
¸
w
gd =
Equation (4.28b) is an integral form of the equilibrium equations. It is important to note that although the integrals are calculated on volumes defined
104
Nonlinear continua
in the reference configuration, the equilibrium is established in the spatial configuration. The corresponding localized form is,
Gw v = Gw
w b + GLY (w P) =
JJJJJ
Example 4.12. From Eqs.(4.27b) and (4.29) we get,
(4.29)
u · w = GLY (w P) =
w
The above equation is a particular application of the Piola Identity. JJJJJ In order to write the equilibrium equations in terms of fully material tensors we have to pull-back Eq.(4.29). For the material velocity field: £ ¤D w ` V = w ! (w yd ) gD = (4.30) A “physical interpretation” of the pull-back of the material velocity contravariant components was presented in Example 2.12. In the same way, for the material acceleration, w
a =
Gw v = w dd w gd Gw
(4.31)
and h
w
A`
iD
=
£w
! (w dd )
¤D
= wd ˜D
(4.32)
the w d ˜D are the components of the material acceleration vector in the convected system { {D } (convected acceleration (Simo & Marsden 1984)). For the external loads per unit mass, we define £ ¤D w ` B = w ! (w ed ) gD = (4.33) Since GLY (w P) is an Eulerian vector, £w
!
¡w
S
Ld
|L
¢¤D
= (w [ 1 )Dd w S Ld |L =
(4.34)
Therefore, the pull-back of Eq.(4.29) is
w A` =
w B` +
w 1 X
· GLY (w P) =
(4.35)
In a Lagrangian formulation, the above equation is the localized form of the equilibrium equations.
4.4 Balance of moment of momentum principle (Equilibrium)
105
4.4 Balance of moment of momentum principle (Equilibrium) Quoting (Malvern 1969) again: “In a collection of particles whose interactions are equal, opposite, and collinear forces, the time rate of change of the total moment of momentum for a given collection of particles is equal to the vector sum of the moments of the external forces acting on the system. In the absence of distributed couples, we postulate the same principle for a continuum”. The condition of no distributed couples (nonpolar media) was introduced in Sect. 3.2. 4.4.1 Eulerian (spatial) formulation of the balance of moment of momentum principle For a body B in the w-configuration we define its moment of momentum with respect to a given point R as, Z w w r × w v w dY > (4.36a) wY
where w
r = w x w x ;
and w x ; w x are the position vectors of an arbitrary point S and of the point R, respectively. The resultant moment with respect to R of the external forces acting on the elements of mass inside the body is, Z w w r × w b w dY > (4.36b) wY
and the resultant moment with respect to R of the external forces acting on the elements of the body’s surface is, Z w r × w t w dV = (4.36c) wV
Using Eqs.(4.36a-4.36c) we can state the balance of moment of momentum principle for the continuum body B: Z Z Z G w w w w w r × w v w dY = r × w b w dY + r × w t w dV = (4.37a) Gw w Y wY wV With the condition of equivalence between external forces and Cauchy stresses inside a continuum defined in Eq.(3.7), we get
106
Nonlinear continua
Z
G Gw
w
wY
w
w
w
r × v dY =
Z
w wY
w
w
w
r × b dY +
Z
w
wV
r × (w n · w ) w dV = (4.37b)
JJJJJ
Example 4.13. The last integral on the r.h.s. of Eq.(4.37b) can be written as, Z
w
wV
r ×
¡w
n · w
¢
w
dV = =
Z
Z
wV
wY
¡w
n · w ¡w
u ·
¢
× w r w dV
× wr
¢
w
dY
where we used Eq. (4.5) (Generalized Gauss’ Theorem). For any second-order tensor, w d , and for any vector, w c , we can write w
d × w c = w gst w fu w gs w gt × w gu =
w st w u w
g
f
tur w gs w gr
= w gst w fu w utr w gs w gr =
Also, w
c × w dW = w fo
and
³
w
Hence,
¡w
gW
c × w dW w
Therefore, Z
wV
w
r ×
¢pq
¡w
w
´W
go × w gp w gq = w fo w gqp w opr w gr w gq
= w fo w gqp w opr
d × wc =
n · w
¢
w
³
dV =
w
Z
c × w dW
´W
u ·
¡w
wY
Using the above result, Z G w w r × w v w dY Gw w Y Z Z w w w w r × b dY + = wY
w
gq
w r
g =
=
r × w W
¢W
w
dY = JJJJJ
(4.38a)
wY
u ·
¡w
r × w W
¢W
w
dY =
4.4 Balance of moment of momentum principle (Equilibrium)
107
Using in the above equation the expression of Reynolds’ transport theorem given in Eq.(4.4), we get ¸ Z C w w ( r × w v) + u · (w w v w r × w v) w dY Cw wY Z Z ¡ ¢W w w w = r × w b w dY + u · w r × w W dY = (4.38b) wY
wY
With the result in Example 4.2, we get £ ¤ u · (w w v w r × w v) = w v · u (w w r × w v) + (w w r × w v) (u · w v) (4.39)
using Eqs. (4.39) and (2.20b) we can write Eq.(4.38b) as,
Z
wY
¸ ¡w ¢ ¡ ¢ w G (w w r × w v) w w w dY u · v + r × v Gw Z Z ¡ ¢W w w = r × w b w dY + u · w r × w W wY
w
dY
wY
and therefore, ½ ¸ ¾ Z ¡ ¡w ¢ Gw ¢ ¢ w ¡w w w w w G w r × v r × v dY + + u · v Gw Gw w ZY Z ¡ ¢W w w w = r × w b w dY + u · w r × w W dY = (4.40a) wY
wY
Equation (4.19), the Eulerian continuity equation, can be written as, ¡ ¢ Gw + w u · wv = 0 Gw
(4.40b)
hence, introducing the above into Eq.(4.40a), we obtain Z
wY
w
w r × w a w dY =
Z
wY
w
w r × w b w dY +
Z
wY
u ·
¡w
r × w W
¢W
w
dY =
(4.40c) For the Eulerian formulation, the above is the integral expression of the balance of moment of momentum principle. From it, we obtain the localized form: w
wr × wa = w wr × wb + u ·
¡w
r × w W
¢W
=
(4.41)
4.4.2 Symmetry of Eulerian and Lagrangian stress measures From the Eulerian localized form of the balance of moment of momentum principle, we will first derive the symmetry of the Cauchy stress tensor.
108
Nonlinear continua
Using an intermediate result that we got in Example 4.13, we can write the localized form of the balance of moment of momentum as, w
r × w
¡ ¢ G wv wr × w wb = u · w × wr = Gw
(4.42)
JJJJJ Example 4.14. The divergence of the cross product between a second order tensor, w , and a vector, w r , is u ·
¡w
× wr
¢
=
C
w q
·
g
C w {q
£w
¡ ¢ = u · w × wr +
× wr w q
g
·
¤ h
h
w
× w gq
i
i gd w ge × w gq h i ¡ ¢ r = w r × u · w + w gq · w de w gd w eqr w g ¡ ¢ r = w r × u · w + w eqr w qe w g =
=
w
r ×
¡ u ·
w
¢
+ w gq ·
w de
w
JJJJJ
Using the above result in Eq.(4.42), we get ¸ Gw v w r × w w w b u · w = w eqr w qe w gr = Gw
(4.43a)
Using the Eulerian localized equilibrium equation (Eq.(4.27b)), w
eqr w qe w gr = 0 =
Introducing in the above Eq. (A.37e), we can write ¯ w l¯ ¯C } ¯ w w qe ¯ ¯ = 0 (r = 1> 2> 3) ¯ C w {m ¯ heqr
(4.43b)
(4.43c)
hence,
(r = 1)
w 23
w 32 = 0 >
(r = 2)
w 31
w 13 = 0 >
(r = 3)
w 12
w 21 = 0 =
Equations (4.43d) show that,
(4.43d)
4.5 Energy balance (First Law of Thermodynamics) w
= w W >
109
(4.44)
that is to say, they show that the Cauchy stress tensor is symmetric. The symmetry of the Cauchy stress tensor implies the symmetry of the Kirchho stress tensor, the second Piola-Kirchho stress tensor and the stress tensor defined in Eq.(3.28). For the first Piola-Kirchho stress tensor, which is not symmetric, we can define the following symmetry condition (see Eq.(3.15d)): w l w Lm [ L S
=
m w Ll w [ L S
=
(4.45)
4.5 Energy balance (First Law of Thermodynamics) To study the conservation of energy in our framework of Newtonian continuum mechanics, we will add to our set of variables a new one: the internal energy. Quoting (Marsden & Hughes 1983) we can state that the internal energy “represents energy stored internally in the body, which is a macroscopic reflection of things like chemical binding energy, intermolecular energy and energy of molecular vibrations”. Examples of internal energy are: • The energy stored in a deformed spring (elastic energy). • The energy stored in a heated body (thermal energy). • The energy stored in a bottle of oil (chemical energy). In the next chapter, when we study the di erent material constitutive relations we will present some phenomenological relations between di erent forms of internal energy and the continuum state variables (stress, strain, temperature, etc.). In the following subsections, we will derive the Eulerian (spatial) and Lagrangian (material) formulations of the First Law of Thermodynamics (Malvern 1969). 4.5.1 Eulerian (spatial) formulation of the energy balance For a body B in the w-configuration we define w u as its internal energy per unit mass. Being w N the kinetic energy of B defined by Eq.(3.9g), the total energy w H in the considered body, at the instant w, is Z w w w w H = wN + u dY = (4.46) wY
w
The external forces acting on the body provide a mechanical power input Sh{w . Using Eq.(3.9j), we write
110
Nonlinear continua w
Sh{w
Gw N = + Gw
Z
w
: w d w dY =
(4.47)
wY
We call “heat” (w T) the energy that flows due to a temperature gradient. We will consider two types of heat: • An outflowing heat flux through the body external surface (w q: heat flux vector). Examples are radiative and convective heat exchanges between the body B and the external medium. • An internal distributed heat source per unit mass (w u). Examples are chemical reactions, phase changes, etc. The total heat input to B at the instant w is, Z Z w w Tlqsxw = q · w n w dV + wV
w
w u w dY =
(4.48)
wY
Using the First Law of Thermodynamics, we can write Gw H = w Sh{w + w Tlqsxw Gw
(4.49a)
hence, G Gw
Z
wY
w
w
u
w
dY =
Z
w
w
w
: d dY
wY
+
Z
w
wV
Z
w
w u w dY =
q · w n w dV (4.49b)
wY
Using Gauss’ theorem (Eq.(4.5)), we get Z Z Z G w w w u w dY = : w d w dY u · w q w dY Gw w Y wY wY Z w w w u dY = (4.49c) + wY
Using in the above equation the expression of Reynolds’ transport theorem given in Eq.(4.4), we get w w ¸ Z ¡ ¢ C ( u) (4.49d) + u · w v w w u w dY Cw wY Z Z Z w w w w = : w d w dY u · w q w dY + u dY = wY
wY
wY
Now, we introduce in the integral on the l.h.s. of the above equation the result in Example 4.2, the Eulerian continuity equation in Eq.(4.19) and the definition of material derivative in Eq.(4.49d); hence,
4.5 Energy balance (First Law of Thermodynamics)
Z
wY
w
Gw u w dY = Gw
Z
w
: w d w dY
wY
+
Z
w
Z
wY
111
u · w q w dY
w u w dY =
(4.49e)
wY
The above equation is the integral form of the Eulerian formulation for the energy conservation principle. Since the above equation has to be fulfilled for any control volume that we define inside the continuum, we obtain the localized form of the energy conservation principle in the Eulerian formulation, w
Gw u = w : wd u · wq + w wu = Gw
(4.50)
JJJJJ Example 4.15. Following from the topic discussed in Examples 4.5 and 4.8, we consider a fluid moving with a velocity field w v and a moving control volume with a velocity field w w. In this example, we are going to analyze the energy balance inside the moving control volume. Using the generalized Reynolds’ transport theorem (Eq. (4.11)) for the fluid internal energy,we get Z Z Z ¡ ¢ Gw w C (w w u) w w w w w w u dY = dY + u w n · w w w dV = Gw (w) Cw
(w) (w) From the generalized Gauss’ theorem (Eq.(4.5)), Z Z ¡ ¡ ¢ ¢ w u · w w u w v w dY = n · w w u w v w dV
(w)
=
(w)
Subtracting the above equation from the previous one, ¸ Z Z ¡ ¢ Gw w C (w w u) w w w u dY = + u · w w u w v w dY Gw (w) Cw
(w) Z ¡ ¢ w w w + u n · w w w v w dV = (w)
Using the result in Example 4.2 and Eq.(4.19) (continuity equation), w ¸ Z Z ¡ ¢ Gw w Cu w w w w u dY = + w v · u w u w dY Gw (w) Cw
(w) Z ¡ ¢ w w w + u n · w w w v w dV = (w)
On the r.h.s. of the above equation, the term between brackets in the first
112
Nonlinear continua
integral is the material derivative of the fluid internal energy. Hence, using Eq.(4.50), Z ¤ £w : w d u · w q + w w u w dY
(w)
Z
Gw w = Gw
w
w u w dY +
w
Z
w
(w)
wu wn ·
¡w
v w w
¢
w
dV =
JJJJJ
4.5.2 Lagrangian (material) formulation of the energy balance Let us call w U the internal energy per unit mass in the w-configuration but referred to the reference configuration. Obviously, w
U ( {L > w) = w u (w {l > w) =
From Eqs.(3.10) and (3.20c), Z Z w : w d w dY = wY
Y
w S
:
(4.51a)
w ˙ dY %
(4.51b)
and using Eq.(2.76a), we define w
Q` = (w T` )D gD = [(w [ 1 )Dd w t d ] gD =
(4.51c)
For the heat sources per unit mass we can also define in the reference configuration, ³ ´ ¡ ¢ w U {L > w = w u w {l > w = (4.51d) Using the Piola Identity (Example 4.10), we can write Z Z ³ ´ u · w q w dY = GLY w M w Q` dY = wY
(4.51e)
Y
Hence, introducing into Eq.(4.49e) the results in Eq. (4.51a-4.51e), we get the integral form of the Lagrangian formulation for the energy conservation principle, Z Z Z ³ ´ w w w w ` G U w dY = S : % ˙ dY GLY M Q dY Gw Y Y Y Z w U dY = (4.52) + Y
Since the above equation has to be fulfilled for any volume that we define in the reference configuration, we get the localized form of the energy conservation principle in the Lagrangian formulation,
4.5 Energy balance (First Law of Thermodynamics)
Gw U = Gw
w S
:
w ˙ %
GLY
³
w
M w Q`
´
+
wU =
113
(4.53)
Example 4.16. JJJJJ Using Eq.(3.18), we can write an alternative localized form of the energy conservation principle,
Gw U = Gw
w W P
:
w ˙ X
GLY
³
w
M w Q`
´
+
wU
= JJJJJ
5 Constitutive relations
Following (Marsden & Hughes 1983) we can state that the constitutive relations in a continuum are the functional forms that adopt the stress tensor, the free energy and the heat flow as functions of the continuum deformation and temperature. Constitutive relations can be formulated using two di erent methodologies: (i) Studying the phenomena that takes place on the atomic scale (deformation of the atomic lattices, movement of dislocations, etc. (Dieter 1986)). (ii) Using phenomenological mathematical models that can match laboratory observations at the macroscopic scale. The phenomenological constitutive relations are generally used in continuum mechanics and we will concentrate on this approach in this chapter. This chapter is intended as an introduction to a large number of di erent constitutive models; hence, the recommended literature has to be classified into di erent areas: • For studying the fundamentals that have to be considered for formulating constitutive relations some reference books are: (Truesdell & Noll 1965, Malvern 1969, Marsden & Hughes 1983). • For studying hyperelasticity: (Ogden 1984). • For studying plasticity: (Hill 1950, Mendelson 1968, Johnson & Mellor 1973, Lubliner 1990, Simo & Hughes 1998, Koji´c & Bathe 2005). • For studying viscoplasticity: (Perzyna 1966, Koji´c & Bathe 2005). • For studying viscoelasticity: (Pipkin 1972). • For studying damage mechanics: (Lamaitre & Chaboche 1990).
116
Nonlinear continua
5.1 Fundamentals for formulating constitutive relations In this section, we will discuss some principles that shall be considered when developing a constitutive relation for modeling the behavior of any material. 5.1.1 Principle of equipresence This principle has been proposed in (Truesdell & Toupin 1960) and very generally states that any independent variable that is included in the formulation of any constitutive relation for a given material has to be included in the formulation of all the other constitutive relations that are developed for the same material unless it is shown that its inclusion is either not necessary or violates some physical law. Often, the constitutive models used by scientists and engineers are derived considering a very simplified material behavior and some variables are not included in the derived relation; e.g. usually when stating the relation between heat flux and temperature the continuum deformations are not considered (Fourier’s Law). The principle of equipresence requires that these simplifications should not be made “by default” and that each of them should be specifically analyzed. These analyses will also be helpful for evaluating and understanding the limitations of the obtained results. 5.1.2 Principle of material-frame indi erence This principle states that the continuum constitutive relations shall be formulated using objective physical laws (see Section 2.12). When using Cartesian coordinate systems in the spatial and material configurations, only classical objectivity is required. In more general cases, covariant formulations should be used. Quoting (Ogden 1984), we can describe classical material objectivity as: “An important assumption in continuum mechanics is that two observers in relative motion make equivalent (mathematical and physical) deductions about the macroscopic properties of a material under test. In other words, material properties are una ected by a superposed rigid motion, and the relation between the stress and the motion has the same form for all observers”. 5.1.3 Application to the case of a continuum theory restricted to mechanical variables This theory considers some measure of the continuum deformations as the only independent variable and some measure of the continuum stresses as the only dependent variable. Since many of the physical problems usually analyzed by scientists and engineers correspond to this category, it is an important case to be considered. In (Truesdell & Noll 1965) the following principles are proposed for the specific case of a continuum theory restricted to mechanical variables:
5.1 Fundamentals for formulating constitutive relations
117
• Stresses are deterministic functions of the continuum deformation history. • Local action: the stresses acting on a material particle (material point) are only a function of the strains at the same material particle and not of the strains at neighboring particles. It is important to note that nowadays nonlocal continuum theories are used for very specific problems (PijaudierCabot, Baˇzant & Tabbara 1988). Hence, we consider the principle of local action as a convenient hypothesis that, although it does not represent a physical law, provides a simplification to the constitutive relations that agrees with physical observations for many materials.
Example 5.1. JJJJJ Let us assume that for a problem in which only mechanical variables are considered, we formulate the following constitutive relation: w
= wm
¡
¢
w X
where w m is a tensorial function that maps the space of invertible two-point tensors into the space of symmetric Eulerian tensors (Ogden 1984). It is important to realize that w m depends on the selected reference configuration. Since we have restricted ourselves to study a purely mechanical problem we can accept that the proposed constitutive relation fulfills the principle of equipresence. To study the objectivity of the formulation (classical objectivity) we consider in the spatial configuration two Cartesian coordinate systems: a fixed one { w } } and a moving one { w } }. Since the Cauchy stress is an objective spatial tensor, from Eq. (2.101c), w
= Q(w) ·
w
· QW (w)
where Q(w) is an orthogonal tensor. And since the deformation gradient tensor is a two-point objective tensor, from Eq. (2.102c): w w X = Q(w) · X = Since the above relation is valid for any orthogonal Q, in particular it is also valid for w R (from the polar decomposition w X = w R · w U ). The observer in the moving frame writes, due to material objectivity, ¡ ¢ w = w m w X and using variables measured in the stationary frame, ³ ´ w = w m w RW · w R · w U = w RW · w · w R =
118
Nonlinear continua
Hence, w
= Q(w) · w m
¡w
¢
U
· QW (w) =
¡ ¢ The principle of material-frame indi erence imposes w m w U instead of ¡ ¢ w m w X . The requirements of determinism and local action are obviously fulfilled. JJJJJ Example 5.2. JJJJJ As an alternative formulation to the one presented in Example 5.1, we assume that for a problem in which only mechanical variables are considered ¡ ¢ w W = w N w X P
where w N is a tensorial function that maps the space of invertible two-point tensors into a space of general two-point tensors. The relation between w m (in Example 5.1) and w N can be derived using Eq. (3.15d). For the fulfillment of the principle of equipresence, we make the same comment as in the above example. Again, to study the objectivity of the formulation, we consider in the spatial configuration two Cartesian systems: a fixed one {w } } and a moving one {w } }. Since the first Piola-Kirchho stress tensor is an objective two-points tensor, from Eq. ( 2.102c): w W = Q (w) · w PW > P where Q (w) is an orthogonal tensor. In the same way w w X = Q (w) · X = The observer in the moving frame writes, due to material objectivity, w W P
and particularizing for = w R · w U ),
Q (w)
= =
¡
w w N X w R
¢
>
(from the polar decomposition
w X
w W P
Hence,
=
w N
³
w W R
w W P
´ · w R · w U =
= Q(w) · w N
¡w
¢
U
w W R
· w PW =
=
The principle of material-frame indi erence imposes the above form for the constitutive relation. JJJJJ
5.1 Fundamentals for formulating constitutive relations
119
Example 5.3. JJJJJ Another alternative formulation for a pure mechanical problem is, ¡w ¢ w w S = M X
where w M is a tensorial function that maps the space of invertible two-point tensors into the space of symmetric Lagrangian tensors. The relation between w m (in Example 5.1) and w M can be derived using Eq. (3.19). For the fulfillment of the principle of equipresence, we make the same comment as in Example 5.1. To study the objectivity of the formulation, as usual, we consider two Cartesian systems in the spatial configuration: a fixed one {w } } and a moving one {w } } = Since the second Piola-Kirchho stress tensor is an objective Lagrangian tensor, we have: w S
=
w S
=
From the objectivity of the deformation gradient tensor it follows that (Eq. (2.102c)), = Q (w) · w X
w X
where Q (w) is an orthogonal tensor. Due to material objectivity, the observer in the moving frame writes: ¡ ¢ w = w M w X S
and particularizing for w w w X = R · U ),
w S
w R
Q (w) =
=
w M
Hence,
³
w S
w W R
=
and using w U
=
we get, w S
=
(from the polar decomposition
´ · w R · w U =
w M
¡
¢
w U
w S=
>
£ w ¤1@2 2 % + I ¡ ¢
wc w M %
=
The principle of material-frame indi erence imposes the above form of the JJJJJ constitutive relation.
120
Nonlinear continua
5.2 Constitutive relations in solid mechanics: purely mechanical formulations In this section we will analyze some of the constitutive relations that are used to model the mechanical behavior of solids, neglecting the couplings with other physical phenomena. An elastic material model (also called Cauchy elastic material (Ogden 1984)) predicts a material behavior independent of the material history and time, that is to say, stresses are univocally determined by strains and vice versa. Of course, an elastic material model cannot be used to model: permanent deformation phenomena, damage of materials, creep e ects, strain-rate e ects, etc. In Chap. 3 we presented the definition of conjugate stress and strain rate measures. If we define an arbitrary stress measure T (it can be either a Lagrangian, Eulerian or two-point tensor) and its conjugate strain-rate measure ˙ , we can write the stress power per unit volume as, E ˙ > S = TW : E
(5.1a)
T = T(E) >
(5.1b)
for an elastic solid, hence, ˙ S = TW (E) : E
=
(5.1c)
In general (Ogden 1984), we cannot assess on the existence of a scalar function, X (E) , such that, ˙ > X˙ = TW (E) : E
(5.1d)
that is to say, in general S is not an exact di erential. When S is an exact di erential, we can write ( 1944) CX ˙ = TW (E) : E ˙ > : E X˙ = CE
(5.1e)
and we say that the material model is hyperelastic (also called Green elastic material model (Ogden 1984)). For a hyperelastic material model, from Eq. (5.1e) taking into account ˙ is arbitrary, that E CX > (5.1f) TW (E) = CE and X is called the elastic energy function per unit volume.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
JJJJJ
Example 5.4. For a hyperelastic material, CX CHlm
W lm = and since
121
W no =
;
CX CHno
C2X C2X = > CHlm CHno CHno CHlm
we must have
CW no CW lm = = CHno CHlm JJJJJ
The inelastic mechanical behavior of some materials can be described with equations of the form, dT = C(T > E) : dE >
(5.2)
which are the hypoelastic material models. 5.2.1 Hyperelastic material models For a hyperelastic material, the elastic energy in the spatial configuration per unit volume of the reference configuration can be written as: d w U =
w LM V
d w %LM >
(5.3a)
using the second Piola-Kirchho stress tensor and the Green-Lagrange strain tensor. If we use w U as the elastic energy in the spatial configuration per unit mass, we get gp (5.3b) d w U = dw U gp = Hence, dw U = and w LM V
=
1 w LM V
d w %LM >
CwU CwU = 2 w = w C %LM C FLM
(5.3c)
(5.3d)
Using the chain rule and considering Eq. (4.51a), we can write (Marsden & Hughes 1983) C w U Cw FDE Cwu = > (5.4a) C w jde Cw FDE C w jde
122
Nonlinear continua
from Eq. (2.93a) w FDE
= w jde w [ dD w [ eE >
(5.4b)
and therefore CwU w d w e CwU Cwu w = w )= [ D [ E = ! ( w w C jde C FDE C FDE
(5.4c)
Pushing-forward Eq. (5.3d) and using the above, we obtain w lm
= 2
Cwu > C w jlm
(5.4d)
and using Eq. (3.12) we obtain the Doyle-Ericksen formula (Simo & Marsden 1984): Cwu w lm = 2 w w = (5.4e) C jlm It is important to realize that the above is the correct relation for deriving the Cauchy stress tensor from the elastic energy per unit mass function, and that (Marsden & Hughes 1983): w lm
6= 2 w
Cwu C w hlm
=
(5.5)
Using the result in the Example 4.16 and remembering that for a hyperelastic material the stress is only a function of the state variables, we also get w E Sd
=
CwU C w [ dE
=
5.2.2 A simple hyperelastic material model In this section we will develop the simplest possible hyperelastic material model: the isotropic, linear hyperelastic material model. To use Eq. (5.3d), in the reference configuration we need to define the strain energy per unit volume of the reference configuration w U
=
w w U( %LM )
>
(5.6a)
the simplest definition is: w U
where w D ; mation).
=
w D
w LM E
+
and
w LM w E %LM a w LMNO F
+
1 w a LMNO w w F %LM %NO > 2
(5.6b)
are constants (independent of the defor-
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
123
• The value of w D is arbitrary since we are only interested in the derivatives of w U , therefore we set w = (5.6c) D = 0 • Using Eq. (5.1f) with Eq. (5.6b) we get, ¶ µ a 1 w a LMNO w LM w LM w NOLM w = E + F + F V %NO 2
=
(5.6d)
Since we are not considering an initial stress/strain state, = 0 +, w V LM = 0 and therefore, we must have
w %LM
w LM E
= 0=
(5.6e)
Hence, for the simplest hyperelastic material model, we have the elastic energy per unit volume of the reference configuration expressed as a quadratic form of the Green-Lagrange strain tensor; w U
=
1 w a LMNO w w F %LM %NO 2
(5.7a)
and a linear stress/strain relation, w LM V
=
w LMNO w F %NO
(5.7b)
where (Malvern 1969), w LMNO F
1 = 2
µ
a w LMNO F
+
a w NOLM F
¶
=
(5.7c)
Doing a push-forward of the above equation to the spatial configuration we get, w lm = w flmno w hno (5.8a) where the spatial elasticity tensor is defined by w lmno
f
=
w LMNO w l w m w n w o F [ L [ M [ N [ O
=
(5.8b)
Note that the obtained spatial elasticity tensor has components that are a function of the deformation (not constant). The Second Law of Thermodynamics indicates that for deforming a real (stable) material we must spend an amount of work; hence, w U
0
(5.9)
and we can only have w U = 0 when w % = 0 . Therefore, w U is a positive definite quadratic form. Using Eqs. (5.7b) and (5.8a) together with the quotient rule (Sect. A.5) we realize that w F LMNO and w flmno are components of two fourth-order tensors, w w C and c .
124
Nonlinear continua
I Symmetries of In Eq. (5.7b) hence,
w C
w LM V
and
w LM %
are components of symmetric tensors;
w LMNO F
=
w MLNO F
w LMNO F
=
w LMON F
(5.10a) =
(5.10b)
Therefore the original 81 components of w C are reduced to only 36 independent ones. Using for this case the result in Example 5.4 we arrive at, w LMNO F
=
w NOLM F
=
(5.11)
Therefore, we are left with only 21 independent constants. It is important to note that while Eqs. (5.10a-5.10b) apply to any material, Eq. (5.11) is only valid for a hyperelastic material. Without introducing any symmetry inherent to a particular material model, for the description of the most general linear hyperelastic material model we have to use 21 material constants. Now we will consider materials with inherent symmetries, that is to say, with planes of elastic symmetry. Let us first consider a material with one plane of elastic symmetry; this means that if we define two coordinate systems { {L } and { { ˜L } with: 1 • { and {2 on the symmetry plane, • {3 normal to the symmetry plane, • { ˜1 = {1 ; { ˜2 = {2 and { ˜3 = {3 , we must have w LMNO = w F˜ LMNO = (5.12) F Taking into account the tensor transformations w ˜ LMNO F
=
w S TUV F
C{ ˜L C { ˜M C { ˜N C { ˜O S T U C { C { C { C {V
(5.13)
it is obvious that the fulfillment of Eq. (5.12) imposes that the components with an odd quantity of indices “3” have to be zero. Hence, a plane of elastic symmetry reduces the material constants from 21 to 13. Now we consider a further simplification imposed by the consideration of more elastic symmetries: the orthotropic hyperelastic material model. In this case we have to consider three mutually orthogonal planes of elastic symmetry. The intersection of the three orthotropy planes determines a Cartesian coordinate system { } }.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
125
Besides the symmetry considerations with respect to the ( } 1 > } 2 ) plane, derived above, we have to consider a symmetry with respect to the ( } 2 > } 3 ) plane (Sokolniko 1956). The fulfillment of Eqs. (5.12) and (5.13) imposes, for this second symmetry, a further 4 zero material constants; hence, an orthotropic material model has only 9 material constants. Examples of materials that are adequately described using orthotropic material models are wood, rolled steel plates, etc. It is interesting to examine further the orthotropic constitutive relation using the following arrays: 5 6 5 65 6 w 11 w 1111 w 1122 w 1133 w V F F F 0 0 0 % 9 : 9 : 9 11 : 9 : 9 :9 : 9w 9w V 22 : 9 : w 2222 w 2233 0 0 0 : 9 : 9 : 9 %22 : F F 9 : 9 :9 : 9w 33 : 9 :9 w : w 3333 9 9 V : 9 : 0 0 0 % : F 9 :=9 : 9 33 : = (5.14) 9 : 9 :9 : w 1212 9 w : 9w V 12 : 9 0 0 : 9 : 9 : 92 %12 : F 9 : 9 :9 : 9w 23 : 9 :9 : w 2323 9 V : 9 0 : 92 w %23 : F 7 8 7 87 8 w w 3131 w 31 2 %31 v|p F V It is obvious from the above equation that if the orthotropy axes are coincident with the principal axes of strain, they are also the principal axes of the stress tensor (collinearity between the stress and strain tensor). When for an orthotropic material the constitutive relation is written in a coordinate system that is not coincident with the material orthotropy system, the convenient form of Eq. (5.14) is lost. I The isotropic hyperelastic material model An important case of materials with inherent symmetry is analyzed in this section: when every plane is a plane of elastic symmetry we have an isotropic material; therefore w C is an isotropic fourth-order tensor (Aris 1962). It was shown in (Aris 1962) that the most general fourth-order isotropic tensor has Cartesian components of the form, w F
= + ( + ) + ( ) = (5.15) Any of the two Eqs. (5.10a-5.10b), derived from the symmetry of the stress and strain tensors, imposes the condition: = 0
=
(5.16)
Hence, it is obvious from Eqs. (5.15) and (5.16) that in the case of isotropic materials there are only 2 independent constants; usually (Malvern 1969):
126
Nonlinear continua
• H : Young’s modulus • : Poisson’s ratio. For any Cartesian system we can write Eq. (5.14) as, (Bathe 1996): 5
6
65
5
9 1 1 9 : 9 9w V 22 : 9 1 9 : 9 9 : 9 9w 33 : 9 9 V : 9 9 : = H (1) 9 9 : (1+) (12) 9 9w V 12 : 9 9 : 9 9 : 9 9w 23 : 9 9 V : 9 7 8 7 w 31 v|p V w 11 9 V :
1
0
0
1
0
0
1
0
0
12 2(1)
0 12 2(1)
0
6 w %11
:9 : :9 : 9 : w 0 : 9 %22 : : :9 : :9 w : 0 : 9 %33 : :9 : > :9 : w 9 : 0 : 92 %12 : : :9 : :9 w : 9 : 0 2 % : 8 7 23 8 12 2 w %31 2(1) (5.17)
and the stress and strain tensors are always collinear. It is important to realize that the numerical values of H and usually found in the engineering literature refer to the relation [Cauchy stresses/infinitesimal strains] rather than to the relation [second Piola-Kirchho stresses/Green-Lagrange strains] that we use in this section. We can define N , the volumetric modulus and J , the shear modulus as:
N =
H 3 (1 2)
(5.18a)
J =
H 2 (1 + )
(5.18b)
and write for the simplest hyperelastic material model that we consider in this section, w V w U
0
= N w %Y + 2 J w % =
1 2 N w %Y + J w %0 w %0 2
(5.19a) (5.19b)
where, w %Y is the volumetric or hydrostatic component or the Green-Lagrange strain tensor, w %Y = w % , and w %0 ] is the deviatoric component of the Green-Lagrange strain tensor, w %0 = w % 13 w %Y . From Eq. (5.19a-5.19b) we conclude that: N 0 J 0
(5.20a) =
(5.20b)
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
It is important to realize that volume change. The above implies,
w %Y
127
is not a measure of the continuum
H 0 1 0=5
(5.20c) =
(5.20d)
We must remember that the symmetries discussed in the last two Sections are directional properties and not positional properties. Even if a material has a certain elastic symmetry at each point, the properties may vary from point to point in a manner not possessing any symmetry with respect to the shape of the analyzed body (Malvern 1969). When considering an isotropic material w S and w % are always collinear tensors. Example 5.5. JJJJJ In the above equations we expressed the constitutive tensor for orthotropic and isotropic material in Cartesian coordinates. To express it in a general coordinate system { {L } we use: ¡ ¢¡ ¢¡ ¢¡ ¢ w ˜ LMNO = w F e · gL e · gM e · gN e · gO = F Even though the material is still defined by the same number of material JJJJJ constants, the convenient form of Eqs. (5.14) and (5.17) is lost. JJJJJ Example 5.6. A hyperelastic constitutive model cannot be formulated, in the spatial configuration, as w lm = w flmno w hno (A) where w c is a constant and isotropic fourth order tensor If Eq. (A) is an acceptable constitutive relation, then taking Lie derivatives on both sides of the equal sign, we get for a hyperelastic material, w
lm
= w flmno w gno =
In Example 5.14, we will show that the above equation cannot represent a hyperelastic material; hence, Eq. (A) cannot either. It is important to point out that in (Simo & Pister 1984) it was also demonstrated that the spatial elasticity tensor cannot be an isotropic and constant fourth-order tensor. Simo and Pister developed their demonstration without the need of going through an equivalent hypoelastic material; however, we could not reproduce the demonstration in (Simo & Pister 1984). JJJJJ
128
Nonlinear continua
5.2.3 Other simple hyperelastic material models In Sect. 5.2.1 we have formulated a simple hyperelastic material model using: w U
=
1 w % : 2
w S
=
C w U = C w %
w C
:
w %
(5.21a) (5.21b)
We can use other conjugate stress/strain rate measures and get, using for the elastic energy per unit volume in the reference configuration quadratic forms with constant coe!cients: w U w
=
=
1 w H : 2
w C
Cw U C w H
:
w H
=
(5.22a) (5.22b)
As we saw in Sect. 3.3.4, Eqs. (5.22a-5.22b) can only be used with isotropic materials. Even considering the above limitation, Eqs. (5.22a-5.22b) are very useful for formulating practical constitutive relations because it was experimentally shown by Anand that for metals, the values of H and that are used in the usual engineering environment [Cauchy stresses/infinitesimal strains] can be accurately used in Eqs. (5.22a-5.22b) for quite large strain values (Anand 1979). Also, for the case of infinitesimal strains, w U
=
1 w % : 2
w C
: w% >
Cw U > C w% µ ¶ w C U w = > w C w%
w
=
(5.23a) (5.23b) (5.23c)
where w % is the infinitesimal strain tensor defined in Example 2.26. In this case since w , w w . The above equations are possible because G w% = wd Gw
=
(5.24)
As we have seen above, in Eq. (5.5), it is not possible to use an alternative hyperelastic formulation in terms of the Almansi strain tensor.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
129
5.2.4 Ogden hyperelastic material models For an isotropic material we can write, w U
=
w U(1 > 2 > 3 )
(5.25)
where the l are the eigenvalues of the second order tensor, w U, that is to say, the principal stretches defined in Eq. (2.58e). Since l = l (L1F > L2F > L3F ) (5.26) where the values (L1F > L2F > L3F ) are the invariants of w C defined in Eqs. (2.59b2.59d); we can write w U
w F F F U(L1 > L2 > L3 )
(5.27a)
L1F = (1 )2 + (2 )2 + (3 )2
(5.27b)
L2F = (2 )2 (3 )2 + (3 )2 (1 )2 + (1 )2 (2 )2
(5.27c)
=
2
2
2
L3F = (1 ) (2 ) (3 ) =
(5.27d)
w F F F ¢ ¡proposed ¢ ¡toFwrite¢ U(L1 > L2 > L3 ) as an infinite series in powers of ¡ FOgden F L1 3 > L2 3 > L3 1 (Ogden 1984). Thus, w U(1 > 2 > 3 )
=
4 X
s>t>u=0
¢s ¡ F ¢t ¡ F ¢u ¡ Fstu L1F 3 L2 3 L3 1
(5.28)
where the coe!cients Fstu are independent of the deformation. For the unstrained configuration, 1 = 2 = 3 = 1 L1F = 3 L2F = 3 L3F = 1 = Therefore, in the unstrained configuration the strain energy per unit mass is zero provided that F000 = 0. Also, the unstrained configuration has to be stress free; hence, Cw U F | F F =0 Cl L1 =L2 =3;L3 =1
i ru l = 1> 2> 3 =
(5.29a)
The above equation leads using Eq. (5.28), to the condition, F100 + 2 F010 + F001 = 0 =
(5.29b)
130
Nonlinear continua
Example 5.7. JJJJJ The third invariant, L3F , has an important physical interpretation. Considering the eigendirections of w U , a di erential volume dY defined in the reference configuration along those directions is transformed, in the spatial configuration, in a di erential volume w dY : w
dY = 1 2 3 dY
hence, w
w
dY = dY
M =
q L3F =
That is to say, the invariant L3F describes the volume change during the continuum deformation. Obviously, for incompressible deformations, w
M = L3F = 1 = JJJJJ
Here Ogden introduces a simplificative hypothesis: the strain energy is decoupled in two parts, a deviatoric part that is independent of the volume change and a volumetric part that is only a function of the volume change (Ogden 1984). The above hypothesis is introduced in Eq. (5.28) by imposing, w U(1 > 2 > 3 )
4 X
=
s>t=0
+
4 X u=1
We can state, j(L3F )
=
¢s ¡ F ¢t ¡ Fst0 L1F 3 L2 3
¢u ¡ F00u L3F 1 =
4 X u=1
¢u ¡ F00u L3F 1
(5.30)
(5.31)
and retain only a few terms in Eq. (5.30); in this way we obtain specific hyperelastic relations that have been successfully used for particular materials. For example, for incompressible materials: L3F = 1 j(L3F ) w U
(5.32a)
=0 =
4 X
s>t=0
(5.32b) ¢s ¡ F ¢t ¡ Fst0 L1F 3 L2 3 =
(5.32c)
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
131
• Retaining only two terms in Eq. (5.32c) we obtain the Mooney-Rivlin strain energy function that has been successfully used for rubber-like materials, w U
¢ ¢ ¡ ¡ = F100 L1F 3 + F010 L2F 3 =
(5.33)
• If F010 = 0 the above reduces to the neo-Hookean strain energy function which has played an important role in the development of the theory and applications of nonlinear elasticity, w U
¢ ¡ = F100 L1F 3 =
(5.34)
The principal values of the collinear Green-Lagrange and second PiolaKirchho tensors are related by, w Vl
=
C w U C w U Cm = C%l Cm C%l
(5.35a)
taking into account that the %l are the eigenvalues of the Green-Lagrange strain tensor, we can write Cm 1 = ml C%l m
(no addition on m) =
(5.35b)
Hence,
1 Cw U (no addition on l) . (5.35c) l Cl With a push-forward of the above, we get the eigenvalues of the Kirchho stress tensor, Cw U w l = l (no addition on l) . (5.35d) Cl Hence, the eigenvalues of the Cauchy stress tensor are, µ w ¶ Cw U w l = (no addition on l) . (5.35e) l Cl w Vl
=
When the material is incompressible the three values of l are not independent since they have to fulfill the relation, w
M 1 = 1 2 3 1 = 0 =
(5.36a)
In this case, Eq. (5.35a) determines the eigenvalues of the Cauchy stress tensor except for the value of the hydrostatic pressure, 4S : w
l = l
Cw U + 4S Cl
(no addition on l) =
(5.36b)
For determining the value of the hydrostatic pressure the equilibrium equations shall be used.
132
Nonlinear continua
Example 5.8. JJJJJ In the case of the biaxial tension of a square incompressible sheet (Ogden 1984), 1 2 3 = 1 ˆ 1 = 2 = therefore, 3 =
1 = ˆ ()2
Also, w
1 = w 2 = w ˆ w 3 = 0 = Using the constitutive equation of the incompressible neo-Hookean material we get, 2 2 2 w U = F100 (1 + 2 + 3 3) = Equations (5.36b) give, w
ˆ 2 + 4s ˆ = 2F100 () 0 = 2F100
Hence, w
ˆ = 2F100
"
1 + 4s = ˆ ()4
ˆ 1 () ˆ 4 () 2
#
=
In plane Cauchy stresses in the biaxial tension of a square incompressible sheet JJJJJ
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
133
Example 5.9. JJJJJ For the case of an incompressible cube subjected to a uniform tension on its faces, in (Marsden & Hughes 1983) a neo-Hookean material is considered with a strain energy function of the form, ¤ £ 2 2 2 w U = F100 1 + 2 + 3 3 =
Incompressible cube subjected to a uniform tension on its faces Using Eqs. (5.36b), we get w
l = 2F100 (l )2 + 4s
(l = 1> 2> 3) =
From the equilibrium between internal and external forces, and taking into account that due to incompressibility 1 2 3 = 1 we get, 2F100 (1 )2 + 4s = w 1 > 2F100 (2 )2 + 4s = w 2 > 2F100 (3 )2 + 4s = w 3 > where w = |w| =
134
Nonlinear continua
Eliminating 4s gives, [2F100 (1 + 2 ) w] (1 2 ) = 0 [2F100 (2 + 3 ) w] (2 3 ) = 0 [2F100 (3 + 1 ) w] (3 1 ) = 0 = In the intuitive case 1 = 2 = 3 and the above equations are automatically fulfilled. However, we will explore the possibility of other solutions. • If we assume 1 6= 2 6= 3 we must have
w = 2F100 (1 + 2 ) = 2F100 (2 + 3 ) = 2F100 (3 + 1 ) = Hence, we must have 1 = 2 = 3 = This contradiction shows that the assumed solution is not possible. • If we assume that two l s are equal and the third one is di erent, for example: 1 = 2 6= 3 > we get
w = 2F100 (1 + 3 ) and due to incompressibility we must have, " # 1 2F100 1 + 2 w=0 = (1 ) In order to obtain 1 = 1 (w) we must solve the equation i () = 31
w 2 + 1 = 0 = 2F100 1
Considering that only the positive roots are admisible, it is shown in (Marsden & Hughes 1983) that: s 3 ¤ If w ? 3 s 2 F100 =, no roots 1 A 0= 3 ¤ If w = 3 s 2 F100 =, one root 1 A 0= ¤ If w A 3 3 2 F100 =, two positive roots 1 A 0= Hence,
w=3
s 3 2 F100
is a bifurcation load.
JJJJJ
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
135
5.2.5 Elastoplastic material model under infinitesimal strains In this section we are going to present the elastoplastic material model, considering only a purely mechanical formulation and infinitesimal strains. In forthcoming sections we are going to present a thermoelastoplastic material model and we are going to extend the model to consider finite strains. The elastoplastic material model has to describe the following experimentally observed phenomena: • For loads below a certain limit loading condition, established via a yield criterion, the material behavior is elastic and can be described using the hyperelastic relations that we have discussed above. • When the limit loading condition is reached there is an onset of permanent or plastic deformations. • The plastic deformations produce an evolution of the yield condition that is described via a hardening law. • When the limit loading condition is reached and then an unloading takes place, elastic deformations are developed. • The material behavior is rate independent, that is to say, the material behavior is not a function of the loading or deformation rate. • The material is stable: we have to spend mechanical work in order to deform it. I 1D case The above observations easily fit into our experience of the 1D load/displacement curve of a steel sample under tension. In the 1D case it is obvious that (see Fig. 5.1): W rwdo 4O = Hodvwlf 4O + S odvwlf 4O =
(5.37a)
For the case of infinitesimal strains, dividing the above by O> we have w
% = w %H + w %S
(5.37b)
where w % : total axial strain in the sample, w %H : elastic axial strain in the sample and w %S : plastic axial strain in the sample. During the plastic loading we can also write, following Fig. 5.2, that 4% = 4%H + 4%S =
(5.37c)
Dividing Eq. (5.37c) by 4w and taking the limit for 4w $ 0 we get for the simple 1D case, w %˙ = w %˙ H + w %˙ S = (5.37d) For the 3D case we generalize the above equation using Eq. (5.24) and get the additive decomposition of the strain-rate tensor,
136
Nonlinear continua
Fig. 5.1. Tensile test of a steel sample
Fig. 5.2. Plastic loading (zoom) w
d = w dH + w dS =
(5.38)
It is important to note that, for the moment, we are postulating the above decomposition only for the case of infinitesimal strains, a very important one for standard engineering applications. In the 1D mechanical test described in Fig. 5.1 it is quite obvious that the loading condition is, w ˙ S A0> (5.39a) and when loading: if w S ?
S|lhog
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
4OH =
4S DH
O
4OS = 0 > if w S >
137
(5.39b) (5.39c)
S|lhog 4OH =
4S DH
O
4OS A 0 >
(5.39d) (5.39e)
where D is the sample transversal area, that due to the assumption of infinitesimal strains we consider as being constant, and H is the steel Young’s modulus. As is shown in Fig. 5.1 when we reach a load w S|lhog and unload w
S˙ ? 0
4OH =
4S DH
(5.40a)
O
4OS = 0 =
(5.40b) (5.40c)
Let us assume now that, when unloading, we reach a value SX O > 0 and then start loading again: w ˙ S A0 (5.41a) the behavior will be elastic (Eqs. (5.39b) and (5.39c)) for w
S ? w S|lhog
(5.41b)
and elastoplastic (Eqs. (5.39d) and (5.39e)) for w
S > w S|lhog =
(5.41c)
Let us divide in Fig. 5.3 the S ydoxhv by D (assumed constant during the deformation) and the 4O ydoxhv by O . We get the diagram shown in Fig. 5.3 (Cauchy stress vs. infinitesimal strain). For a material having a softening behavior, rather than a hardening behavior, we would have the % diagram shown in Fig. 5.4 . It is evident in this figure that when we go from point “1” to point “2” :
138
Nonlinear continua
Fig. 5.3. -% for a steel sample
Fig. 5.4. Softening in the 3 % relation
4 ? 0
(5.42a)
4%S A 0
(5.42b)
4 4%S ? 0 =
(5.42c)
and therefore We will now show that the above stress/strain relation is incompatible with the requirement of material stability.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
139
Let us now assume that the 1D sample is in equilibrium at “0” and an external agent makes it describe the loading-unloading path 0 1 2 3, described in Fig. 5.4. The work performed by the external agent per unit volume of the sample is, Z
Zh=d= =
1
%˙ dw + 0
Z
Z
2
%˙ dw +
1
1
%˙ dw
0
Z
Z
2
2
%˙ dw
1
3
%˙ dw Z
3
%˙ dw =
(5.43)
2
For a stable material it must be Zh=d= > 0 =
(5.44)
Taking into account that in the paths 0 1 and 2 3 we are inside the elastic range, we can write
Zh=d= =
Z
1 H
( ) %˙
dw +
0
Z
Z
2
( ) %˙ H dw +
1
3 H
( ) %˙ dw +
2
Z
2
( ) %˙ S dw =
(5.45)
1
The first three integrals on the r.h.s. of the above equation add up to zero because they correspond to a loading-unloading elastic cycle and there is neither energy dissipated nor generated in that cycle. Z 2 Zh=d= = ( ) %˙ S dw = (5.46) 1
When “1” and “2” are infinitesimaly close,
d2 Zh=d= = d d%S 6 0 =
(5.47)
The points on the softening branch are in unstable equilibrium. The material shown in Fig. 5.4, with a softening behavior is not stable. However, it is possible to obtain diagrams S 4 with a softening region; for example: • In the 1D test of a steel sample after necking (localization). In this case, the hypothesis of constant area is not valid and using at every configuration the actual area for constructing the diagram in Fig. 5.4 (true stress), we get a hardening behavior rather than a softening one.
140
Nonlinear continua
• In the 1D test of a concrete sample. During the descending branch of the S curve there are micro-cracks propagating inside the sample; hence, again the consideration of a uniform stress across the transversal section is not realistic (Ottosen 1986). In what follows, we will generalize the intuitive concepts of this 1D example to a general 3D formulation. I The general formulation For the general formulation of an elastoplastic material model we need the following three ingredients: • A yield surface that in the 3D stress space describes the locus of the points where the plastic behavior is initiated. • A flow rule that describes the evolution of the plastic deformations. • A hardening law that describes the evolution of the yield surface during the plastic deformation process. The yield surface In the stress space, for a given material we can define a yield surface, w
i ( w > w tl l = 1> q ) = 0
(5.48)
where w is the Cauchy stress tensor and w tl are internal variables to be defined for every particular yield criterion. The elastic range is described by the inequality w
i ?0
(5.49a)
and the plastic range by the equality w
i =0=
(5.49b)
Note that w i A 0 is not possible in the elastoplastic framework. Many di erent yield functions have been proposed over the years to phenomenologically describe the behavior of di erent materials (Chen 1982, Lubliner 1990). In this section, we concentrate on the yield function that is generally used to describe the behavior of metals: the von Mises yield function. In his experimental work, developed in the 1950s, Bridgman found that for metals, it can be assumed that the yield function is not a ected by the confining hydrostatic pressure - at least for not very extreme hydrostatic pressures (Hill 1950 and Johnson & Mellor 1973). It is important at this point to introduce the following decomposition of the Cauchy stress tensor:
5.2 Constitutive relations in solid mechanics: purely mechanical formulations w
= ws +
´ 1 ³w : wg wg 3
141
(5.50a)
which in Cartesian coordinates is written as, w
= w v +
¢ 1¡w * w * w = 3
(5.50b)
In the above equation w s is the deviatoric Cauchy stress tensor and h ³ ´i 1 w w : g is the hydrostatic or spherical component of the Cauchy stress 3 tensor . Using the above decomposition together with Bridgman experimental observations for the case of metals, we can write Eq. (5.48) as, w
i ( w s > w tl l = 1> q ) = 0 =
(5.51)
Taking into account that the first invariant or trace of the deviatoric Cauchy stress tensor is, w s : wg = 0 (5.52) we can write Eq. (5.51) for an isotropic material whose behavior is symmetric in the stress space as, ¡ ¢ w i w M2 > w M3 > w tl l = 1> q = 0 (5.53) where w M2 and w M3 are the second and third invariant, respectively, of the deviatoric Cauchy stress tensor.
By isotropic material we mean that the yield condition does not distinguish orientations predefined in the material. Experimental results indicate that when the yield surface is intersected in the stress space with a plane that forms equal angles with the three principal stress axes, a good approximation for the obtained curve is a circle. Therefore, von Mises proposed ¡ ¢ w i w M2 > w tl l = 1> q = 0 =
(5.54)
Hence, the von Mises yield function is also known as the w M2 -yield function (Simo & Hughes 1998). More specifically the actual form of Eq. (5.54) can be written as, w
i=
or, w
i=
2 ¢ ¡ ¢ 1¡w (w | ) s w : ws w =0 2 3
¸ ¢ ¡ ¢ 1@2 3¡w s w : ws w w | = 0 = 2
In the above we have introduced the following internal variables:
(5.55)
(5.56)
142
Nonlinear continua
Fig. 5.5. Von Mises yield surface w
| : uniaxial yield stress at the w-configuration; that is to say corresponding to a given plastic deformation. The evolution of w | is going to be described by the hardening law. w : back-stress tensor at the w-configuration. In many metals subjected to cyclic loading it is experimentally observed that the center of the yield surface experiences a motion in the direction of the plastic flow; the backstress tensor describes this behavior (Mc Clintock & Argon 1966). The evolution of w is going to be described by the hardening law. We will show that w is a traceless tensor. In Fig. 5.5 we represent von Mises yield surface in the space of princital (over-)stresses. The von Mises yield surface in the stress space is a circular cylinder whose axis forms equal angles with each of the coordinates axes. When, later, we discuss Drucker’s definition of stable materials, we will show that for any stable material whose behavior is modeled using any yield surface, at every time during the yield surface evolution, this surface has to remain as a convex surface in the stress space. The flow rule As we stated at the beginning of the section, now we are focusing on the case of infinitesimal strains; hence, the starting point for describing the deformation of an elastoplastic solid during plastic loading is Eq. (5.38) which decomposes the material flow into the addition of an elastic flow plus a plastic flow.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
143
During the material plastic flow there is a plastic dissipation per unit volume of mechanical energy given by: w
D = w lm w gS lm
(5.57)
(Hill 1950, Lubliner 1990, Simo & Hughes 1998). If w dS = 0 (no plastic loading) w D = 0, otherwise the Second Law of Thermodynamics imposes that w D A 0. For many materials, such as metals, the plastic flow is developed so as to maximize the plastic dissipation. In mathematical form we can say that for defining the plastic loading we seek for the maximum of w D under the constraint w
i =0=
(5.58a)
DB = w D w ˙ w i
(5.58b)
We define (Luenberger 1984), w
where w ˙ is a Lagrange multiplier used to enforce the constraint in Eq. (5.58a). The conditions for w D to attain a maximum under the constraint in Eq. (5.58a) are, C w DB =0 C w lm
(5.59a)
C w DB =0= C w ˙
(5.59b)
The first of the above equations leads to w S glm
Cwi = w ˙ w lm C
(5.60)
and the second one to Eq. (5.58a). Note that i ? 0 =, w ˙ = 0 (elastic behavior ) > w i = 0 =, w ˙ A 0 (plastic loading) . w
The above equations can be summarized using the Kuhn-Tucker conditions for constrained optimization (Luenberger 1984), w˙ w
i =0> w˙ >0>
(5.61b)
i 60=
(5.61c)
w
(5.61a)
The Principle of Maximum Plastic Dissipation states that, for a given plastic strain rate w dS , among the possible stresses w satisfying the yield
144
Nonlinear continua
criterion, the plastic dissipation attains its maximum for the actual stress tensor (Simo & Hughes 1998). The flow described by Eqs. (5.60-5.61c) is called associative or associated plastic flow and presents many important properties that we will study in what follows. A general or nonassociated plastic flow is described by Yield function : Flow rule :
w
i =0
w S glm
(5.62a) w
C j = w ˙ w lm C
(5.62b)
where w j is called the plastic potential and is di erent from the yield function. JJJJJ Example 5.10. For a material model developed using the von Mises yield criterion in Eq. (5.55), we can write in a Cartesian coordinate system: ¢ ¡ C w i C w v C wi = = w v w w w w C C v C
=
Hence, in the case of associated plastic flow w S g
= w ˙
¡
w
v w
¢
=
Since w s and w are traceless tensors (see Eqs. (5.78) and (5.52)), it is obvious that, w S g = 0 > which is the condition of incompressible plastic flow (see Example 4.4). The above is, of course, a direct consequence of the fact that due to Bridgman experimental observations the yield function does not include the trace of w . JJJJJ Stable materials - Drucker’s postulate The principle of maximum plastic dissipation (associated plasticity) implies that the plastic flow develops in the direction of the yield surface external normal, Eq. (5.60). For an arbitrary yield function we schematize this normality rule in Fig.5.6. Note that in the case of infinitesimal strains, it was shown in = Eq. (5.24) that w d = w % ; which is the nomenclature used in Fig. 5.6. Let us assume an elasticplastic material that is initially at a stress state w , inside the elastic range. Let us also assume that an “external agent” (one that is independent of whatever has produced the current loads) slowly
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
145
applies an incremental load resulting in a stress/strain increment and then slowly removes it. For a stable material, the work performed by the external agent in the course of the cycle consisting of the application and removal of the external load is non-negative (Lubliner 1990).
Fig. 5.6. Normality rule in associated plasticity (maximum plastic dissipation)
The above is Drucker’s definition of a stable material, also known as Drucker’s postulate. In order to analyze the consequences of the above definition let us schematize the above defined cycle in Fig. 5.7. The total work per unit volume performed during the cycle 0-1-2-0 is, Z 1 Z 2 Z 0 ZW RW DO = lm d%lm + lm d%lm + lm d%lm (5.63a) 0
1
2
hence, the work performed by the external agent is, Z 1 Z 2 ¡ lm ¢ ¡ lm ¢ Zh=d = w lm d%lm + w lm d%lm 0
+
Z
2
1
0
¡ lm ¢ w lm d%lm =
For the small strains case, using Eq. (5.38) we obtain,
(5.63b)
146
Nonlinear continua
Fig. 5.7. Drucker’s postulate (work-hardening material)
Trajectory
d%lm
0-1
d%H lm
1-2
S d%H lm + d%lm
2-0
d%H lm
Taking into account that I
I
lm d%H lm = 0 w lm
d%H lm = 0
(5.63c) (5.63d)
we get, Zh=d =
Z
1
For a stable material
2
¡ lm ¢ w lm d%S lm =
Zh=d 0 =
(5.63e)
(5.63f)
The above requirement implies that the integrand in Eq. (5.63e) has to be non-negative, that is to say
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
147
Fig. 5.8. Convexity of the yield surface as a consequence of Drucker’s postulate
¡ lm ¢ w lm d%S lm 0 =
(5.63g)
We now specialize the above equation for the case in which point “2”is inside an infinitesimal neighborhood of “1”; hence, d lm d%S lm
0=
(5.63h)
The above constrain has already been derived for the 1D case, see Eq. (5.47). Equations (5.63g) and (5.63h) are two mathematical constraints that a stable material has to fulfill. We can rewrite Eq. (5.63h) as, w lm w S ˙ glm
0=
(5.64)
The above equation indicates that the plastic strain rate cannot oppose the stress rate (Lubliner 1990). Note that: w lm w S • While w ˙ lm w gS ˙ glm = 0 lm A 0 indicates a work-hardening material, indicates a perfectly plastic material. • Drucker’s postulate excludes from the range of stable materials the possibility of strain-softening materials. However, Drucker’s postulate has been obtained in the environment of stress - space plasticity, i.e. in our plasticity theory the stress is the independent variable. Since the 1960s strain - space plasticity formulations have been proposed even though their application has not been widespread yet (Lubliner 1990).
148
Nonlinear continua
As a consequence of Drucker’s postulate, we can show that for a stable material the yield surface has to be a convex surface in the stress space. It is obvious from the two cases schematized in Fig. 5.8 that the nonconvex one fails to fulfill Eq. (5.63g). Therefore, in the environment of stress-space plasticity, a stable material has to have a convex yield surface in the stress space.
Example 5.11. JJJJJ In this example we are going to show that a frictional material cannot be modeled using an associated plasticity formulation (Baˇzant 1979). Let us assume the simplest frictional material represented in the following figure: two rigid plates slide one on top of the other, and the sliding surface has a Coulomb friction coe!cient . We formulate a yield function in the stress space using W and Q (the modulus of T and N) as independent variables, w
when w i ? 0
i = W Q >
$ no sliding and when w i = 0
$ sliding.
The simplest frictional material The sliding is a nonreversible (plastic) deformation The elastic deformations are zero (rigid-plates hypothesis). In the following figure we draw the yield surface and the di erential plastic displacement obtained under the assumption of associated plasticity.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
149
Yield function and plastic deformation predicted using an associated plasticity formulation (simplest frictional material) The hypothesis of associated plasticity produces a nonphysical plastic displacement component in the N-direction (remember that the plates were assumed to be rigid). Therefore, to model frictional materials, it is necessary to use nonassociated plasticity formulations (Baˇzant 1979, Vermeer & de Borst 1984, Dvorkin, Cuitiño & Gioia 1989). JJJJJ Stress - strain relation Let us consider an elastoplastic material during the process of plastic loading, to relate the stress and strain increments. For the small-strains case in a Cartesian coordinate system Eq. (5.38) can be written as S d% = d%H + d% >
(5.65a)
therefore, for a linear elastic behavior, H d = F d%H =
(5.65b)
The fourth-order tensor CH is the material elastic constitutive tensor, it is constant for linear elastic behavior and it is a function of the total elastic strains for nonlinear elastic behavior. In this book we are not going to discuss the influence of the plastic deformations on the material elastic properties (damage theory (Lamaitre & Chaboche 1990)). From Eq. (5.60), for an associated plasticity formulation, d%S = d
C wi C w i C w v = d C w C w v C w
(5.66a)
150
Nonlinear continua
and using Eq. (5.55), the von Mises yield criterion,
also, from Eq. (5.50b),
¡ ¢ C wi = w v w > w C v
(5.66b)
1 C w v = = w C 3
(5.66c)
Taking into account that w s and w are traceless tensors, ¡w ¢ d%S v w = = d
(5.67a)
Using the above together with Eq. (5.65a) in Eq. (5.65b) we get ¡ £ ¢¤ H d = F d% d w v w = (5.67b)
During plastic loading d A 0 ; hence, using Eq. (5.61a), we get the consistency condition di = 0 (5.68a) which leads to,
Cwi Cwi d + d%S = 0 = C w C w %S
(5.68b)
Using the above, we get ¡w ¡ ¢ H £ ¢¤ v w F d% d w v w ¡ ¢ Cwi + w S d w v w = 0 = C %
(5.68c)
Hence,
d =
H d% ( w v w ) F H ( w v% w % ) F%& ( w v& w & )
Cwi C w %S %
( w v% w % )
= (5.68d)
Replacing in Eq. (5.67b) g with the above-derived value, we get "
H d = F
H H F* ( w v* w * ) ( w v w ) F H ( w v w ) F ( w v w )
Cwi C w %S
( w v w )
(5.69) 6 8 d% =
The term between brackets, w F HS , represents the Cartesian components of the continuum tangential elastoplastic constitutive tensor. Therefore, d = w CHS : d% = It is important to note that the following symmetries are present:
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
151
w
w HS F HS = F HS F = w F HS w HS F = w F HS
• • •
w
It is important to realize that the last symmetry is lost in the case of non-associated plastic models (see Eq. ( 5.62b)) (Baˇzant 1979, Vermeer & de Borst 1984). The hardening law Following Hill we can say that “The yield law for a given state of the metal must depend, in some complicated way, on the whole of the previous process of plastic deformation since the last annealing”(Hill 1950). In order to solve the equations that describe the elastoplastic deformation process, we have to describe the yield surface evolution during plastic deformation, that is to say, we have to describe the material hardening. The simplest hardening models are : • Isotropic hardening model. • Kinematic hardening model. While the first one does not describe the Bauschinger e ect (Hill 1950), the second one was developed to model the basic features of this e ect. In Fig. 5.9 we present a schematic description of the Bauschinger e ect. For an initially isotropic hardening material, after loading in tension to W | , when we unload, the yield stress is • •
W F
| when we reload in tension, | when we load in compression.
Isotropic hardening We assume that in Eq. (5.55) w
=0
(5.70a)
| = w | ( w Z S ) =
(5.70b)
and w
Hence, the yield surface remains centered and the yield stress is a function of the irreversible work performed on the solid (work hardening). In the above equation w Z S is the plastic work per unit volume performed on the material. We can state that, Gw Z S = (5.70c) Gw The total work per unit volume that has to be spent to deform a solid from its unstrained configuration to a configuration defined by w % is, assuming infinitesimal strains, w
D =
152
Nonlinear continua
Fig. 5.9. Bauschinger e ect
w
Z =
Z
w
%
d% =
(5.71a)
0
Using Eq. (5.65a), we get w
Z =
Z
0
w H %
d%H
+
Z
0
w S %
d%S =
(5.71b)
Note that we have not yet defined the upper limits of the above integrals. The first integral on the r.h.s. of Eq. (5.71b) is the elastic (reversible) work per unit volume while the second integral is the plastic (irreversible) work per unit volume. For an isotropic hardening von Mises material during plastic loading w
= w | ( w Z S ) > (5.72a) q where w : equivalent stress = 32 w s : w s . The rate of plastic work per unit volume is, considering that the plastic flow is incompressible: w ˙ S Z = w v w gS (5.72b) = We define, for the isotropic hardening von Mises material the equivalent plastic strain rate, r 2 w S w S w S g = d : d = (5.73a) 3
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
Hence, w
S
wg =
r ¡
´ ¢³ S w d : w dS : ws =
ws
153
(5.73b)
Using Eq. (5.60) we can see that w dS and w s are collinear tensors when isotropic von Mises plasticity is considered; hence, we can write Eq. (5.73b) as, w w S ˙S g = w s : w dS = w Z (5.73c) S
therefore w and w g are energy conjugate. We define the equivalent plastic strain as w S
% =
Z
w S
%
w S
g dw =
(5.74a)
0
Considering Eqs. (5.72a) and (5.73c) dZ S = w | ( w Z S ) d%S =
(5.74b)
C w | w C w | C w Z S C w | S S d% = d% = d%S = | CwZ S C w Z S C w %S C w %S
(5.74c)
Hence, d | =
Therefore, we can construct a curve, w
| = w |
¡w
%S
¢
=
(5.75)
“The assumption that one universal stress - strain curve of the form of Eq. (5.75) governs all possible combined - stress loadings of a given material is obviously a very strong one” (Malvern 1969). Example 5.12. JJJJJ In a uniaxial tensile test, before the necking is localized, with the I-axis the loading direction and the II and III - axes orthogonal ones, we can write w w w
L =
>
LL = 0
>
LLL = 0
>
2 > 3 1 w vLL = > 3 1 w vLLL = = 3 w
Hence, = = Also, due to incompressibility
vL =
154
Nonlinear continua w S %L w S %LL w S %LLL
= %S 1 = %S 2 1 = %S = 2
Hence, w S
% = %S =
Therefore, for an isotropic hardening von Mises material, the complete universal stress - strain curve is determined with only an uniaxial test. JJJJJ Kinematic hardening In this hardening model, which was developed to simulate the basic features of the Bauschinger e ect, we assume: w
| =
| = frqvw=
(5.76)
Kinematic hardening represents a translation of the yield surface in the stress space by shifting its center. This is in fairly good agreement with the Bauschinger e ect for those materials whose stress-strain curve in the workhardening range can be approximated by a straight line (“linear hardening”) (Lubliner 1990). Prager, in his kinematic hardening model, assumes a linear hardening (Malvern 1969): w ˙ lm = f w gS (5.77) lm where c is a constant. w Since w gS = 0 (incompressibility), the back-stress tensor is also traceless; that is to say w
: wg = 0 =
(5.78)
In the nine-dimensional stress space, the yield surface is displaced in the direction of its external normal at the load point. Example 5.13. JJJJJ We consider the 1D case of monotonic loading, also considered in the previous example. Considering the yield function in Eq. (5.55) under the constraints in Eqs. (5.76) and (5.77); and imposing that during loading w
we get,
i˙ = 0 >
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
155
·
f=
¯ · 3 % 2¯
=
Therefore, the hardening parameter, c, is constant for linear hardening materials. JJJJJ
When using the kinematic hardening model, as also discussed for the isotropic hardening model, the complete universal stress-strain curve is determined with one axial test. It is important to realize that the results for monotonic loading are exactly coincident when considering either the isotropic or the kinematic hardening models.
5.2.6 Elastoplastic material model under finite strains I Hypoelastic models Following what has been done for the case of elastoplastic materials under infinitesimal strains, we start this Section by assuming a hypoelastic description of the deformation process. Referring the problem to the equilibrium configuration at time t, we may again use w d = w dH + w dS = (5.79) As we have shown in Example 2.22, w d is an objective strain rate; therefore, considering Eq. (5.79), both w dH and w dS have to be considered as objective strain rates too. Hence, we can extend the constitutive laws used for infinitesimal strains and write
w
= w cH : w dH
w S
·
d = ws =
(5.80a) (5.80b)
In the above equation w is an objective stress rate such as the Oldroyd stress rate (see Sect. 3.4) and w cH is the spatial elasticity tensor. Equation (5.80a) is the hypoelastic expression of an elastic behavior and we expect it to conserve energy; that is to say, it has to be the hypoelastic expression of a hyperelastic material behavior.
156
Nonlinear continua
In the next example we show that only for the case of infinitesimal strains, it is valid to assume that w cH is a constant and isotropic tensor.
Example 5.14. JJJJJ Following (Simo & Pister 1984) we will show that the hypoelastic equation w
lm
= w flmno w gno
fails to model a hyperelastic behavior when the fourth-order constitutive tensor is constant and isotropic (see also Example 5.6). (a) Calculation of w ˙ lm Using Eq. (3.35), we get w
= w ˙ w l · w w · w lW =
Also, using the definition of the second Piola-Kirchho stress tensor, we can write w = w M 1 w X · w S · w XW > (A)
where w M = w . Using the result in Example 5.3, we can write ¡w ¢ w w S = S C = From Eq. (A) w
M˙ w X · M2
w
˙ = w
+ w M 1 + w M 1
¡w ¢ w W w 1 w l · C · X + M ¡ ¢ · Cw S w C w · w C · w XW X · w C C ¡w ¢ w W w w · w lW = X · S C · X w S
w X
·
w S
¡w ¢ C ·
w W X
Also, w npst
f
= 2 M 1 w [ nN w [ pP w [ sS w [ tT
Using Example 4.1 we can write
w
·
M =
w
C w V NP = C w FS T
M (u · w v) =
w
M
(5.81) ³
w
d : wg
´
and taking into account that w j de |l = 0 , after same algebra, we get, using components, the equation (Truesdell & Noll 1965)
5.2 Constitutive relations in solid mechanics: purely mechanical formulations w np
˙
w npst
k
= w knpst w ost
157
(B.1)
= w np w j st + w j ns w tp + w fnpst + w nt w j ps =
(B.2)
In the derivation of the above equation we made use of the symmetry condition w npst f = w fnpts . (b) The Bernstein formula Following (Truesdell & Noll 1965) we now present the conditions that w knpst in Eqs. (B.1-B.2) needs to fulfill in order to model a hyperelastic material behavior. For a hyperelastic material behavior, we can write, using Eq. (5.4e), w lm
= 2 w
Cwu > C w jlm
where w u is the elastic energy per unit mass. We can also write the following functional dependence, ¡ d¢ w np = *np w [D =
(C)
Hence,
w np
˙
=
C*np w d w e d o e [D = Cw [D
Therefore, using the above and Eq. (B.1), we get C*np w d w e w npst w ost > d o e [D = k Cw [D and after some algebra C*np w np s s = k Cw [D
t
¡w
[
¢ 1 D t
=
(D)
The above is written in (Truesdell & Noll 1965) as Eq. (100.24). The function *np has to fulfill the following condition to be a potential function, C 2 *np C 2 *np = w u w s = u w C [E C [E C [D
s Cw [D
(E)
Using in Eq. (E) the equality (D) and considering that (Truesdell & Toupin 1960) the equation
158
Nonlinear continua
¡w
[
leads to C
¡w
¢ 1 E t w [s D
[
C
¢ 1 E w [ tP t =
we finally get the Bernstein formula:
¡w
[
= E P ¢ 1 E s
(5.82)
¡w
[
¢ 1 D t
C w knpst w uvmo C w knpmo w uvst k w uv k w knpso w j mt + w knpmt w j so = 0 = C w uv C
(5.83)
(F)
(c) The constant and isotropic constitutive tensor Finally, we are going to show that when using a constant and isotropic constitutive tensor in Eq. (5.80a), the Bernstein formula is not fulfilled and therefore, a hyperelastic material behavior cannot be modeled. A general constant isotropic tensor is written as (Aris 1962) ¡ ¢ w npmo f = w j np w j mo + w j nm w j po + w j no w j pm then we replace in Eq. (F) and we find that the equality can be satisfied only for ( + ) = 0 . Since this constraint on the material properties does not correspond to a physical acceptable material model, we conclude that it is not possible to use a constant and isotropic constitutive tensor in Eq. (5.80a) to model a hyperelastic material behavior. JJJJJ
I The multiplicative decomposition of the deformation gradient The use of hypoelastic models to numerically analyze finite strains elastoplastic problems leads to many di!culties: • The strain- and stress-rate measures have to be both objective and incrementally objective (i.e. % and have to be objective tensors). As we have shown in Sect. 3.4 the Jaumann stress-rate, which is an objective stress-rate measure, is not suitable for producing an objective incremental stress measure. • The limitation discussed in Example 5.14 to represent an elastic behavior using a hypoelastic constitutive model. An alternative kinematic formulation to numerically analyze finite-strain elastoplastic problems can be found in (Lee & Liu 1967, Lee 1969). Lee’s kinematic formulation: the multiplicative decomposition of the deformation gradient, is based on a micromechanical model of single-crystal metal plasticity (Simo & Hughes 1998).
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
159
Lee’s multiplicative decomposition of the deformation gradient has been the basis of the hyperelastic model for finite-strain elastoplasticity developed by Simo and Ortiz (Simo & Ortiz 1985, Simo 1988, Simo & Hughes 1998). We will now present an “intuitive description” of Lee’s multiplicative decomposition of the deformation gradient (Lubliner 1990). Let us consider a reference configuration that we assume to be unstressed and unstrained and the spatial configuration corresponding to a certain time “t”. In this spatial configuration, we have reversible (elastic) deformations and permanent (plastic) deformations. If we now cut the spatial configuration into hexahedric infinitesimal volumes and if we assume for each of those volumes an elastic unloading process, we obtain a stress-free configuration that is called the intermediate configuration. Obviously, the infinitesimal hexahedrals will not match together in the stress free or intermediate configuration to form a continuum because compatibility was lost when we divided the spatial continuum into infinitesimal parts. Therefore, the intermediate configuration is not a proper configuration because there is not a bijective mapping between the material particles and 1] is the hardening ratio; = 0 corresponds to purely kinematic hardening and = 1 corresponds to purely isotropic hardening. We also define the equivalent plastic strain as: Z w w S w ¯S h¯ = (5.94) g dw = w
0
I Energy dissipation We now introduce w # as the free energy at the spatial configuration per unit volume of the reference configuration. Considering that the mechanical problem is uncoupled from the thermal problem, we can write (Simo & Hughes 1998) w
: w d w #˙ > 0 =
(5.95a)
The above equation, known as the Clausius-Duhem inequality, is a restriction imposed by the Second Law of Thermodynamics (Simo & Hughes 1998): • For the elastic case the deformation is reversible and the equal sign holds. • When there are plastic deformations the process is irreversible and the greater-than sign holds.
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
163
Therefore, using Lee’s multiplicative decomposition, we can write w S [
=
$
w
: w d w #˙ = 0
(5.95b)
w S [
6=
$
w
: w d w #˙ A 0 =
(5.95c)
For the free energy of the purely mechanical problem, we can state the following functional relation: ³ ´ w # = w # w HH > w | > w B = (5.96a) Following Simo 1988, we use the following uncoupled expression for the free energy, ³ ´ ¡ ¢ w # = w # h w HH + w # s w | > w B = (5.96b)
Considering a metal, w # h is the elastic free energy that we identify with the atomic lattice deformation energy and w # s is the energy associated with atomic lattice defects (e.g. dislocations) (Lubliner 1990). From Eq. (5.85b), l = w lH + w lS ³ ´1 w H ˙ H · w XH l = w X = w dH + w $ H w
w S
l =
S · w¯l ·
w H X
Therefore, w
³
w H X
: wd = w :
³
´1
w H
d
(5.97a) (5.97b)
= w dS + w $ S =
(5.97c)
´
(5.98)
+ w dS
=
After some algebra, we can write ³ ³ ´W ´W ¸ S w w S w H w w H : d = · · X : w¯l = X
(5.99)
Since we restrict this formulation to the case of isotropic elastic properties, we can write (see Sect. 3.3.4) w
: w dH = w :
w ˙ H H
(5.100)
and the Clausius-Duhem inequality takes the form, Ã
w
C w #h Cw HH
!
:
w ˙ H H
+
³
w H X
´W
· w ·
³
w H X
´W ¸
S : w¯l w #˙ s > 0 =
(5.101) Since the above must also be valid for the case of an elastic deformation, we obtain
164
Nonlinear continua w
C w #h = Cw HH
=
We define as dissipation (Simo 1988): ³ ³ ´W ´W ¸ S w D = w XH · w · w XH : w¯l w #˙ s > 0 =
(5.102)
(5.103)
Considering that: • For elastically isotropic materials the tensors w , w HH and therefore w H are collinear. U • The contraction of a symmetric tensor with a skew-symmetric one is zero. We get, w
¯S w #˙ s > 0 = D = w : wd
(5.104)
We search for the value of w that maximizes the dissipation under the unilateral constraint w i 6 0 . For the case w i ? 0 (elastic loading or unloading) w ¯S
d =0=
(5.105)
For the case w i = 0 (plastic loading) to solve the minimization problem, we use the Kuhn-Tucker conditions (Luenberger 1984) and we obtain the well-known associated flow rule (see Eqs. (5.57) to (5.61c) for the case of infinitesimal strains): ³ ´ 3 w G w B 2 S w¯ (5.106a) d = w ˙ r ³ ´ ³ ´ 3 w wB : w wB 2 G G where from w
we obtain
w˙
·S
¯% =
r
2 w ¯S w ¯S d :d = 3
(5.106b)
·S
= w¯% .
I The incremental formulation If we assume a conservative loading and a fixed intermediate configuration, in order to satisfy the equilibrium equations at time (load level) w + 4w we have to fulfill the Principle of Minimum Potential Energy (see Chap. 6): ³ ´ w+4w H w+4w H =0 (5.107)
5.2 Constitutive relations in solid mechanics: purely mechanical formulations
165
where w+4w is the potential energy corresponding to the w + 4w configu ration. From Chap. 6, Eq. (6.51), we can write Z w+4w w+4w = U dY + w+4w j (5.108a) Y
where Y : volume of the reference configuration; w+4w U : elastic energy per unit mass stored in the (w + 4w)-configuration; and, w+4w j : potential of the external loads acting on the (w + 4w)-configuration. Using the elastic free energy defined in Eq. (5.96b), we can write w+4w
=
Z
w+4w
Y
# h dY +
w+4w
j=
(5.108b)
Equation (5.107) together with the above leads to Z
w+4w
:
Y
+
³
w+4w H H
Z
´
w+4w
w+4w V
dY =
f v · u
Z
w+4w w+4w Y
w+4w
f e · u
w+4w
dY
(5.108c)
dV =
In the above equation: Y : volume of the spatial configuration, w+4w V : external surface of the spatial configuration, w+4w f e : body forces per unit volume, acting on the (w + 4w)-configuration, w+4w f v : surface forces acting on the (w + 4w)-configuration, u : displacement from w to (w + 4w). w+4w
Also, w+4w HH =
Cw+4w HH Cw+4w H
: w+4w H=
For the calculation of the fourth-order tensor
Cw+4w HH Cw+4w H
(5.109a) , we follow the
appendix in (Dvorkin, Pantuso & Repetto 1994) and we get Cw K HLM Cw K HLM Cw F HP Q Cw FUV = = Cw KNO Cw F HPQ Cw FUV Cw KNO
(5.110a)
To calculate the derivative in the first factor on the r.h.s. of the above equation, we use q w H w CH (5.110b) H = ln
166
Nonlinear continua
being WL = [L > L > L ] (L = 1> 2> 3) the 3 eigenvectors of 3 eigenvalues
w H C
and L its
H H H Cw KLM Cw KLM CN C N Cw KLM = + H H H CN Cw FPQ C N Cw FPQ Cw FPQ
+
H H Cw KLM Cw KLM C N CN + = H H w w C N C FPQ CN C FPQ
(5.110c)
To calculate the derivative in the second factor on the r.h.s. of Eq. (5.110a), we use ³ ³ ´W ´1 w H w S · w C · w XS > (5.110d) C = X
and to calculate the derivative in the third factor we use q w wC > H = ln
(5.110e)
and proceed as in Eq. (5.110c) but using the eigenvectors and eigenvalues of
w C.
For the elastic deformation, we use w+4w
= CH :
w+4w H H
>
(5.111)
where CH is a constant and isotropic elasticity tensor (Hooke’s law). The main aspects of the finite strain elastoplastic formulation that we presented in this Section are: • We use Lee’s multiplicative decomposition of the deformation gradient. • We use a hyperelastic constitutive relation for the elastic strains/stress relation; that is to say, we relate total strains with total stresses. • We describe the plastic flow using the maximum dissipation principle (associated plasticity). • We use the total Hencky strain as our strain measure. The reason for this choice is that according to the experimental data reported in (Anand 1979), “the classical strain energy function of infinitesimal isotropic elasticity is in good agreement with experiment for a wide class of materials for moderately large deformations, provided the infinitesimal strain measure occurring in the strain energy function is replaced by the Hencky or logarithmic measure of finite strain”. From a numerical viewpoint, an additional advantage in using the Hencky strain measure is that the first invariant of the logarithmic strain tensor is the logarithmic volume strain; therefore many techniques developed for handling incompressibility in the infinitesimal strain problem can be carried over for the finite strain problem. We discussed the above formulation, the “total Lagrangian - Hencky formulation” and its finite element implementation in (Dvorkin 1995a\1995b\1995c, Dvorkin & Assanelli 2000, Dvorkin, Pantuso & Repetto 1992\1993\1994\1995).
5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations
167
5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations 5.3.1 The isotropic thermoelastic constitutive model Considering a hyperelastic solid under mechanical loads and thermal evolution, the two point variables that define the state of the solid at any instant are a strain measure and the temperature. Therefore, the stresses at any point in the solid are a function of the strains and temperature at that point (local action). Using, for example, the Green-Lagrange strain tensor; and w W being the temperature, we can write for any particle in the spatial configuration its internal energy per unit mass (elastic energy + caloric energy) as ¡ ¢ w U = w U w %>w W (5.112a)
and considering a reversible process (Boley & Weiner 1960), we can write w
= w
w
¡w
w %>
W
¢
(5.112b)
where is the spatial entropy per unit mass. The principle of energy conservation (First Law of Thermodynamics) can be written as Gw U 1 (5.113) = w S : w %˙ + w W w ˙ = Gw We can define Helmholtz’s free energy per unit mass, (Boley & Weiner 1960, Malvern 1969) as: ¡ ¢ ¡ ¢ w # w %>w W = w U w %>w W w W w = (5.114a) Using the above and Eq. (5.113), we get µ
Cw# 1 w V LM Cw %LM
¶
w ˙ LM %
+
µ
Cw# + w CwW
¶
w
W˙ = 0 =
(5.114b)
Hence considering the isothermal ( w W˙ = 0 ) and isometric ( w %˙ LM = 0 ) cases, we have Cw# Cw %LM Cw# w = w = C W
w LM V
=
(5.114c) (5.114d)
In a hyperelastic material the stresses and entropy are a function of the strain/temperature value at the point and not of its history; then, the above equations are valid for any process.
168
Nonlinear continua
Since the free energy, w # , is invariant under changes of reference frame, for an isotropic material, it can only depend on the invariants of w % , which for the t-configuration, and considering the strain tensor Cartesian components, are w L1
=
w %
(5.115a)
1 w 1 ¡w ¢2 w L1 % % 2 2 1 w h h w % w % w % = L3 = 6 w L2
=
Hence, w
# = w#
¡w
w w w L1 > L2 > L3 > W
¢
=
(5.115b) (5.115c)
(5.116)
The most general expression for the free energy is w
¡ ¢ ¡ ¢2 # = d0 + d1 w L1 + d2 w L2 + d3 w L3 + d4 w W WU + d5 w W WU ¡ ¢ ¡ ¢ ¡ ¢ + d6 w L1 w W WU + d7 w L2 w W WU + d8 w L3 w W WU ¡ ¢2 + d9 w L1 + = = = = (5.117)
In the above equation WU is the reference temperature, usually the temperature of the undeformed solid. Using Eq. (5.114c), we get w V
=
C w # Cw Ll > Cw Ll Cw %
(5.118a)
where Cw L1 = > Cw % Cw L2 = Cw %
w %
(5.118b)
w L1
>
1 Cw L3 = h h w % w % = w C % 6
(5.118c) (5.118d)
Physical restrictions used to determine the material constants: •
w % = 0 wW = W U
=,
w V
= 0 ; hence, d1 = 0.
• For the above condition, we set an arbitrary value for the free energy; hence, we set d0 = 0. • Doing the same consideration for the entropy, we set d4 = 0.
5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations
169
I Specialization for small strains and small temperature increments In this case:
w w % $ % wV w $
(infinitesimal strain tensor ) (Cauchy stress tensor ) . Using Eq. (5.114c) and (5.117) and neglecting higher-order terms in w % and (w W WU ) > we get, for an isotropic material (Malvern 1969), w
= w % + 2 J w %
¢ ¡w H W WU (1 2)
(5.119)
H ; where H : Young’s modulus; : Poisson’s ratio; J : shear modulus, J = 2(1+) H = (12)(1+) ; and, : linear coe!cient of thermal expansion. For an isotropic solid with constant and uniform material properties, in the absence of volumetric heat generation or consumption, the heat conduction equation is (Boley & Weiner 1960):
n u2 w W =
w W w ˙
(5.120)
where n is the heat conduction coe!cient of the material (Fourier’s law). The above equation together with Eq. (5.114d) leads to, ¸ C2 w# w C2 w# w ˙ 2 w w n u W = W %˙ + w 2 W = (5.121) C w W C w % C W The specific heat of the material is defined as: w
f=
CwU CwW
(5.122)
and after some algebra,
Cw = CwW Using Eqs. (5.114c) and (5.114d) in (5.121), we get µw ¶ w C Cw %˙ + w W w w W˙ = n u2w W = w W w C W C W w
f = wW
(5.123)
(5.124)
And using Eqs. (5.119) and (5.123) in (5.124), we get n u2w W =
w
W H w %˙ + (1 2)
w f w W˙ =
(5.125)
Equations (5.119) and (5.125) show that in the most general case of thermoelastic materials the heat transfer and stress analysis problems are coupled. However, in most engineering applications the first term on the r.h.s. of Eq. (5.125) can be neglected.
170
Nonlinear continua
In (Boley & Weiner 1960) numerical examples in aluminum and steel were considered and it was shown that the coupling is negligible when w
%˙ ¿ 20 = 3 w W˙
(5.126)
5.3.2 A thermoelastoplastic constitutive model In Sect. 5.2.5 we developed the constitutive relation for an elastoplastic material under infinitesimal strains; in that section we made the assumption of a purely mechanical formulation, now we shall remove that limitation incorporating thermal e ects. However, we will keep the other assumptions made in that section: infinitesimal strains, limit loading condition (yield criterion), rate-independent behavior, stable material, etc. Since we have to take into account the thermal strains, we rewrite Eq. (5.38) as: w d = w dH + w dS + w dW K = (5.127) For the yield condition, we rewrite Eq. (5.48) as: ¡ ¢ w i w > w tl l = 1> q > w W = 0 =
(5.128)
Considering that we are focusing on the behavior of metals, we will keep on using the von Mises yield criterion and therefore in the case of isotropic hardening, we can rewrite Eq. (5.55) as: w
i=
w 2 | 1 w s : ws =0 2 3
(5.129a)
¢ ¡ where w | = w | w¯%S > w W . In the case of kinematic hardening we can rewrite Eq. (5.55) as (Snyder 1980): w 2 ¢ ¡ ¢ | 1 ¡w w i= s w : ws w (5.129b) 2 3 Rw . where w | = w | ( w W ); w lm = ˙ lm g ; and, w ˙ lm = w f (w W ) w gS lm
For the unstressed state with no previously accumulated plastic strains (Boley & Weiner 1960) w i (0> 0>w W ) ? 0 = (5.130) During plastic loading the consistency equation takes the form (Boley & Weiner 1960), Cwi Cwi w ˙ Cwi W =0= i˙ = w lm v˙ lm + w S w gS lm + Cv CwW C %lm
(5.131)
Following (Boley & Weiner 1960) we will study three possible cases:
5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations
171
(a) Cwi C w i w lm v˙ + w w W˙ = 0 = (5.132a) w lm C v C W Using the above equation together with Eq. (5.131), we see that it is possible for the stress components and the temperature to change so that the point remains on the yield surface but without further plasticity development. ¡ ¢ Therefore this change is called neutral w gS lm = 0 . (b)
Cwi C w i w lm v˙ + w w W˙ ? 0 = w lm C v C W The above equation represents an unloading and therefore
(5.132b) w S glm
= 0.
(c) Cwi C w i w lm (5.132c) v˙ + w w W˙ A 0 = w lm C v C W The above equation represents a condition of plastic loading and using Eq.(5.131), we get w gS lm . I Stress - strain - temperature relation As we did above for the case of isothermal plasticity we consider that the plastic flow maximizes the plastic dissipation (Lubliner 1985). We again define the plastic dissipation via Eq. (5.57) and imposing during plastic loading the condition w i = 0 we obtain, in a general curvilinear system, w ¸ Cwi C i lm w S w˙ lm d glm = d + w dW = (5.133) C w lm C W Considering Eq. (5.132c) and since w ˙ > 0> we get for plastic loading the condition w lm w S ˙ glm A 0 > (5.134)
which is the same stability condition already obtained for the isothermal case (Drucker’s postulate). Again, we obtain the convexity condition for the yield surface in the stress space. From Eq. (5.133), ¸ Cwi Cwi w S glm w ˙ w lm d lm + w dW = 0 = (5.135) C CW Hence, the normality rule already developed for the isothermal case applies:
172
Nonlinear continua w S glm
Cwi = w ˙ w lm = C
(5.136)
Stress - strain relations for the case of isotropic hardening Since we are considering the case of infinitesimal strains, we can write in a Cartesian system, S WK d% = d%H + d% + d%
(5.137a)
and w
H w H = w F % =
(5.137b)
We consider an isotropic linear elastic material with elastic constants function of the temperature; therefore (Snyder 1980), H d%H d = w F +
H C w F w H % dW = CwW
(5.138)
Hence, H £ ¤ C w F H WK w H d% % dW = (5.139a) d = w F d% d%S + CwW
For a von Mises material,
w d%S = d v
(5.139b)
and for an isotropic thermal expansion, d%WK = w dW =
(5.139c)
During plastic loading gi = 0 and using Eq. (5.131), Cwi Cwi Cwi S d + d¯ % + dW = 0 = S C w CwW C w¯%
(5.140)
Developing each of the terms in the above equation, we obtain ¡ ¢ Cwi H d = w v [ w F d% d w v w dW w C H C w F CwW Cwi 4 d¯%S = w 2| S w C ¯% 9 Cwi 2 dW = w | CwW 3
+
therefore (Snyder 1980),
w H %
dW ]
(5.141a)
w
C | d C w ¯%S C w | dW > CwW
(5.141b) (5.141c)
5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations w
d =
H C w F w H % dW ] Cw W 4 w 2 C w | wv w w H F v + 9 | C w ¯ %S
H v [ w F (d% w dW ) +
C w | 2 w 3 | Cw W
173
dW
(5.142) Hence, we introduce the above in Eqs. (5.139a-5.139c) and we can inmediately relate increments in strains/temperature with stress increments. In order to be able ³ w ´ ³ w to ´evaluate the terms in Eq. (5.142) it is necessary to C C | relate C w ¯%S| and to the actual material behavior (Snyder 1980). CwW From the data obtained in isothermal tensile tests of virgin samples, we can develop the idealized bilinear stress-strain curves shown in Fig. 5.11.
Fig. 5.11. Stress-strain curves at di erent temperatures, Wl
For a constant temperature curve, we can write µ ¶ ¸ | w w | = ( | )W + % (Hw )W H W w | w % = w %S + = (H)W
(5.143a) (5.143b)
Therefore, w
| = ( | )W + w %S
(H Hw )W = (H Hw )W
(5.143c)
=
174
Nonlinear continua
Using, as in the isothermal case, the concept of a universal stress-strain curve that is valid for any multiaxial stress-strain state, we can use Eq. (5.143c) for any stress - strain state, provided that w %S is replaced by w¯%S (Eq. (5.74a)). Hence, in Eq. (5.142), we have ¶ µ H Hw C w | = (5.144a) C w ¯%S H Hw W ¶¸ µ ¶ µ C C w | C | H Hw w S + ¯% = (5.144b) = CwW CwW W C w W H Hw W Hence, we can rewrite Eq. (5.142) as: w
d =
2 3
CwFH
w H H F (d% w dW ) + C w % dW W ³ ´ H Hw 4 w 2 w wv w H F v + 9 | H Hw W h³ ´ ³ ³ ´´ i C | w | + w ¯%S CCw W HHHHw w dW CwW W ³ ´W = H Hw 4 w 2 w H wv w F v + 9 | H Hw
v
w
¸
(5.145)
W
In the above equation, we consider a linear isotropic elastic model; therefore using Eqs. (5.15) and (5.16), we get w
H F = ()W + (J)W ( + )
(5.146)
and taking into account that w v = 0, we get w
H v w F = 2 (J)W
w
v =
(5.147)
Taking into account that (Snyder 1980) ³´ h ¡ ¢1 i 1 w = + ( + ) FH H W 4 (J)W
(5.148)
we can show that w
v
µ ¶¸ H C w F 1 CJ w H % = CwW J CwW W
w
v w =
(5.149)
Hence,
d =
¡1
¢
CJ w w J CW W v v ³ ´ H Hw 4 w )2 + 4 w 2 (J) ( | | W 3 9 HHw W
2 (J)W
2 w 3 |
w
h³
4 3
v d% +
C 0 | CW
´
W
+ w %S 2
(J)W (w | ) +
³
C CwW
4 w 2 9 |
³
H Hw HHw
³
H Hw HHw
dW
´´ i ´
W
W
dW =
(5.150)
5.3 Constitutive relations in solid mechanics: thermoelastoplastic formulations
175
Stress - strain relations for the case of kinematic hardening We use the kinematic hardening results in Section 5.2.5 and adapt them for the case of nonisothermal processes,
w
w
w
¢ ¡ ¢ 1 ¡w 1 w 2 v w w v w =0 2 3 | ¡ ¢ = w | w W
i =
|
=
Zw
w
˙ dw
(5.151a) (5.151b) (5.151c)
0
w
w
˙ = f w gS ¡ ¢ w f = wf wW =
(5.151d) (5.151e)
During the plastic loading Cwi Cwi Cwi g + w g + w g | = 0 = w C C C |
(5.152)
Developing each of the terms in the above equation, we obtain ¡ ¢ Cwi d = w v w (5.153a) w C ( ) H ¡w £ ¢ ¤ C w F* w H w w w H F* d%* d v* * dW * + %* dW CW ¡ ¡ ¢ ¢ Cwi 2 d = w v w w f d w v w = w f d w 2| C w 3 (5.153b) 2 C w | Cwi d | = w | w dW w C | 3 C W
(5.153c)
therefore (Snyder 1980), ( w v w ) d =
w
H F* (d%* w dW * ) +
H C w F* w H %* CW
H ( w v w ) w F# ( w v# w # ) +
( w v w )
C w | 2 w 3 | C w W dW wF H w w # ( v# # )
+
2 w w 2 3 f |
2 w w 2 3 f |
dW
¸
(5.154)
176
Nonlinear continua
Again, as in the case of isotropic hardening, we relate the above expression to the actual material behavior using the information contained in the isothermal uniaxial stress-strain curves. For an isothermal loading in a bi-linear material, we can use the result in Example 5.13 and obtain, ¶ µ 2 H Hw w f(W ) = = (5.155) 3 H Hw W
5.4 Viscoplasticity In Sects. 5.2 and 5.3, we discussed constitutive relations that have a common feature: the response of the solids is instantaneous; that is to say, when a load is applied, either a mechanical or a thermal load, the solid instantaneously develops the corresponding displacements and strains. We know, from our experience, that this is not the case in many situations; e.g. a metallic structure under elevated temperature increases its deformation with time; a concrete structure in the first few months after it has been cast increases its deformation with time, etc. There is also an important experimental observation related to the response of materials, in particular metals, to rapid loads: the apparent yield stress increases with the deformation velocity. In the previous sections, when considering instantaneous plasticity, we represented the strain hardening of metals with equations of the form: | = | (%> W ) =
(5.156)
To take into account the above commented experimental observation, the yield stress has to present the following functional dependence (Backofen 1972): ˙ W) = | = | (%> %>
(5.157)
We can say that the strain-rate e ect shown in Eq.(5.157) is a viscous e ect. There are basically two ways in which a viscous e ect can enter a solid’s constitutive relation: • In the viscoelastic constitutive relations, the elastic part of the solid deformation presents viscous e ects. In this book, we are not going to discuss this kind of constitutive relations and we refer the readers to (Pipkin 1972) for a detailed discussion. • In the viscoplastic constitutive relations (Perzyna 1966), the permanent deformation presents viscous e ects. The examples we discussed above are described using viscoplastic constitutive relations and also, other important problems like metal-forming processes are very well described using this constitutive theory (Zienkiewicz, Jain & Oñate 1977, Kobayashi, Oh & Altan 1989).
5.4 Viscoplasticity
177
As in the case of elastoplasticity, we can divide the total strain rate into its elastic and viscoplastic parts; hence, we get an equation equivalent to Eq. (5.38), but now for an elastoviscoplastic solid: w
d = w dH + w dY S
(5.158)
where, w dY S is the viscoplastic strain rate tensor. In some cases, for example when modeling bulk metal-forming processes (Zienkiewicz, Jain & Oñate 1977), w dH ?? w dY S . Therefore, we can set w H d = 0, introducing a very important simplification in the model without any significant loss in accuracy; these are the rigid-viscoplastic material models. I The yield surface As in the case of plasticity, a yield surface is defined in the stress space with an equation identical to Eq. (5.48): w
i (w > w tl l = 1> q) = 0 =
(5.159)
The internal variables w tl indicate that in the viscoplastic case, the yield surface is also modified in its shape and/or position by the hardening phenomenon. In the case of elastoplastic material models, we remember that Eqs. (5.49a5.49b) established that in the stress space every point in the solid is either inside the yield surface ( w i ? 0 and therefore the behavior is elastic and w S d = 0 ) or on the yield surface ( w i = 0 and therefore the behavior is elastoplastic and permanent deformations are generated with w dS 6= 0). In the viscoplastic theory, the point can be either inside the yield surface ( w i ? 0 and therefore w dY S = 0) or outside the yield surface ( w i A 0 and in this case w dY S 6= 0 ). I The flow rule In a Cartesian system, for viscoplastic materials, we use the following flow rule (Perzyna 1966): w YS g
=
C w i ¡w ¢® = ! i C w
(5.160)
In the above equation, we use the Macauley brackets defined by: hdi = d hdi = 0
li d A 0 li d 0 =
(5.161a) (5.161b)
178
Nonlinear continua
An important di erence between the flow rate for the viscoplastic constitutive model (Eq. (5.160)) and the flow rate for the plastic constitutive model (Eq. (5.60)) is that in the present case, the fluidity parameter is a material constant, while in the plasticity theory w ˙ is a flow constant, derived by imposing the consistency condition during the plastic loading. Obviously, the correct value of and the correct expression for ! (w i ) are derived from experimental observations. In what follows we will concentrate on the details of a rigid-viscoplastic relation suited for describing the behavior of metals with isotropic hardening, "µ
w
!( i ) =
1w v w v 2
¶ 12
w
| s 3
#
·
(5.162)
In the above equation the term between brackets is the von Mises yield function. Using the definition of the second invariant of the deviatoric Cauchy stresses we get, ¯ 1 Ci ¯¯ w = s v (5.163) C ¯w 2 w M2
hence, using Eq.(5.160), we get w YS g
® = sw w v w i · 2 M2
(5.164)
The above equation indicates that with the selected yield function the resulting viscoplastic flow is incompressible; a result that matches the experimental observations performed on the viscoplastic flow of metals. Using the definition of equivalent viscoplastic strain associated to the von Mises yield function, Eq. (5.73a), we have w ® %Y S = s i · 3
w˙
Therefore, for w i 0
¡w ¢ i =
s 3 w˙ %Y S ·
(5.165)
(5.166)
Formulating, for a rigid-viscoplastic material model, the relation among deviatoric stresses and strains as, w
v = 2w w gYS
(5.167)
and using the above equations we get, for w i 0 w
w
=
s| 3
s ¸ 1 · + 3 w %Y S s · 3 w %˙ Y S
(5.168)
5.4 Viscoplasticity
179
From Eqs. (5.167) and (5.168) we see that a rigid-viscoplastic material behaves as a non-Newtonian fluid. It comes as no surprise that the solid behaves in a “fluid way”, since we have neglected the solid elastic behavior and therefore its memory; the material memory is the main di erence between the behavior of solids and fluids. In the limit, when $ 4 Eq. (5.168) describes the behavior of a rigidplastic material (inviscid), in this case, w
w
=
3
| w% ˙Y S
·
(5.169)
JJJJJ Example 5.16. An important experimentally observed e ect, that the viscoplastic material model explains, is the increase in the apparent yield stress of metals when the strain rate is increased (Malvern 1969) (strain-rate e ect). Let us assume a uniaxial test in a rigid-viscoplastic bar,
Therefore,
11 = b 22 = 33 = 0 · v11 =
2 b 3
1 v22 = v33 = b· 3
Also, for the viscoplastic strain rates we can write, ·
gY11S = % 1 gY22S = gY33S = %˙ · 2 Hence, the equivalent viscoplastic strain rate is, ·
%Y S = %˙ = Using Eqs. (5.167) and (5.168) together with the above we get, Ã s !1@ s 3 = b = | + 3 %˙
In the above equation, | is the bar yield stress obtained with a quasistatic test and b is the apparent yield stress obtained with a dynamic test. When $ 4(inviscid plasticity), the strain-rate e ect vanishes. Using other functions in Eq. (5.162) more complicated strain-rate dependences can be explained (Backofen 1972). JJJJJ
180
Nonlinear continua
In (Zienkiewicz, Jain & Oñate 1977) a finite element methodology, based on a rigid-viscoplastic constitutive relation was developed, for analyzing bulk metal-forming processes. This methodology known as the flow formulation has been widely used since then for analyzing many industrial processes (Dvorkin, Cavaliere & Goldschmit 2003, Cavaliere, Goldschmit & Dvorkin 2001a\2001b, Dvorkin 2001, Dvorkin, Cavaliere & Goldschmit 1995\1997\1998, Dvorkin & Petöcz 1993).
5.5 Newtonian fluids We define as an ideal or Newtonian fluid flow a viscous and incompressible one. The first property of a Newtonian fluid is the lack of memory: Newtonian fluids do not present an elastic behavior and they do not store elastic energy. Regarding the incompressible behavior we can write the continuity equation, using the result of Example 4.4 as, u · wv = 0 ·
(5.170)
It is important to remark that even though there are some fluids that can be considered as incompressible, most of the cases of interest in engineering practice are flows where Eq. (5.170) is valid even though the fluids are not necessarily incompressible in all situations (e.g. isothermal air flow at low Mach numbers) (Panton 1984). The constitutive relation for the Newtonian fluids can be written in the spatial configuration as, w
= w s w g + 2 w d =
(5.171)
In the above equation, w is the Cauchy stress tensor, w s is its first invariant also called the mechanical pressure, w d is the strain-rate tensor and is the fluid viscosity that we assume to be constant (it is usually called “molecular viscosity”). Note that for an incompressible flow w gll = 0 and therefore w d = w dG = Taking into account the incompressibility constraint in Eq. (5.170), it is important to realize that the pressure cannot not be associated to its energy conjugate: the volume strain rate, because it is zero; hence, the pressure will have to be determined from the equilibrium equations on the fluid-flow domain boundaries. Therefore it is not possible to solve an incompressible fluid flow in which all the boundary conditions are imposed velocities, at least at one boundary point we need to prescribe the tractions acting on it. Many industrially important fluids, like polymers, do not obey Newton’s constitutive equation. They are generally called non-Newtonian fluids. When
5.5 Newtonian fluids
181
bulk metal forming processes are described neglecting the material elastic behavior (i.e. neglecting the material memory) the resulting constitutive equation is usually a non-Newtonian one (Zienkiewicz, Jain & Oñate 1977).
5.5.1 The no-slip condition When solving a fluid flow usually two kinematic assumptions are made: • At the interface between the fluid and the surrounding solid walls the velocity of the fluid normal to the walls is zero. • At the interface between the fluid and the surrounding solid walls the velocity of the fluid tangential to the walls is zero. The first of the above assumptions is quite obvious when referring to nonporous walls: the fluid cannot penetrate the walls. The second of the above assumptions is not so obvious and, as a matter of fact, it has been historically the subject of much controversy; our faith in it is only pragmatic: it seems to work (Panton 1984).
6 Variational methods
In this chapter we will assume that the reader is familiar with the fundamentals of variational calculus. The topic can be studied from a number of references, among them (Fung 1965, Lanczos 1986, Segel 1987, Fung & Tong 2001). The most natural way for starting the presentation of the theory of mechanics is by accepting the Principle of Momentum Conservation as a law of Nature and then stepping forward to demonstrate the Principle of Virtual Work as a consequence of the momentum conservation; this is perhaps the most direct way for developing the mechanical concepts because the Principle of Momentum Conservation is quite intuitive to the reader with a background in basic mechanics. An alternative route for developing the theory of mechanics is by accepting the Principle of Virtual Work as a law of Nature and then stepping forward to demonstrate the Principle of Momentum Conservation. This route is perhaps not as intuitive as the first one but equally valid from a formal point of view. However, more important than deciding which formulation is aesthetically more rewarding, an important fact for the scientist or engineer interested in solving advanced problems in mechanics is that the Principle of Virtual Work, and the other variational methods that can be derived from it, are the bases for the development of approximate solutions to problems for which analytical solutions cannot be found (Washizu 1982, Fung & Tong 2001).
6.1 The Principle of Virtual Work We have represented in Fig. 6.1 the spatial configuration of a continuum body w B; its external surface w V can be subdivided into: w Vx : on this surface the displacements are prescribed as boundary conditions, w V : on this surface the external loads are prescribed as boundary conditions.
184
Nonlinear continua
Fig. 6.1. Spatial configuration of a continuum
It is important to realize that a given point can pertain to w Vx in one direction and to w V in another direction, but at one point, the displacement and the external load corresponding to the same direction cannot be simultaneously specified. Taking this into account we realize that the surfaces w V> w Vx and w V have to be defined as the addition of the surfaces corresponding to each of the three space directions. Also, w
w
V = w Vx ^ w V > Vx _ V = B = w
The external forces acting on the body w B in the spatial configuration are: t : external loads per unit surface acting on w V > w b : external loads per unit mass. w
We refer the continuum body to a spatial Cartesian coordinate system {w } }. To each point in the wconfiguration, which is an equilibrium configuration of the continuum body, we can associate a displacement vector w u. We can also define an admissible displacements field as (Fung 1965), w
e (w } ) = w u(w } ) + w u(w } ) = u
(6.1)
In the above w u is the variation of the displacements field, called the virtual displacements. The virtual displacements have to satisfy the boundary condition w u 0 on w Vx and they are arbitrary on w V > (Fung 1965).
6.1 The Principle of Virtual Work
185
e , the external Assuming that when the continuum evolves from w u to w u loads remain constant, the work performed by them is the virtual work of the external loads ( w Zh{w ), Z Z w w w Zh{w = b · w u w w dY + t · w u w dV = (6.2) wY
wV
Using in the above Eq.(3.7), which is an equilibrium equation for the particles on the body surface, we get Z Z ¡w ¢ w t · w u w dV = w x w q w dV (6.3a) wV wV Z ¡w ¢ w x w q w dV (6.3b) = w ZV ¡w ¢ w x > w dY = (6.3c) = wY
In the above, for deriving the last line we have used Gauss’ theorem. Hence, Z Z Z w w w t · w u w dV = > w x w dY + (w x> ) w dY = (6.4) wV
wY
wY
In the last integral we have used the equality (Fung 1965) µ w ¶ C x C ¡ w ¢ = w x = w C } C }
(6.5)
Using in Eq. (6.4) the momentum conservation equation (Eq.(4.27b)), Z Z Z ¡ ¢ w w w t · w u w dV = e w x w w dY + w x> w dY = (6.6) wV
wY
wY
In the derivation of the above equation we have assumed in Eq. (4.27b) w that GGwv = 0; however, dynamic problems can also be considered by including the inertia forces among the external loads per unit mass (Crandall 1956). It is easy to show that, w
w x> = w w % " ¡ ¢ ¢# ¡ w C w x 1 C x w + = % = 2 C w } C w }
(6.7a) (6.7b)
In the above equations the terms w % are the infinitesimal strain components developed by the virtual displacements; hence, we refer to them as virtual strain components.
186
Nonlinear continua
Note that the actual strains in the t-configuration are arbitrary, only the virtual strains are infinitesimal. Replacing with Eq. (6.7a) in Eq. (6.6), Z Z Z w w b · w u w w dY + t · w u w dV = wY
wV
w
: w % w dY =
(6.8)
wY
The above equation is the mathematical statement of the Principle of Virtual Work and it states that for a continuum body in equilibrium, the virtual work of the external loads equals the virtual work of the stresses. Notes: • No assumption was made on the material, i.e. on its stress - strain relation; hence, the Principle of Virtual Work holds for any constitutive relation. • No assumption was made on the actual strains in the spatial configuration; hence, the Principle of Virtual Work holds for finite or infinitesimal strains. • No assumption was made on the external loads; hence, the Principle of Virtual Work holds for conservative and nonconservative loads (Crandall 1956). • The integrals in Eq. (6.8) are calculated on the spatial configuration of the body. • The Principle of Virtual Work was derived from momentum conservation and not from energy conservation. As we see the Principle of Virtual Work is a very general statement, holding for any type of nonlinearities that may be present in the spatial configuration (material and geometrical nonlinearities). It is also possible to go through the inverse route, that is to say, starting from the Principle of Virtual Work to demonstrate the equations of momentum conservation. For this demonstration we refer the reader to (Fung 1965, Fung & Tong 2001).
6.2 The Principle of Virtual Work in geometrically nonlinear problems In Eq. (6.8) the integrals are calculated in the spatial configuration of the continuum, which is normally one of the problem unknowns; however, for geometrically linear problems (w x> ?? 1) the di erence between the spatial configuration and the unloaded configuration, normally the reference configuration, is negligible; hence w
Y w V
= =
Y V=
(6.9a) (6.9b)
6.2 The Principle of Virtual Work in geometrically nonlinear problems
187
In the case of geometrically nonlinear problems it is convenient to calculate the integrals in Eq. (6.8) using the reference configuration. The coordinates w } remain constant during the virtural displacement; hence, ¶ µ 1 C w y C w y d w % + (6.10) = dw 2 C w } C w }
where w v is the virtual velocity vector. Equation (3.11) is valid for any velocity field, in particular when we use the virtual velocity field, we get using Eq. (6.10), Z Z w w : w % w dY = : w % dY = (6.11) wY
Y
Replacing in Eq. (6.8), Z
wY
w
b · w u w w dY +
Z
w
wV
t · w u w dV =
Z
w
: w % dY =
Also, using another pair of energy conjugate measures, Z Z Z w w w w b · w u w w dY + t · w u w dV = r S : r % dY = wY
wV
(6.12)
Y
(6.13)
Y
In the above, w r S: second Piola-Kirchho stress tensor, w r %: Green-Lagrange strain tensor. We can define a general load, either a load per unit mass or per unit surface as: w
f = o p* =
(6.14)
In the above, o is a scalar proportional to the load modulus and (Schweizerhof & Ramm 1984): • o = 0 implies that the load modulus is a function of the reference coordinates (body-attached loads); • o = w implies that the load modulus is a function of the spatial coordinates (space-attached loads). The unitary vector
p
* is a direction and (Schweizerhof & Ramm 1984):
• p = 0 implies a constant direction load; • p = w implies a follower load (the direction is a function of the body displacements).
188
Nonlinear continua
Example 6.1. JJJJJ Buckling of a circular ring. In (Brush & Almroth 1975) we find that the elastic buckling pressure acting on a circular ring depends on the type of load that we consider: Load
Buckling pressure
Hydrostatic pressure loading
sfu = 3 HL d3
Centrally directed pressure loading
sfu = 4=5 HL d3
Both are cases of follower loads but, the description of the load as a function of the displacements is di erent. JJJJJ
Using the mass conservation principle in Eq. (4.20d) we can write, Z Z w w b · w u w w dY = b · w u r dY = (6.15) wY
Y
At each point on the surface bounding the continua we can calculate, w
hence,
Z
wV
w
w
dV = w MV dV >
w
t · u dV =
Z
V
w
(6.16)
t · w u w MV dV =
(6.17)
Therefore, we can write the principle of Virtual Work calculating the integrals over the reference configuration as, Z Z Z w w w w b · w u r dY + t · w u w MV dV = r S : r % dY = (6.18) Y
V
Y
JJJJJ Example 6.2. Let us consider the work of the external loads per unit surface of the spatial configuration for the case of a typical follower load: the hydrostatic fluid pressure. In this case, w t = ws wn where w n is the surface external normal. For this case, Z V w = s w u · w n w dV = w Zh{w wV
6.2 The Principle of Virtual Work in geometrically nonlinear problems
189
Using Nanson’s formula (Example 4.9) we get, Z V w = s w u · w M n · wr X1 dV = w Zh{w V
For a case with infinitesimal strains, w
M r1 r wr RW
w 1 rX
and therefore, V Zh{w
=
Z
V
h
w W rR
i £ ¤ · w u · w s n dV =
In the above equation, the first bracket inside the integral is the displacements variation rotated back from the spatial configuration to the material one; and the second bracket is the load per unit surface, but in the reference configuration. Hence, it is very important to realize that for the case of fluid-pressure loads and infinitesimal strains we can easily calculate the external surface loads virtual work in the reference configuration. JJJJJ
Z
Using other alternative energy conjugate stress/strain measures, Z Z w w w w W b· w u r dY + t· w u w MV dV = r P : r X dY > (6.19)
Y
V
Y
and, for an isotropic constitutive relation Z Z Z w w b · w u r dY + t · w u w MV dV = Y
V
w Y
: wr H dY = (6.20)
6.2.1 Incremental Formulations We have represented in Fig. 6.2 a typical Lagrangian analysis where the configuration at w = 0 is known and the configuration at w = w1 is sought. Normally, we perform an incremental analysis; that is to say, we determine the sequence of equilibrium configurations at w = 0> ===> w> w + w> ===w1 = In this incremental analysis, the basic link to be analyzed is the generic step w $ w + w; that is to say, knowing the equilibrium configuration at w we seek the one at w + w= Of course, once this generic step can be solved, then the complete incremental analysis can be performed. In what follows, to describe the step w $ w + w we follow the presentation in (Bathe 1996).
190
Nonlinear continua
Fig. 6.2. Lagragian incremental analysis
First, we have to recognize that for describing the w + w-configuration we can use as a reference configuration either the one at w = 0 or any of the intermediate ones, already known. In what follows we will specifically analyze two particular cases: • The total Lagrangian formulation, where we use as the reference configuration the one at w = 0 (usually the undeformed configuration) • The updated Lagrangian formulation, where we use as the reference configuration the previous one (w). The total Lagrangian formulation Using the principle of Virtual Work to define the w + w equilibrium configuration, we write: Z w+w LM w+w V r %LM dY = w+w Zh{w = (6.21) r Y
In the above equation, components of the second Piola-Kirchho stress tensor, corresponding to the w + w configuration and referred to the configuration at w = 0= w+w %LM : components of the Green-Lagrange strain tensor, corresponding to r the w + w configuration and referred to the configuration at w = 0= n o A general curvilinear coordinate system {L > L = 1> 2> 3 is used in the reference configuration, with covariant base vectors gO (O = 1> 2> 3)= The volume of the reference configuration is Y and the virtual work of the external loads acting at time w + w is w+w Zh{w (see the previous section for a discussion on the calculation of this term). We can write, w+w LM V = wr V LM + r V LM (6.22) r w+w LM V : r
where r V LM are the components of the incremental second Piola-Kirchho stress tensor. It is important to recognize that the three tensors in Eq. (6.22)
6.2 The Principle of Virtual Work in geometrically nonlinear problems
191
Fig. 6.3. Total Lagrangian formulation
are referred to the same reference configuration (w = 0). For the GreenLagrange strain tensor we can also write an incremental equation, w+w %LM r
= wr %LM + r %LM >
(6.23)
again, in the above equation the three tensors are referred to the same reference configuration (w = 0). Replacing with Eqs. (6.22) and (6.23) in Eq. (6.21) and taking into account that for the step that we are investigating, wr %LM is data and therefore, wr %LM = 0, we get Z (wr V LM + r V LM ) r %LM dY = w+w Zh{w = (6.24) Y
We write an incremental constitutive equation of the form, rV
LM
= r F LMNO r %NO
(6.25)
and get, Z
Y
(wr V LM + r F LMNO r %NO ) r %LM dY = w+w Zh{w =
(6.26)
Refering the problem to a fixed Cartesian system, we can write for a generic particle S , as shown in Fig. 6.3: w S
u = w xS xS uS = w+w uS w uS =
We can show that (Bathe 1996),
(6.27a) (6.27b)
192
Nonlinear continua
¢ 1¡ w w r x> + r x> + r x> r x> + r x> r x> + r x> r x> = 2 (6.28) Cx C w x w In the above equation, r x> = C } and r x> = C } .
r %
=
Hence, it is possible to rewrite Eq. (6.28) as, r % r h r
r h + r ¢ 1¡ w w = r x> + r x> + r x> r x> + r x> r x> 2 1 = r x> r x> = 2
=
(6.29a) (6.29b) (6.29c)
The term in Eq. (6.29b) is linear in the unknown incremental displacements, u, while the term in Eq. (6.29c) is nonlinear. We introduce Eq. (6.29a) in Eq. (6.26) and obtain, Z [wr V + r F (r h + r )] (r h +r ) dY = w+w Zh{w = (6.30) Y
The above is the momentum balance equation at time w + w; which is a nonlinear equation in the incremental displacement vector. In order to solve it we use an iterative technique, in which the first step is the linearization of Eq. (6.30) (Bathe 1996). Keeping only up to the linear terms in u, we obtain the linearized momentum balance equation: Z [r F r h r h + wr V r ] dY (6.31) Y Z w = w+w Zh{w r V r h dY = Y
The updated Lagrangian formulation Using the principle of Virtual Work to define the w + w equilibrium configuration, we write: Z w+w LM w+w V w %LM w dY = w+w Zh{w = (6.32) w wY
In the above equation, components of the second Piola-Kirchho stress tensor, corresponding to the w + w configuration and referred to the configuration at w= w+w %LM : components of the Green-Lagrange strain tensor, corresponding to w the w + w configuration and referred to the configuration at w= w+w LM V : w
We can write, w+w LM V w
= ww V LM + w V LM
(6.33)
6.2 The Principle of Virtual Work in geometrically nonlinear problems
193
where ww V LM = w LM and w V LM are the components of the incremental second Piola-Kirchho stress tensor; it is important to recognize that the three tensors in Eq. (6.33) are referred to the spatial configuration at time w. Also, w+w %LM = w %LM = (6.34) w because ww %LM = 0. Replacing with Eqs. (6.33) and (6.34) in Eq. (6.32), we get Z ¡w LM ¢ + w V LM (w %LM ) w dY = w+w Zh{w >
(6.35)
wY
we can write an incremental constitutive equation referred to the wconfiguration, wV
and get, Z
wY
¡w
LM
= w F LMNO w %NO >
(6.36)
¢ LM + w F LMNO w %NO (w %LM ) w dY = w+w Zh{w =
(6.37)
In a fixed Cartesian system we can show that (Bathe 1996), w %
where
w x>
=
Cx C w }
=
1 (w x> + w x> + w x> w x> ) 2
(6.38)
=
We can decompose the strain increment into a linear and a nonlinear increment in the unknown incremental displacement; that is to say, w % w h w
= w h + w 1 = (w x> + w x> ) 2 1 = (w x> w x> ) = 2
(6.39)
Hence we can write Eq. (6.37) as, Z
wY
£w
+ w F
¡
w h
+ w
¢¤
¡
w h
+ w
¢
w
dY = w+w Zh{w =
(6.40) The above is the momentum balance equation at time w + w; which is a nonlinear equation in the incremental displacement vector. Proceeding in the same way as in the total Lagrangian formulation we obtain the linearized momentum balance equation (Bathe 1996): Z Z w w w w dY (6.41) w F w h w h dY + wY wY Z w w h w dY = = w+w Zh{w wY
194
Nonlinear continua
It is easy to show that rV
LM
r
V w w
=
lm
¡w
r[
¢ 1 L l
¡w
r[
= w %lm wr [ lL wr [ mM
r %LM
¢ 1 M m
(6.42) (6.43)
and therefore if the same material is considered in both formulations the incremental constitutive tensors should be related, F
LMNO
r
=
F w w
pqst
¡w
r[
¢ 1 L p
¡w
r[
¢ 1 M q
¡w
r[
¢ 1 N s
¡w
r[
¢ 1 O t
= (6.44)
Any problem can be alternatively solved using either the total or the updated Lagrangian formulations and the results should be identical (Bathe 1996). For solving finite-strain elastoplastic problems, in Sect. 5.2.6 we introduced an adhoc incremental formulation, the total Lagrangian-Hencky formulation.
6.3 The Principle of Virtual Power There are formulations where the primary unknowns are the material velocities rather than the material displacements (e.g. fluid problems, metal-forming Eulerian (Dvorkin, Cavaliere & Goldschmit 1995, Dvorkin & Petöcz 1993) or ALE formulations (Belytschko, Liu & Moran 2000), etc.). For these cases the momentum conservation leads to, Z Z Z w w w w w w w w b · v dY + t · v dV = : w d w dY = (6.45) wY
wV
wY
In the above equation w v is the material velocity at a point and w d is the strain-rate tensor. Of course, we can use, for formulating the Principle of Virtual Power, other energy conjugated stress/strain rate measures, for example: Z Z Z w r w w w w w b · v dY + t · v MV dV = : w d dY > (6.46a) Z
Y
w
Y
Z
Z
w Y
w Y
b · w v r dY +
Z
V
w
V
b · w v r dY +
b · w v r dY +
w
Z
Z
t · w v w MV dV = w
V
w V
Z
Y
Y
t · w v w MV dV =
t · w v w MV dV =
Z
w rS
Z
Y
Y
·
: wr % dY > (6.46b)
w W rP
·
: wr X dY > (6.46c)
w
·
: wr H dY > (6.46d)
6.4 The Principle of Stationary Potential Energy
195
the last one only being valid for isotropic constitutive relations.
6.4 The Principle of Stationary Potential Energy As we remarked above, the Principle of Virtual Work can be used for any material constitutive relation, for any type of loading and for any nonlinearity in the case to be analyzed. In the present section we will specialize the Principle of Virtual Work for: • Hyperelastic materials. • Conservative external loads. For a hyperelastic material we have seen in Chap. 5 (Eq. (5.3d) that, w LM rV
= r
C w U( wr %) = C wr %LM
(6.47)
The external conservative loads are the external loads that can be derived from a potential. Hence, a load field is said to be conservative in a region if the net work done around any closed path in that region is zero (Crandall 1956). A typical conservative load system can be represented as, w
f=
* =
(6.48)
Following the definitions introduced above, the load system in Eq. (6.48) is a body attached load system with constant direction. For conservative loads per unit mass, we write w
C w J (w u) Cu
(6.49)
C w j (w u) = Cu
(6.50)
b=
and for conservative surface loads w
t=
Note that the above-defined surface loads are defined as loads per unit R reference surface; therefore, its resultant at time w is V w t dV . We now define a functional of the function w u called the potential energy functional: Z Z ¡w ¢ w w w = U + J dY + j dV (6.51) r Y
V
196
Nonlinear continua
Therefore, Z "
w
=
Y
CwU w : w % + C %
# Z CwJ w C wj w · u dY + · u dV = (6.52) Cu Cu V
¡ ¢ In the above, w u are admissible variations w u = 0 on Vx see Fig. 6.1 and w % is derived from the displacement variations. Therefore, Z h Z i w w w w w w = dY t · w u dV = (6.53) S: % b · u Y
V
Hence, for a hyperelastic material under a conservative load system, the principle of virtual work, in Eq. (6.18), can be written as w = 0 =
(6.54)
The above equation states that when the wconfiguration is in equilibrium the potential energy functional reaches a stationary value; i.e. it fulfills the necessary requirements for being an extreme (Fung 1965). In what follows we show that in the case of infinitesimal strains the potential energy not only is stationary at the equilibrium configuration but it actually attains there a minimum. Using the nomenclature introduced in Eq. (6.1) we write the potential energy functional for an admissible configuration close to the equilibrium one as w 0 r
=
Z
Y
Z
£ ¡ ¢¤ w U(w % + w %) w b · w u + w u dY w
V
t·
¡w
Using a Taylor expansion, w w U( % + w %)
¢ u + w u dV =
¯ w ¯ C U ¯ = w U(w %) + w ¯ C % ¯w
%
Hence, w 0 r
w r
=
w
+
Z
Y
(6.55)
:
w % +
¯ 1 w C 2w U ¯¯ % : w ¯ 2 C % Cw % ¯w
%
¯ C 2w U ¯¯ 1 w % : w ¯ 2 C % Cw % ¯w
%
: w % + · · ·
=
(6.56)
: w % dY + · · · = (6.57)
Since at equilibrium w = 0, the sign of the l.h.s. is the sign of the integrand on the r.h.s..
6.4 The Principle of Stationary Potential Energy
197
w In the case of infinitesimal strains case we can ¯ assume that % 0 and we ¯ w ¯ have w U(0) = 0 (convention) and w S¯0 = CCw U% ¯ = 0; hence, from Eq. (6=56)
0
¯ ¯ 2w 1 C U ¯ w w w U( %) = % : w ¯ 2 C % Cw % ¯
0
: w % + · · · =
(6.58)
Since, in a stable material the value of the elastic strain energy is positive for any strain tensor (the elastic strain energy is a positive-definite function) we conclude that, w 0 w (6.59) r r A 0 > and the potential energy is a local minimum at the equilibrium configuration. In the infinitesimal strains case we call it the minimun potential energy principle (Washizu 1982). JJJJJ
Example 6.3. Conservative and nonconservative loading. (a) Conservative loading
Let us consider a linear elastic, cantilever beam under the conservative endload shown in the figure,
Conservative load
The elastic energy stored in the beam is,
w
U=
Z
0
O
HL 2
µ
d2 w x2 dw }12
¶2
dw }1
where H is Young’s modulus and L is the beam cross section moment of inertia. The Principle of Virtual Work states,
198
Nonlinear continua
¡w
w U = w S x2 ¢ U S x2 = 0 w
w
where w = w U w S w x2 is the potential energy of the system. (b) Nonconservative loading We now consider the same linear elastic cantilever beam but under a follower load, as shown in the figure
Body-attached follower load The principle of virtual work states, ¡ ¢ ¡ ¢ w U = w S sin w x1 + w S cos w x2 =
For small displacement derivatives we can approximate µ w ¶ ¡ ¢ d x2 sin w w dw }1 O ¡w ¢ cos 1 hence,
µ w ¶ ¸ d x2 w w x1 + x2 = U= S dw }1 O w
Since w
w
¸ µ w ¶ CwG w d x2 w w = 6 S x + x · u 1 2 dw }1 O Cu
the load is nonconservative and the principle of stationary potential energy cannot be used. JJJJJ
6.4 The Principle of Stationary Potential Energy
199
Example 6.4. JJJJJ Stability of the equilibrium configuration (buckling) (Ho 1956). Let us consider the system shown in the following figure, in equilibrium at time w, in the straight configuration:
w
S : axial conservative load ; O : length of the rigid bar ; n : sti ness of
the linear spring; nW : sti ness of the torsional spring. Assume that the equilibrium configuration is perturbed with a rotation ?? 1. The axial load displacement is obtained from the following scheme:
200
Nonlinear continua
2
For ?? 1 , S O 2 and O sin() O . The potential of the external load is, w
J = w S S =
w
S O 2 = 2
The only deformable bodies are the springs; hence w
U=
1 1 n (O )2 + nW 2 = 2 2
Therefore the potential energy functional of the system is w r
=
w 1 1 S O 2 n O2 2 + nW 2 + 2 2 2
and the equilibrium configuration is defined by w = 0 which leads to,
£ ¤ n O2 + nW + w S O = 0 =
Since is arbitrary the bracket has to be zero. Two solutions are possible: (i) = 0 ; that ¡ is to say, ¢ the straight (undeformed) configuration. (ii) w S = n O + nOW .
For the second solution is undefined. We call this load value the critical value, Sfu , because at this load there are two branching solutions ( = 0 and 6= 0 ).
6.4 The Principle of Stationary Potential Energy
201
Sfu defines the bifurcation or buckling load. The equilibrium path is
Since in the above derivation the terms higher than 2 were neglected, we cannot assess anything about the branching equilibrium path.
JJJJJ
Example 6.5. JJJJJ Postbuckling behavior. We repeat the previous example derivation keeping terms higher than 2 . By doing this, we get µ 2 ¶ 4 S = O (1 cos ) O 2 4! µ 2 4¶ w J = w S S w S O 2 4! µ ¶2 1 1 3 w Un = n (O sin )2 n O2 2 2 3! 1 w UW = nW 2 = 2 Hence w r
=
1 n O2 2
µ ¶ 4 2 4 6 1 2 + + nW 2 + w S O wS O = 3 36 2 2 24
For the equilibrium configuration w = 0 and therefore, µ ¶ ¸ 2 3 3 5 2 w w nO + + nW + S O S O = 0 = 3 12 6
202
Nonlinear continua
Since is arbitrary, we get, neglecting terms higher than 3 , µ µ ¶ ¶¸ 2 2 2 2 w nO 1 + nW + S O 1 =0 3 6 which has again two possible solutions: (i) = 0 the straight solution ´ ³ (ii) w S =
n O
1 2 3
2
+
nW O
2 1 6
¡ ¢ In the second solution, for = 0> w S = Sfu = n O + nOW . The bifurcation point is the same as the one calculated in the previous example; however, now is defined. We see that for A 0 Eq. (ii) provides w S = w S (). If we examine the case with nW = 0, we get ´ ³ 2 n O 1 2 3 wS = 2 1 6 and we can represent
If we examine the case with n = 0, we get wS = and we can represent
n ³ W O 1
2 6
´
6.4 The Principle of Stationary Potential Energy
203
It is clear that the above cases represent two very di erent behaviors from a structural point of view. For the case nW = 0, the buckling is catastrophic because for A 0 the load-carrying capacity of the structure keeps dimishing: unstable postbuckling behavior. For the case n = 0, the load-carrying capacity of the structure increases after buckling: stable postbuckling behavior. JJJJJ JJJJJ Example 6.6. Natural boundary conditions. Let us study the following linear elastic cantilever beam under conservative loads:
H : Young’s modulus; L : moment of inertia of the beam cross section. Assume w x2 =w x2 (w }1 ) is the beam transversal displacement and using linear beam theory (Ho 1956)
204
Nonlinear continua w
µ 2 w ¶2 Z O d x2 HL w w w d } t x2 dw }1 1 w} 2 2 d 1 0 µ w ¶ 0 ¡w ¢ d x2 w w SO x2 O PO = dw }1 O
=
Z
O
For the equilibrium configuration w = 0; hence Z
O
HL
0
¶ Z O ¡ ¢ d2 w x2 w w d }1 t w x2 dw }1 dw }1 2 µ w0 ¶ ¸ ¡ ¢ d x2 =0= w SO w x2 O w PO dw }1 O
µ
d2 w x2 dw }1 2
¶
µ
In the first integral we use (Fung 1965) grating by parts twice, we get Z
O
0
³
d2 w x2 dw }1 2
´
=
d2 dw }1
2
((A))
¡ w ¢ x2 and inte-
µ
¶ ¸O d2 w x2 d2 w x2 d ¡ w ¢ d2 ¡ w ¢ w HL x2 d }1 = H L w 2 w x2 dw }1 2 dw }1 2 d }1 d }1 0 ¸O Z O 3 w 4 w d x2 d x2 H L w 3 w x2 + H L w 4 w x2 dw }1 = d }1 d }1 0 0
At w }1 = 0 we have as boundary conditions w x2 = h ³ w ´i ¡ w ¢ x2 w } =0 = ddwx}12 = 0. 1
w}
dw x2 dw }1
= 0, hence,
1 =0
Replacing in (A), we get Z
0
O
¸ µ ¶ ¸ ¡ ¢ d3 w x2 d4 w x2 w w w w + SO w x2 O H L w 4 t x2 d }1 H L w 3 d }1 d }1 µ ¶ ¸ µ w ¶O d2 w x2 d x2 + HL w 2 w PO =0= d }1 dw }1 O O
Since w x2 is arbitrary at every point 0 6 following di erential equation w
t= HL
w
}1 6 O we must fulfill the
d4 w x2 dw }1 4
which is the well-known equation of beam theory. At w }1 = O we get
6.4 The Principle of Stationary Potential Energy
205
Essential (rigid) boundary conditions
or Natural boundary condition
Either (w x2 )O is fixed and (w x2 )O = 0
or w SO = H L
Either
³
dw x2 dw }1
´
O
is fixed and
³
dw x2 dw }1
´
O
= 0 or w PO = H L
³
³
d3 w x2 dw }1 3
d2 w x2 dw }1 2
´
´
O
O
JJJJJ
.
Example 6.7. JJJJJ The Rayleigh-Ritz method. In the previous example, from the principle of stationary potential energy we derived the di erential equation that governs the deformation of a cantilever beam. Usually, we need to work in the opposite direction: we know the di erential equations that govern the deformation of a continuum but we cannot integrate them and we resort to the principle of stationary potential energy to derive an approximate solution. One method for deriving approximate solutions is the Rayleigh-Ritz method (Ho 1956). Let us consider again the linear case analyzed in the previous example and let us assume that we want to derive an approximate solution for the case w t = w SO = 0. For this case w
=
Z
0
O
HL 2
µ
d2 w x2 dw }1 2
¶2
dw }1 w PO
µ
dw x2 dw }1
¶
=
O
To derive an approximate solution we consider trial functions that fulfill the geometrical or essential boundary conditions, µ w ¶ d x2 w x2 (0) = =0= dw }1 0 For example w
µ ¶ w }1 x2ª (w }1 ) = d 1 cos 2O
where the parameter d will be determined by imposing the minimization condition on w ª = w ª (d) = Using the adopted trial function, we get w
ª =
w H L 4 d2 PO d = 64 O3 2O
206
Nonlinear continua
The minimum value that can attain the above functional is, within the considered set of trial functions, our best approximation to the equilibrium configuration. Imposing Cw ª =0> Cd we get 16 w PO O2 = d= H L 3 Therefore our approximate solution is µ ¶ w }1 16 w PO O2 w ª w 1 cos x2 ( }1 ) = H L 3 2O w 2 4 PO O w ª = = H L 2 For the case we are analyzing the exact solution is w
¡w ¢ w PO (w }1 )2 }1 = 2HL w P2 O w h{dfw = O = 2HL
x2 h{dfw
It is obvious that w ª A w h{dfw . If we want to improve our approximate solution we enrich the trial function set using, for example µ ¶ µ ¶ ¡ ¢ w }1 w }1 w x2 w }1 = d 1 cos + e 1 cos = 2O O
It is important to note that the above defined trial function: Fulfills the essential (rigid) boundary conditions. Contains the previous one, w x2 ª (w }1 ), as a particular case (e = 0). Since we will determine the values of both constants by imposing on w the necessary conditions for attaining a minimum, it is obvious that w
6 w ª =
That is to say, we will either find the same solution as before (e = 0 and = w ª ) or a better one (e 6= 0 and w ? w ª ). We cannot deteriorate the solution by adding more terms in the trial function. Using w x2 (w }1 ) > we get µ ¶ w H L 3 de 2 2 PO d w = + + d e = 3 2O 3 32 2 2O w
Imposing
Cw Cd
=
Cw Ce
= 0, we get
6.5 Kinematic constraints
207
w
PO O2 HL w PO O2 e = 0=0668 HL w 2 P w O O = 0=4940 = HL d = 0=6294
It is clear from the derived values that, as expected: w h{dfw ? w ? w ª , and therefore w x2 (w }1 ) is a “better” approximation than w x2 ª (w }1 ). JJJJJ In the previous example we have introduced three relevant topics that we want to highlight: 1. When obtaining approximate solutions using the Rayleigh-Ritz method, based on the minimum potential energy principle (infinitesimal strains), we can only rank the merit of di erent solution using their potential energy value; that is to say, if w D ? w E then the D-solution is a better approximation than the E-solution. 2. The trial functions have to exactly satisfy the rigid boundary conditions (admissible functions) but not the natural boundary conditions. 3. Approximate solutions do not need to fulfill exactly either the equilibrium equation inside the dominium or the natural boundary conditions (equilibrium equations on the boundary).
6.5 Kinematic constraints In the example shown in Fig. 6.4, where w S is a conservative load, the potential energy is, 1 w = n w x2 w S w y = (6.60) 2 For the inextensible string there is a kinematic constraint given by, 2 wy wx = 0 =
(6.61)
Hence, we have to minimize the functional of the potential energy given in Eq.(6.60) under the constraint expressed in Eq. (6.61)= Using the Lagrange multipliers technique (Fung 1965, Fung & Tong 2001), we define a new functional (w ) and we perform on it an unconstrained minimization: w
=
¡ ¢ 1 w 2 n x wS wy + w 2 wy wx 2
where w is the Lagrange multiplier.
(6.62)
208
Nonlinear continua
Fig. 6.4. Kinematics constraints
We need to determine the set ( w > w x> w y) that satisfies w = 0. The necessary conditions are, C w =0 C w C w =0 C wx C w =0= C wy
(6.63a) (6.63b) (6.63c)
From the above we get, w
S 2n w S w y= 4n
w
w
x=
= n wx =
(6.64a) (6.64b) w
S = 2
(6.64c)
JJJJJ Example 6.8. Physical interpretation of the Lagrange multiplier in the above example (Crandall 1956). Let us assume that the string, instead of being inextensible has a sti ness nv ; hence, with w the tensile load on the spring we have, ¢ ¡ w = nv 2 w y w x =
6.6 Veubeke-Hu-Washizu variational principles
209
For this system with no constraints we can define the potential energy w
nv =
¢2 ¡ 1 w 2 1 n x + nv 2 w y w x w S w y 2 2
and w nv = 0 leads to,
Hence,
¢ ¡ n w x nv 2 w y w x = 0 ¢ ¡ 2 nv 2 w y w x w S = 0 = w
w
x=
S 2n
Also,
;
w
w
=
S = 2
w
$ 0= nv nv $4 Therefore, w is independent of the displacement (conservative load) and we can use Eq. (6.62) for writing the potential energy, and identify the Lagrangian multiplier with the string tensile load. JJJJJ 2 wy wx =
In the above example, it is important to realize that the Lagrangian multiplier is the energy conjugate of the physical magnitude that represents the constraint equation: the string elongation.
6.6 Veubeke-Hu-Washizu variational principles In the previous section we analyzed a simple mechanical system and we developed the imposition, using the Lagrange multipliers technique, of a kinematic constraint on the stationarization of the potential energy functional. In the present section we are going to generalize the above technique to impose di erent constraints on the potential energy functional (Fraeijs de Veubeke 1965). 6.6.1 Kinematic constraints via the V-H-W principles Let us assume that we relax the compatibility conditions (see Sect. 2.15) when formulating the potential energy functional; that is to say we consider in Eq. (6.51) a strain tensor wr % that can not necessarily be derived from the displacements field. We now define the functional: Z Z £ w ¡w ¢ w w ¤ ¡ ¢ w w r + = U % J( u) dY + j w u dV (6.65) r r Y V Z ¡ ¢ w : (wr % w u wr %) dY + Y
210
Nonlinear continua
and we search for the equilibrium configuration imposing w = 0
(6.66) w
we have as independent variables: w u> wr % and w ; with wr S = r CCw %U we get r
Z
+
Z
Y
Z
:
w r % dY
r
w
Z
w b · u dY t · w u dV (6.67) V Z w w w w : (r % r %) dY + : ( wr % wr %) dY = 0 =
Y
w rS
w
Y
Y
Considering that the variations are arbitrary, Z Z Z w w r w : wr % dY = b · w u dY + t · w u dV Y Y V Z ¡w ¢ w w r S : r % dY = 0 ZY w : (wr % wr %) dY = 0 =
(6.68) (6.69) (6.70)
Y
The last equations impose the conditions w rS w r%
= w
(6.71)
w r%
(6.72)
=
which are always fulfilled for the continuum problem but not necessarily in finite element approximations. Adding Eqs. (6.68) and (6.69), we get Z Z w w w S : % dY + : ( wr % wr %) dY (6.73) r r Y Y Z Z w r w = b · w u dY + t · w u dV = Y
V
From the above, we can state the Principle of Virtual Work as, Z Z Z w w w w r w S : % dY = b · u dY + t · w u dV r r Y
Y
(6.74)
V
as long as we fulfill the condition of variational consistency (Simo & Hughes 1986), Z w : ( wr % wr %) dY = 0 > (6.75) Y
which is obviously fulfilled for the continuum problem.
6.6 Veubeke-Hu-Washizu variational principles
211
6.6.2 Constitutive constraints via the V-H-W principles Let us now assume that we consider in Eq. (6.51) a stress tensor wr S that is not necessarily derived from the kinematically consistent strain field wr %. We can write w rS
=
r
CwU Crw %
(6.76a)
w rS
=
r
CwU = Crw %
(6.76b)
Therefore w r
=
Z
r
Y
Z £w ¡w ¢ w w ¤ ¡ ¢ w U r % + J( u) dY + j w u dV V Z w + : ( wr S wr S) dY =
(6.77)
Y
We search for the equilibrium configuration imposing w = 0 >
(6.78)
¡ ¢ and considering the independent variables w u>w and wr % > wr S : Z Z w w w : wr S dY = 0 (6.79) r S : r % dY Y Y Z Z Z w w r w : wr S dY b · w u dY t · w u dV = 0 (6.80) Y Y V Z w w w : (r S r S) dY = 0 = (6.81) Y
The last equation imposes the condition w rS
=
w rS
(6.82)
which is always fulfilled for the continuum problem but not necessarilly in the finite element approximations. Adding Eqs. (6.79) and (6.80), we get Z Z w w w S : % dY + : ( wr S wr S) dY r r Y Y Z Z w w r w b · u dY + t · w u dV = (6.83) = Y
V
From the above, we can state the Principle of Virtual Work as,
212
Nonlinear continua
Z
Y
w rS
:
w r % dY
=
Z
Y
r
w
w
b · u dY +
Z
V
as long as we fulfill the condition, Z w : ( wr S wr S) dY = 0 >
w
t · w u dV
(6.84)
(6.85)
Y
which is obviously fulfilled for the continuum problem. Other constraints can also be considered and they constitute the basis of di erent finite element applications. When using variational principles of the Veubeke-Hu-Washizu type for developing finite element formulations, the interpolation functions selected for the di erent interpolated fields should fulfill orthogonality conditions of the form of Eqs. (6.75) or (6.85) (Simo & Hughes 1986). Di erent forms of the Veubeke-Hu-Washizu variational principles have been used to develop mixed and hybrid finite element formulation some of them can be read from the classical paper (Pian & Tong 1969) and also from (Dvorkin & Bathe 1984, Bathe & Dvorkin 1985\1986, Dvorkin & Vassolo 1989, Fung & Tong 2001), etc.
A Introduction to tensor analysis
In this Appendix, assuming that the reader is acquainted with vector analysis, we present a short introduction to tensor analysis. However, since tensor analysis is a fundamental tool for understanding continuum mechanics, we strongly recommend a deeper study of this subject. Some of the books that can be used for that purpose are: (Synge & Schild 1949, McConnell 1957, Santaló 1961, Aris 1962, Sokolniko 1964, Fung 1965, Green & Zerna 1968, Flügge 1972, Chapelle & Bathe 2003).
A.1 Coordinates transformation Let us assume that in a three-dimensional space ( 2> 3 }, and an arbitrary system of curvilinear coordinates { l > l = 1> 2> 3 } . The following relations hold: l = l (} > = 1> 2> 3)
>
l = 1> 2> 3 =
(A.1)
The above functions are single-valued, continuous and with continuous first derivatives. We call M the Jacobian of the coordinates transformation defined by Eq. (A.1). Hence " # Cl M = = (A.2) C} An admissible transformation is one in which det M 6= 0, that is to say, a transformation where a region of nonzero volume in one system does not collapse into a point in the other system and vice versa.
214
Nonlinear continua
A proper transformation is an admissible transformation in which det M A 0. A.1.1 Contravariant transformation rule From Eq. (A.1) we obtain dl =
Cl d} = C}
(A.3)
When the coordinates system is changed, the mathematical entities dl at a certain point of m = 1> 2> 3) and
o n = n (ˆ > o = 1> 2> 3)
> >
l = 1> 2> 3
(A.4a)
n = 1> 2> 3 =
(A.4b)
We can write the coordinate di erentials as: dl =
Cl ˆm d m C ˆ
(A.4c)
l
l C ˆ dˆ = m dm = C
(A.4d)
In the same way, a contravariant mathematical entity can be defined in either of the two systems dl = dl (m > m = 1> 2> 3)
>
l = 1> 2> 3
(A.4e)
m ˆl (ˆ > m = 1> 2> 3) d ˆl = d
>
l = 1> 2> 3
(A.4f)
and we transform it from one curvilinear system to the other following a transformation rule similar to the transformation rule followed by the coordinate di erentials:
dl =
Cl m ˆ m d C ˆ
>
l = 1> 2> 3
(A.4g)
>
l = 1> 2> 3 =
(A.4h)
l
C ˆ m d ˆ = d Cm l
A.2 Vectors
215
Although the contravariant transformation rule applies to dl and not to l , using a notation abuse, we follow the convention of using upper indices for the coordinates.
A.1.2 Covariant transformation rule Given an arbitrary continuous and di erentiable function i (1 > 2 > 3 ) and using the chain rule, we write Ci Cm Ci = l Cm C ˆl C ˆ We define dm =
>
Ci Cm
l = 1> 2> 3 =
>
m = 1> 2> 3 =
(A.5a)
(A.5b)
l In the {ˆ } coordinate system we define
d ˆm =
Ci m C ˆ
d ˆl = dm
>
Cm l C ˆ
m = 1> 2> 3 >
l = 1> 2> 3
(A.5c) (A.5d)
m
C ˆ > l = 1> 2> 3 = (A.5e) Cl When the coordinates system is changed, the mathematical entities dl at a certain point of 2> 3) are the components of v in the basis gl (l = 1> 2> 3). Example A.1. In a Cartesian system {} > = 1> 2> 3} the base vectors are
JJJJJ
e1 = (1> 0> 0) > e2 = (0> 1> 0) > e3 = (0> 0> 1) > where we have indicated the projection of the base vectors on the Cartesian axes. The position vector r of a point S in but also, dr =
Cr d} = C}
Therefore, we get e =
Cr C}
> = 1> 2> 3 = JJJJJ
A.2.2 Covariant base vectors In the arbitrary curvilinear system {l > l = 1> 2> 3} we can write, at any point S of the space, Cr (A.7a) dr = l dl = C Since
A.2 Vectors
217
Fig. A.1. Covariant base vectors at a point P
dr = dl gl
(A.7b)
we obtain
Cr > = 1> 2> 3 = (A.7c) Cl The vectors gl , defined with the above equation, are the covariant base vectors of the curvilinear coordinate system { l } at the point S . From its definition, the vector g1 is tangent to the line, 2 = 2 (S ) and 3 = 3 (S ) . Similar conclusions can be reached for the covariant base vectors g2 and g3 . In a Cartesian system, we can write Eq. (A.7c) as: gl =
gl =
C} e Cl
> l = 1> 2> 3 =
l In a second curvilinear system { ˆ > l = 1> 2> 3 },
(A.8)
218
Nonlinear continua
ˆm l l C ˆ dr = d g ˆl = d g ˆ = Cl m
(A.9a)
Hence, we have m
C ˆ g ˆ > l = 1> 2> 3 = (A.9b) Cl m Due to the similarity between Eqs. (A.9b) and Eq. (A.5e) the base vectors gl are called covariant base vectors. gl =
A.2.3 Contravariant base vectors In an arbitrary curvilinear coordinate system { l > l = 1> 2> 3 } we define the contravariant base vectors (dual basis) (gl > l = 1> 2> 3) with the equation gl · gm = lm >
(A.10)
where the dot indicates a scalar product (“dot product”) between two vectors and lm is the Kronecker delta ( lm = 1 for l = m and lm = 0 for l 6= m ). l Defining in l = 1> 2> 3
(A.11c)
C ˆ Cp o g · gp Co C ˆm
(A.11d)
ˆl · gl · gm = g If we define
l
g ˆl =
C ˆ o g Co
from Eq. (A.11b), we obtain l
gl · gm = and
l l C ˆ Cp o C ˆ l = (A.11e) p m = m > ˆ Co C ˆm C where we can see that the relation (A.11a) is satisfied. Therefore, Eq.(A.11c) can be considered the transformation rule for the contravariant base vectors. Due to the similarity between Eqs. (A.11c) and (A.4h) the base vectors gl are called contravariant base vectors.
gl · gm =
A.3 Metric of a coordinates system
219
Fig. A.2. Covariant and contravariant base vectors
In Fig.A.2 we represent in a space 2> 3 } the distance between S and S 0 is given by dv2 = dr · dr = dl dm (gl · gm ) =
(A.14a)
jlm = jml = gl · gm
(A.14b)
We call the covariant components of the metric tensor at S in the curvilinear system {l } (this notation will be clarified in Section A.4.3.). Using Eq. (A.8), we get jlm =
C} C} = Cl Cm
(A.15a)
Defining a second curvilinear system { ˆl > l = 1> 2> 3 } and using Eq. (A.9b), we get o p C ˆ C ˆ jlm = jˆop = (A.15b) Cl Cm Equations (A.15a-A.15b) are the reason for using the name “covariant” for the metric tensor components defined in Eq. (A.14b). A.3.3 Curvilinear coordinates. Contravariant metric components The scalars defined in Eq. (A.14b) by the dot product of the covariant base vectors were named covariant components of the metric tensor. In the same way, we define j lm = j ml = gl · gm (A.16a) the contravariant components of the metric tensor at S . Using Eq. (A.11c), we get j lm =
Cl Cm op ˆ = p j o C ˆ C ˆ
(A.16b)
A.3 Metric of a coordinates system
221
The above equation is the reason for using the name “contravariant” for the metric tensor components defined in Eq. (A.16a). It is obvious that in the Cartesian system, we have = =
(A.17a)
l When {ˆ } is a Cartesian system, Eq. (A.16b) is
j lm =
Cl Cm = C} C}
(A.17b)
A.3.4 Curvilinear coordinates. Mixed metric components In any curvilinear coordinate system {l > l = 1> 2> 3 } we can define the mixed components of the metric tensor as j lm = gl · gm = lm
(A.18a)
jm l = gm · gl = lm =
(A.18b)
JJJJJ Example A.2. Any vector in 3 } to the system { ˆ > l = 1> 2> 3 }, using Eqs. (A.9b), we obtain m
v = y l gl = y l
C ˆ g ˆ = yˆm g ˆm = Cl m
(A.20a)
Hence, m
C ˆ ; m = 1> 2> 3 = (A.20b) Cl We see from the above that when the coordinate system is changed, the components y l transform following a contravariant rule. Using Eq. (A.11c), we can write yˆm = y l
m
v = yˆm g ˆ
m
C ˆ l = yˆm g = yl gl = Cl
(A.21a)
Hence, m
C ˆ ; l = 1> 2> 3 = (A.21b) Cl We see from the above that when the coordinate system is changed, the components y l transform following a covariant rule. As a conclusion to this section, we can state that the invariance of v under coordinate transformation requires the use of: yl = yˆm
• covariant components + contravariant base vectors or • contravariant components + covariant base vectors.
A.4 Tensors
223
A.4.1 Second-order tensors Generalizing the concept of vectors that we presented above, we define as second-order tensors the following mathematical entities: a = dlm gl gm = dlm gl gm = dl m gl gm = dl m gl gm
(A.22)
that remain invariant under coordinate transformations. In the above equation, we used tensorial or dyadic products between vectors (gl gm ; gl gm ; gl gm ; hwf=) that we are going to formally define in this Section. l For the transformation {l } $ {ˆ } using Eq. (A.9b), we get n
lm
a = d
lm
gl gm = d
o
C ˆ C ˆ g ˆ g ˆ = d ˆno g ˆn g ˆo = Cl Cm n o
(A.23a)
Thus, we have n
no
d ˆ
lm
= d
o
C ˆ C ˆ Cl Cm
; n> o = 1> 2> 3 =
(A.23b)
That is to say, the components dlm transform following a double contravariant rule. In the same way, we can show that d ˆno = dlm
Cl Cm n o C ˆ C ˆ
; n> o = 1> 2> 3 =
(A.23c)
That is to say, the components dlm transform following a double covariant rule. We can also show that: n
d ˆno = dl m
C ˆ Cm Cl C ˆo
d ˆo n = dml
Cm C ˆ l o C ˆ C
; n> o = 1> 2> 3
(A.23d)
; n> o = 1> 2> 3 =
(A.23e)
n
That is to say, the components dl m and dl m transform following mixed rules. From Eq. (A.22), we have dno gn go = dlm gl gm =
(A.24a)
When we postmultiply by gu on both sides (the formal definition of this operation is given in what follows), we get dno gn ou = dlm jmu gl
(A.24b)
224
Nonlinear continua
and if we now postmultiply (inner product) both sides by gv , we obtain dno ou nv = dlm jlv jmu =
(A.24c)
Finally, dvu = dlm jlv jmu
; u> v = 1> 2> 3 =
(A.24d)
In the same way, we can show the following relations for n> o = 1> 2> 3: dno = dnm jmo
(A.24e)
dno = dlm j ln j mo = dnm j mo
(A.24f)
dno = dnm jmo = dmo j mn =
(A.24g)
It is evident that we can raise and lower indices using the proper components of the metric tensor. In Eq. (A.22) and the ones that followed, we wrote dyads of the type gl gm or gl gm or gl gm or gl gm that define an operation known as the tensorial product of two vectors. To define the tensorial product of two vectors a and b (ab in our notation or a b in the notation used by other authors), we will define the properties of this new operation: • Given a scalar , (ab) = ( a)b = a( b) = ab =
(A.25a)
• Given a third vector c, (ab)c = a(bc) = abc
(A.25b)
and a(b + c) = ab + ac 6= ba + ca = (b + c) a =
(A.25c)
• In general, ab 6= ba =
(A.25d)
• The scalar product of a vector c with the dyad ab is a vector, c · (ab) = (c · a)b > where (c · a) is a scalar. Also,
(A.25e)
A.4 Tensors
225
(ab) · c = a(b · c) 6= c · (ab) = (c · a)b =
(A.25f)
It should be notd that (ab) · c is a vector with the direction of the vector a , while c · (ab) is a vector with the direction of the vector b . • The scalar or inner product between two dyads is another dyad: (ab) · (cd) = (b · c) ad =
(A.25g)
• The double scalar or inner product between two dyads is a scalar: (ab) : (cd) = (a · c) (b · d) =
(A.25h)
Besides (Malvern 1969), (ab) · · (cd) = (a · d) (b · c)
(A.25i)
which is a scalar too. Using the above definition, we can perform the scalar product of the second-order tensor a defined by Eq. (A.22) and the vector v defined by Eq. (A.19), a · v = dln yn gl = dln yn gl = dl n yn gl = dl n yn gl
(A.26a)
then, we obtain a vector b = a · v with: covariant components: el = dln y n = dl n yn contravariant components: el = dln yn = dl n yn = It is easy to show that (v · a) is also a vector and that in general v · a 6= a · v =
(A.26b)
Eigenvalues and eigenvectors of second-order tensors We say that a vector v is an eigenvector of a second-order tensor a if a · v = v
(A.27)
and we call the eigenvalue associated to the eigendirection v. It is easy to show that the following relation holds ( dlm jlm ) ym = 0 =
(A.28)
Equation (A.28) represents a system of 3 homogeneous equations (m = 1> 2> 3) with 3 unknowns (y 1 > y 2 > y 3 ) . To obtain a solution di erent from the trivial one, we must have
226
Nonlinear continua
| dlm jlm | = 0 =
(A.29)
The above is a cubic equation in that leads to 3 eigenvalues and therefore 3 associated eigendirections. It is obvious that if a pair (> v) satisfies Eq. (A.27), the pair (> v) will also do so. Hence, the modulus of the eigenvectors remains undefined. The following properties can be derived: • If a is symmetric, the eigenvalues and eigenvectors are real.
Proof. (Green & Zerna 1968) Assume is not real, then = + l y
m
m
(A.30a) m
= + l =
(A.30b)
From Eq. (A.28), equating real and imaginary parts, (dlm jlm ) m + jlm m = 0
(A.30c)
(dlm jlm ) m jlm m = 0 =
(A.30d)
After some algebra, from the two above equations, we get (jlm l m + jlm l m ) = 0
(A.30e)
for dlm = dml . Since all the l and l cannot be zero and the terms (jlm l m ) and (jlm l m ) are always positive (see Eq. (A.14a)), then = 0=
(A.30f)
Therefore, the eigenvalues are always real and to satisfy Eq. (A.28) the eigenvectors shall also be real.
• If a is symmetric, the eigenvectors form an orthogonal set.
A.4 Tensors
227
Proof. (Crandall 1956) For two pairs (1 > v1 ) and (2 > v2 ) from Eq. (A.27) v1 · a · v2 v2 · a · v1 = (2 1 ) v1 · v2 =
(A.31)
For a symmetric tensor, the l.h.s. of the above equation is zero. Hence, If 1 6= 2 then v1 · v2 = 0. That is to say, v1 and v2 are orthogonal. If 1 = 2 there are infinite vectors v1 > v2 that satisfy the above equation. Among them we can select a pair of orthogonal vectors. Hence, in general we assess that for symmetric second-order tensors, the eigenvectors are orthogonal.
JJJJJ Example A.4. As a is a symmetric second order tensor, with eigenvalues L and eigenvectors vL (L = 1> 2> 3) with |vL | = 1 , the canonical form of a is: a = 1 v1 v1 + 2 v2 v2 + 3 v3 v3 also known as the diagonalized form.
JJJJJ
A.4.2 n-order tensors In the same way that we defined the tensorial products of two vectors (dyad), we can define the tensorial product of q vectors (n-poliad ). Therefore, we can define mathematical entities of the type: t = wlm===q gl gm · · · gq = wlm===q gl gm · · · gq
(A.32)
= wlm===n op===q gl gm · · · gn go gp · · · gq which we call tensors of order q and we associate to them the property of remaining invariant when coordinate transformations are performed. When we go from the curvilinear system { l > l = 1> 2> 3 } to the curvil linear system { ˆ > l = 1> 2> 3 }, due to the invariance property, we get t = wlm===n op===q gl gm · · · gn go gp · · · gq ˆd g ˆe · · · g ˆf g ˆg g ˆh · · · g ˆi = = wˆde===fgh===i g Hence, the following relations can be derived:
(A.33a)
228
Nonlinear continua
wˆde===fgh===i = wlm===n op===q (ˆ gd · gl ) (ˆ ge · gm ) · · · (ˆ gf · g n ) gh · gp ) · · · (ˆ g i · gq ) (ˆ gg · go ) (ˆ
(A.33b)
and using Eqs. (A.9b) and (A.11c), we obtain d
e
f
C ˆ Co Cp Cq C ˆ C ˆ wˆde===fgh===i = wlm===n op===q · · · · · · = h i Cl Cm Cn C ˆg C ˆ C ˆ
(A.33c)
A.4.3 The metric tensor As a particular but important example of second-order tensors, we will refer in this section to the metric tensor, g, g = jlm gl gm = j lm gl gm = lm gl gm = ml gl gm =
(A.34)
In Sects. A.3.1 - A.3.3, we introduced the covariant, contravariant and mixed components of this tensor. We can rewrite Eq.(A.14a) as: ³ ³ ´ ´ ¢ ¡ gm gm gl gl · jno gn go · (A.35a) gv2 = gr · g · gr = and therefore,
gv2 = gl gm jno nl om = gl gm jlm =
(A.35b)
Going back to Eq. (A.34), we post-multiply both sides by the vector gs and jlm gl gm · gs = j no gn go · gs = (A.36a) Operating, we get
jlm j ms gl = j no so gn =
(A.36b)
Using Eqs. (A.15a) and (A.17b), we arrive at jlm j ms =
C} C} C} C} Cs Cm Cs = = C} C} Cl Cm Cl C} C}
(A.36c)
Rearranging,
Cs C} Cs = = sl = l C} C Cl Using the above in Eq. (A.36b), we finally obtain jlm j ms =
gs = j sn gn =
(A.36d)
(A.36e)
The above equality was also derived in Example A.2. In an identical way, we can also derive the result of the Example A.3.
A.4 Tensors
229
A.4.4 The Levi-Civita tensor The Cartesian components of the Levi-Civita or permutation tensor are defined as:
h = h
< ; @ ? 0 when two of the indices are equal 1 when the indices are arranged as 1,2,3 = = > = 1 when the indices are arranged as 1,3,2
By using the tensorial components transformation rules in an arbitrary curvilinear system { l > l = 1> 2> 3 } and for the covariant components, we get C} C} C} h = (A.37a) lmn = Cl Cm Cn Taking into account that the determinant of a (3×3) matrix can be written as: ¯ l ¯ ¯d m ¯ = huvw du1 dv2 dw3 (A.37b) it is easy to show that
hlmn |dpq | = huvw dul dvm dwn =
(A.37c)
Another important relation is h h = = get
(A.37d)
Introducing the above relation in Eq. (A.37a) and also using Eq. (A.2), we ¯ p¯ ¯ C} ¯ lmn = hlmn ¯¯ q ¯¯ = (A.37e) C In the same way, we can show that lmn
= h
lmn
¯ q¯ ¯ C ¯ ¯ ¯ ¯ C} p ¯ =
(A.38)
Some authors define the components of the permutation tensor in any curvilinear system using the same definition that we just used for the Cartesian components. In this way, the tensorial components transformation rules are not fulfilled (invariance is lost) and the permutation tensor in this case is called a pseudotensor. In a Cartesian system, we define the cross product between two vectors as e × e = h e = Taking into account that
(A.39)
230
Nonlinear continua
Co g C} o C} q = g Cq
e =
(A.40a)
e
(A.40b)
and using the above-derived curvilinear components of the Levi-Civita tensor, we get i Co Cp h q × g g (A.40c) g = 0= opq o p C} C} Considering that the above expression is valid in any curvilinear system, we obtain (A.41) go × gp = opq gq = Example A.5. JJJJJ For a second-order tensor we can write Eq. (A.29) using mixed components as: | dl m l m | = 0 = Hence, using Eq. (A.37b) £ ¤ huvw (du1 u1 ) (dv2 v2 ) (dw3 w 3 ) = 0 =
After some algebra (Flügge 1972) we get the characteristic equation of the second-order tensor a. 3 dl l 2 +
1 l m (d l d m dl m dml ) |dl m | = 0 = 2
Since the eigenvectors of a are independent of the coordinate system we use to describe the tensor, the coe!cients of the above equation are invariant against coordinate transformations. We define the invariants as: LL = dl l = dlm jlm = dlm j lm = a : g > i ¢ 1 h l m 1 ¡ LLL = d m d l dl l dmm = a · · a LL 2 > 2 2 LLLL = |dl m | > Finally, the characteristic equation can be written as: 3 LL 2 LLL LLLL = 0 = JJJJJ
A.4 Tensors
231
Example A.6. JJJJJ In a plane normal to the axis } 3 , we define an arbitrary curvilinear system { l > l = 1> 2 } with 3 = } 3 . The base vectors of the curvilinear system are C} 1 C} 2 e + e2 > 1 C1 C1 C} 1 C} 2 = e + e2 > 1 C2 C2 = e3 =
g1 = g2 g3
We define the area di erential in the plane normal to } 3 as: dA3 = d1 d2 g1 × g2 and after some algebra, we get
where |M3 |
=
³
C} 1 C1 l
dA3 = |M3 | d1 d2 e3 ´ C} 2 C} 2 C} 1 = In the particular case when the 2 1 2 C C C
curvilinear system { } is in fact a Cartesian system { }ˆl }> it is easy to show that |M3 | = 1= Therefore, dA3 = dˆ } 1 dˆ } 2 e3 = JJJJJ JJJJJ Example A.7. We define in the l = 1> 2> 3 } with the following covariant base vectors gl = We also define dY = d1 d2 d3 and after some algebra, we get
C} e = Cl h
g1 · (g2 × g3 )
i
¯ p¯ ¯ C} ¯ dY = ¯¯ q ¯¯ d1 d2 d3 = C
In the particular case when the curvilinear system { l } is in fact a Cartesian ¯ p¯ ¯ = 1= Therefore, system { }ˆl }> it is easy to show that, ¯ C} Cq dY = dˆ } 1 dˆ } 2 dˆ }3 =
JJJJJ
232
Nonlinear continua
A.5 The quotient rule Let D(lmnuv) be a set of 243 quantities, E uv the contravariant components of an arbitrary second-order tensor (independent of D(lmnuv) ) and Glmn the covariant components of a third-order tensor. If, in any coordinate system, the relation Glmn = D(lmnuv) E uv
(A.42)
is satisfied, then we are going to prove that the D(lmnuv) are the covariant components of a fifth order tensor. Proof. Since D and B are tensors, when we change the coordinate system l from { l > l = 1> 2> 3 } to { ˆ > l = 1> 2> 3 }, we get l m n ˆ opq = C Cp Cq Glmn G o C ˆ C ˆ C ˆ
E uv =
Cu Cv ˆ st = s t E C ˆ C ˆ
(A.43a) (A.43b)
Using Eqs. (A.42) and (A.43b) in Eq. (A.43a), we get l m n u v ˆ opq = C Cp Cq D(lmnuv) Cs Ct E ˆ st = G o ˆ ˆ ˆ ˆ ˆ C C C C C
(A.44a)
We can write ˆ opq = Dˆ(opqst) E ˆ st G substracting Eq. (A.44a) from Eq. (A.44b), we get " # Cl Cm Cn Cu Cv ˆ ˆ st = 0 = D(opqst) E p q s t D(lmnuv) o ˆ ˆ ˆ ˆ ˆ C C C C C
(A.44b)
(A.44c)
Since B is an arbitrary second order tensor, from the above equation, we obtain the following relation: Cl Cm Cn Cu Cv Dˆ(opqst) = p q s t D(lmnuv) = o C ˆ C ˆ C ˆ C ˆ C ˆ
(A.44d)
The above equation shows that the D(lmnuv) transform according to a covariant transformation rule that shows they are the covariant components of a fifthorder tensor.
A.6 Covariant derivatives
233
The generalization of the case that we analyzed, the quotient rule, is a tool for identifying general tensors. Example A.8. Let us consider the vectors (first-order tensors)
JJJJJ
x = {u gu y = | u gu z = }u g u = If we know that = Duvw {v | w }u is invariant under coordinate transformations (a scalar), then the quotient rule indicates that the Duvw are the mixed components of the following tensor A = Duvw gu gv gw = JJJJJ
A.6 Covariant derivatives A.6.1 Covariant derivatives of a vector Contravariant components Given a vector v, we can define it using its Cartesian components as v = y e >
(A.45a)
and since the base vectors of a Cartesian system do not change with the coordinates, we get Cv Cy = e = (A.45b) C} C} Using, in the Euclidean space, a system of arbitrary curvilinear coordinates {l > l = 1> 2> 3> }> we get v = y v gv Cgv Cv Cy v v = q = q gv + y C C Cq
(A.46a) (A.46b)
234
Nonlinear continua
Using Eq. (A.8), we obtain Cgv
C2} e Cv Cq
(A.46c)
C 2 } Cs s g = vq gs = Cv Cq C} s
(A.46d)
C
q
=
and using it once more, Cgv C
q
=
s vq is defined as the Christo el symbol of the second kind in the Euclidean space: C 2 } Cs s = = (A.47) vq Cv Cq C} It should be noted that:
• The Christo el symbol of the second kind is a function of the coordinate system under consideration { l } and of the coordinates of the point where the calculations are performed. • The Christo el symbols of the second kind are not tensorial components and therefore do not transform as such, d
d ˆef =
In general,
C 2 } C ˆ = e f C ˆ C ˆ C}
(A.48a)
d
C ˆ Cv Cq d s 6= vq = ˆef Cs C ˆe C ˆf It is obvious from Eq. (A.47) that s s = qv = vq
(A.48b)
(A.49)
It is important to note that in general Eq. (A.49) is not necessarily valid in a non-Euclidean space. = 0. • In the Cartesian coordinate system
From Eqs. (A.46b), (A.46d) and (A.47), we get ¸ Cy s Cv s v = + vq y gs = Cq Cq Defining ys |q = we can write
Cy s s + vq yv Cq
(A.50a)
(A.50b)
A.6 Covariant derivatives
v.
We call ys |q
235
Cv = y s |q gs = (A.50c) Cq the covariant derivative of the contravariant components of
We are going to show in Sect. A.7. that the ys |q are mixed components of a second-order tensor and that the subindex q, associated to the variable q , transforms in a covariant way. JJJJJ
Example A.9. Since jlm = gl · gm and using Eq. (A.46d), we get Cjlm = los jsm + mos jls = Co
JJJJJ
JJJJJ
Example A.10. From the above result, we get Cjlm Cjmo Cjol s + = los jsm + mos jsl + ml jso l o C Cm C
In the Euclidean space, jsm los
1 = 2
+ ols jsm oms jsl lms jso ³ ´ = (los + ols ) jsm + mos oms jsl ¡ s ¢ + ml lms jso = µ
Cjlm Cjmo Cjol + l o C Cm C
¶
= JJJJJ
Covariant components We are now going to perform the derivations of the previous Section but, in the present case, for a vector defined using its covariant components and contravariant base vectors, the following results
236
Nonlinear continua
Cgv Cyv v Cv = q = q g + yv C C Cq
(A.51)
Taking into account that gv · gw = vw > we get Cgw Cgv v = 0= q · gw + g · C Cq
(A.52a)
Using Eq. (A.46d) in the above, Cgv s · gw + wq gv · gs = 0 Cq
(A.52b)
and after some algebra, we have Cgv v = wq gw = Cq Therefore, Cv = Cq
Cys v yv sq Cq
We now call ys |q =
(A.52c) ¸
gs =
Cys v yv sq = Cq
(A.53a)
(A.53b)
Hence, Cv = ys |q gs = (A.53c) Cq We call ys |q the covariant derivatives of the covariant components of v. We are going to show in Sect. A.7 that the ys |q are covariant components of a second-order tensor. A.6.2 Covariant derivatives of a general tensor Given an arbitrary n-order tensor, t = wlm···n st···u gl gm · · · gn gs gt · · · gu
(A.54)
we can generalize the previous derivations, Ct = wlm===n st===u |q gl gm · · · gn gs gt · · · gu Cq
(A.55a)
where wlm===n st===u |q =
Cwlm===n st===u l m + wvm===n st===u vq + wlv===n st===u vq + Cq n v v · · · + wlm===v st===u vq wlm===n vt===u sq wlm===n sv===u tq v · · · wlm===n st===v uq
(A.55b)
A.7 Gradient of a tensor
237
is the covariant derivative of the mixed components of the tensor w. We are going to show in Sect. A.7 that the wlm···n st···u |q are mixed components of a (q + 1)-order tensor. JJJJJ
Example A.11. Using Eq.(A.55b), we get jlm |p =
Cjlm s s jsm lp jls mp Cp
and taking into account Example A.9, we get jlm |p = 0
= JJJJJ
A.7 Gradient of a tensor Let w be a general q-order tensor, t = wlm===n st===u gl gm · · · gn gs gt · · · gu =
(A.56)
We define the gradient of the tensor w as: u t = gq
i C h lm===n s t u g g · · · g g g · · · g w = st===u l m n Cq
(A.57)
Using the quotient rule and taking into account that due to the definition of gradient, g t = gr · u t (A.58)
and that gt is an q-order tensor while gr = gq gq is a vector, we conclude that u t is a (q + 1)-order tensor. Using Eq. (A.55a), we can rewrite Eq. (A.57) as: u t = wlm===n st===u |q gq gl gm · · · gn gs gt · · · gu =
(A.59)
Therefore, the wlm===n st===u |q are mixed components of a (q + 1)-order tensor. In the particular case of t being a vector, it is now evident that y s |q are mixed components and the ys |q are covariant components of the second-order tensor, then uv = y s |q gq gs = ys |q gq gs = (A.60)
238
Nonlinear continua
Example A.12. JJJJJ We are going to show that if the components of a given tensor t are constant in a Cartesian system, then in any curvilinear coordinate system in the Euclidean space, the covariant derivatives of the components of t are zero. In a Cartesian system { }ˆ }, using Eq. (A.59), we get C wˆ=== === e e e · · · e e e · · · e C }ˆ ( e = e in a Cartesian system). If the Cartesian components of w are constant, ut =
C wˆ=== === = 0= C }ˆ Hence, we get ut = 0
=
Since the above is a tensorial equation, it has to be fulfilled in any coordinate system. In particular, in a system { l } wlm===n st===u |q = 0 =
JJJJJ
A.8 Divergence of a tensor Let t be a general q-order tensor, t = wlm===n st===u gl gm · · · gn gs gt · · · gu >
(A.61)
we define the divergence of the tensor w as: h i C lm===n s t u · w g g · · · g g g · · · g = (A.62a) u · t = gq st===u l m n Cq After some algebra, we get u · t = wlm===n st===u |l gm · · · gn gs gt · · · gu =
(A.62b)
When we write t as t = wl m===n st===u gl gm · · · gn gs gt · · · gu
(A.63a)
its divergence is u · t = j ql wl m===n st===u |q gm · · · gn gs gt · · · gu =
(A.63b)
The divergence of an q-order tensor is a (q 1)-order tensor. In the particular case of a vector, u · v = y q |q = j ql yl |q > the divergence of a vector is a scalar.
(A.64)
A.9 Laplacian of a tensor
239
A.9 Laplacian of a tensor Let t be a general q-order tensor, t = wlm===n st===u gl gm · · · gn gs gt · · · gu
(A.65)
we define the Laplacian of the tensor t as u2 t = u · u t =
(A.66)
Using Eqs. (A.59) and (A.62a-A.62b) and after lengthy algebra, we obtain u2 t = wlm===n st===u |qo j qo gl gm · · · gn gs gt · · · gu
(A.67a)
where wlm===n st===u |qo =
l C 2 wlm===n st===u Cwvm===n st===u l Cvq vm===n + + w st===u vq Cq Co Co Co
+
m Cvq Cwlv===n st===u m lv===n + w + st===u vq Co Co
+
n Cwlm===v st===u n Cwlm===n vt===u v Cvq vq + wlm===v st===u sq o o C C Co
wlm===n vt===u ···
v Csq
Co
···
(A.67b)
v Ctq Cwlm===n sv===u v lm===n w sv===u tq Co Co
v Cwlm===n st===v v Cuq lm===n v w wlm===n st===u |v qo st===v uq Co Co
+ wvm===n st===u |q vol + wlv===n st===u |q vom + · · · + wlm===v st===u |q von v v v wlm===n vt===u |q so wlm===n sv===u |q to · · · wlm===n st===v |q uo =
The Laplacian of a q-order tensor is another q-order tensor. Example A.13. JJJJJ In the same way we proved the lemma in Example A.12 we can show that if the components of a given tensor t in a Cartesian { }ˆ } system have zero second derivatives, i.e. C 2 wˆ=== === = 0 C} C} then in any curvilinear coordinate system {l } in the Euclidean space, we get wlm===n st===u |qo = 0 = JJJJJ
240
Nonlinear continua
A.10 Rotor of a tensor Let t be a general q-order tensor, t = wlm===n st===u gl gm · · · gn gs gt · · · gu >
(A.68)
we define the rotor of the tensor t as: h i C u × t = gq q × wlm===n st===u gl gm · · · gn gs gt · · · gu (A.69a) C = gq × wlm===n st===u |q gl gm · · · gn gs gt · · · gu =
Using Eq. (A.41), u × t = %qlp wlm·n st·u |o j qo gp gm · · · gn gs gt · · · gu =
(A.69b)
The rotor of a qorder tensor is another qorder tensor. In the particular case of a vector u × v = %lmn y m |q j ql gn = %lmn ym |l gn >
(A.70)
the rotor of a vector is a vector.
A.11 The Riemann-Christo el tensor Using Eqs. (A.67a-A.67b) to calculate the Laplacian of an arbitrary vector v, we obtain: u2 v = y l |qo j qo gl (A.71a) where yl |qo =
C 2 yl Cy v l Cy l v + (A.71b) vq Cv qo Cq Co Co ¸ l Cvq Cy v l s l s l + vs qo + vq so yv = + Cq vo Co
Using the quotient rule it is easy to show that the y l |qo are the mixed components of a third-order tensor. v v Since we are working in the Euclidean space where qo = oq (Eq.(A.49)), we write ¸ l Cvq Cvol l l w l w l y |qo y |oq = + vq wo vo wq yv = (A.72a) Cq Co Using again the quotient rule, we realize that the term between brackets on the r.h.s. of the above equation contains the mixed components (one
A.11 The Riemann-Christo el tensor
241
contravariant index and three covariant ones) of a fourth-order tensor: the Riemmann-Christo el tensor (R). Hence, y l |qo y l |oq = Uvl oq y v =
(A.72b)
In any Cartesian system, we have y | =
C 2 y C} C}
(A.73a)
y | =
C 2 y = y | C} C}
(A.73b)
and therefore, using the result in Example A.13, in any curvilinear system in the Euclidean space, we have y l |qo y l |oq = 0 =
(A.73c)
Uvl oq = 0 >
(A.73d)
Therefore, that is to say, in the Euclidean space, R = 0=
(A.74)
In the Euclidean space, we can also prove that the following relation holds yl |qo yl |oq = Uvlqo yv
(A.75a)
where
v Clov Clq v w + wq low wov lq = (A.75b) q o C C We can use the metric tensor components to lower the contravariant index; hence, Ulmno = jvl Uvmno = (A.76a)
Uvlqo =
Therefore, Ulmno = jvl
Cmov Cn
v Cmn
Co
v w + wn mow wov mn
¸
=
(A.76b)
We now define the Christo el symbol of the first kind, lmn , as: lmn = jvn lmv lmv = j vn lmn using the above in Eq. (A.76b) we get,
(A.77a) (A.77b)
242
Nonlinear continua
¸ Cjvl Ulmno vol = vnl + Co (A.77c) It is very important to realize that Eqs.(A.77a) and (A.77b) are not standard operations to go from contravariant tensorial components to covariant tensorial components and vice versa because we have already established that the Christo el symbols are not tensorial components. The result in Example A.9 can now be rewritten as: Cmol Cmnl = + mov n C Co
Cjvl Cn
¸
v mn
Cjvl = vol + lov = Co
(A.77d)
Using the above in Eq. (A.77c) and taking into account that in the Euclidean space lov = olv , we get Ulmno =
Cmol Cmnl v mov nlv + mn olv = n C Co
(A.77e)
In what follows, we will prove the identities: (l) Ulmno = Ulmon >
(A.78a)
(ll) Ulmno = Umlno >
(A.78b)
(lll) Ulmno =
Unolm =
(A.78c)
(i) Ulmno = Ulmon Using Eq. (A.77e), we write Cmol Cmnl v mov nlv + mn olv n C Co ¸ Cmnl Cmol v v = + mn olv mo nlv Co Cn
Ulmno =
= Ulmon =
(A.79a)
(ii) Ulmno = Umlno v Since we are working in the Euclidean space, lmv = ml and lmn = mln . Also, we can rewrite the result of Example A.10 as: ¶ µ 1 Cjef Cjde Cjdf def = + = (A.79b) 2 Cd Cf Ce Using the above in Eq.(A.77e), we obtain, after some algebra:
A.12 The Bianchi identity
Ulmno =
1 2
C 2 jmn C 2 jmo C 2 jnl C 2 jol + Cm Cn Cl Co Cl Cn Cm Co
+ j vd [ mnd olv mod nlv ] =
243
¸ (A.79c)
Changing the order of the indices, we obtain ¸ 1 C 2 jln C 2 jlo C 2 jnm C 2 jom Umlno = + 2 Cl Cn Cm Co Cm Cn Cl Co
+ j vd [ lnd omv lod nmv ] ¸ 1 C 2 jol C 2 jmn C 2 jmo C 2 jnl = + 2 Cm Cn Cl Co Cl Cn Cm Co j vd [ old mnv nld mov ]
= Ulmno =
(A.79d)
(iii) Ulmno = Unolm Using Eq. (A.79c), we can write ¸ 2 1 C 2 jol C 2 jom C 2 jln C jmn + Unolm = 2 Co Cl Cn Cm Cn Cl Co Cm + j vd [ old mnv omd lnv ] ¸ 1 C 2 jmn C 2 jmo C 2 jnl C 2 jol = + 2 Cm Cn Cl Co Cl Cn Cm Co + j vd [ mnv old mod nlv ]
= Ulmno =
(A.79e)
A.12 The Bianchi identity A second-order tensor g can be considered a metric tensor in a Euclidean space if it fulfills the set of equations Ulmno = 0, derived from Eq.(A.74). However, between those equations, certain relations exist that we are going to demonstrate in this Section. Using Eq. (A.55b), we can write Ul mno |p =
CUl mno l v + Uvmno vp Ul vno mp Cp v v Ul mvo np Ul mnv op >
and with the help of Eq. (A.75b), we get, in the Euclidean space,
(A.80a)
244
Nonlinear continua
Ul mno |p =
C 2 mol Cn Cp
l C 2 mn
Co Cp
+
l Cmov Cvn v l + vn Cp mo Cp
v v Cmov l Cmn Cmn Cl p v l C mn vol + vp vp vo Cp Cn Co
v l w l + wn mow vp wov mn vp
l Cvol v Cvn v + mp mp Cn Co
l v w v wn vow mp + wol vn mp
l Cmol v Cmv v np v np + C Co
l v w v wv mow np + wol mv np
l Cmv
Cn
v op +
l w v l w v wn mv op + wv mn op =
l Cmn v Cv op
(A.80b)
We can develop similar expressions for Ul mop |n and Ul mpn |o and rememd d bering that in the Euclidean space ef = fe > we finally obtain the Bianchi identity: Ul mno |p + Ul mop |n + Ul mpn |o = 0 = (A.81) Starting from,
Ulmno = jsl Usmno
(A.82a)
and using the result in Example A.11, we have Ulmno |p = jsl Usmno |p =
(A.82b)
Hence, Ulmno |p + Ulmop |n + Ulmpn |o = jsl
³
´ Usmno |p + Usmop |n + Usmpn |o (A.82c)
and using Eq.(A.81), we get Ulmno |p + Ulmop |n + Ulmpn |o = 0 =
(A.82d)
It is worth noting that the Bianchi identities are not restricted to Euclidean spaces and can be demonstrated in other spaces in which the second Christo el symbol is also symmetric (e.g. Riemmanian spaces (McConnell 1957)).
A.13 Physical components In an arbitrary curvilinear system { l }> we can write the q-order tensor t , using its contravariant components and the covariant base vectors, t = wlm===n gl gm · · · gn =
(A.83)
A.13 Physical components
245
In general, the covariant base vectors: (l) Do not have a unitary modulus. (ll) Are not dimensionally homogeneous. Example A.14. JJJJJ In a cylindrical coordinate system where 1 is the radius, 2 the polar angle and 3 } 3 ,we can write g1 = cos 2 e1 + sin 2 e2 g2 = 1 sin 2 e1 + 1 cos 2 e2 g3 = e3 = Therefore, ¯ ¯ ¯ ¯ ¯g1 ¯ = 1 ¯ ¯ ¯ ¯ ¯g2 ¯ = 1 ¯ ¯ ¯ ¯ ¯g3 ¯ = 1
which are obviously not dimensionally homogeneous.
JJJJJ
We can rewrite Eq. (A.83) as: t =
3 3 X X l=1
m=1
···
3 X
n=1
wlm===n
gm g g s s s jll jmm · · · jnn s l s ··· s n = jll jmm jnn
(A.84a) In the above equation, we did not use the summation convention to avoid misinterpretations. Obviously, ¯ ¯ ¯ gl ¯ ¯ s ¯ (A.84b) ¯ jll ¯ = 1 > and therefore the terms w?lm===nA = wlm===n
s s s jll jmm · · · jnn
( qr dgglwlrq rq l> m = = = n) (A.84c)
are the projections of the tensor w on base vectors of unitary modulus. The terms w?lm===nA are known as the physical components of the tensor w. It is obvious that the above-defined physical components are not tensorial components and therefore, when the coordinate system is changed the physical components cannot be transformed using either a covariant or a contravariant transformation rule.
B References
Anand, L. (1979), “On Hencky’s approximate strain-energy functions for moderate deformation”, J. Appl. Mech., 46, 78-82. Aris, R. (1962), Vectors, Tensors, and the Basic Equations of Fluid Mechanics, Prentice Hall, Englewood-Cli s, New Jersey. Atluri, S.N. (1984), “Alternate stress and conjugate strain measures, and mixed variational formulations involving rigid rotations for computational analysis of finitely deformed solids, with applications to plates and shells - Part I”, Comput. & Struct. , 18, 93-116. Backofen, W.A. (1972), Deformation Processing, Addison-Wesley, Reading MA. Bathe, K.J. (1996), Finite Element Procedures, Prentice Hall, Upper Saddle River, New Jersey. Bathe, K.J. & E.N.Dvorkin (1985), “A four-node plate bending element based on Mindlin / Reissner plate theory and a mixed interpolation”, Int. J. Numerical Methods in Engng., 21, 367-383. Bathe, K.J. & E.N.Dvorkin (1986), “A formulation of general shell elements the use of mixed interpolation of tensorial components”, Int. J. Numerical Methods in Engng., 22, 697-722. Baˇzant, Z.P. (1979), Advanced Topics in Inelasticity and Failure of Concrete, Swedish Cement and Concrete Research Institute, Stockholm. Belytschko, T., W.K. Liu & B. Moran (2000), Nonlinear Finite Elements for Continua and Structures, John Wiley & Sons, Ba!ns Lane. Boley, B.A. & J.H. Weiner (1960), Theory of Thermal Stresses, John Wiley and Sons. Brush, D.O. & B.O. Almroth (1975), Buckling of Bars, Plates and Shells, McGraw-Hill. Cavaliere, M.A., M.B. Goldschmit & E.N. Dvorkin (2001a), “Finite element simulation of the steel plates hot rolling process”, Int. J. Num. Methods Eng., 52, 1411-1430.
248
Nonlinear continua
Cavaliere, M.A., M.B. Goldschmit & E.N. Dvorkin (2001b), “Finite element analysis of steel rolling processes”, Comput. Struct., 79, 2075-2089. Chapelle, D. & K.J. Bathe (2003), The Finite Element Analysis of Shells Fundamentals, Springer-Verlag, Berlin Heidelberg. Chen, W.F. (1982), Plasticity in Reinforced Croncrete, Mc Graw Hill, New York. Cheng, Y.M. & Y. Tsui (1990), “Limitations to the large strain theory”, Int. J. Num. Methods Eng., 33, 101-114. Crandall, S.H. (1956), Engineering Analysis, McGraw-Hill, New York. Dienes, J.K. (1979), “ On the analysis of rotation and stress rate in deforming bodies”, Acta Mech., 32, 217-232. Dieter, G.E. (1986), Mechanical Metallurgy, McGraw-Hill, New York. Dvorkin, E.N. (1995a), “On finite strain elasto-plastic analysis of shells”, Proceedings of the Fourth Pan American Congress of Applied Mechanics, (Ed. L. Godoy et al.), Buenos Aires, Argentina, 353-538. Dvorkin, E.N. (1995b), “MITC elements for finite strain elasto-plastic analysis”, Proceedings of the Fourth International Conference on Computational Plasticity, (Ed. E. Oñate et al.), Barcelona, Spain, 273-292. Dvorkin, E.N. (1995c), “Non-linear analysis of shells using the MITC formulation”, Arch. Comput. Methods Eng., 2, 1-56. Dvorkin, E.N. (2001), “Computational modelling for the steel industry at CINI”, IACM-Expressions, 10. Dvorkin, E.N. & A.P. Assanelli (2000), “Implementation and stability analysis of the QMITC-TLH elasto-plastic (2D) element formulation”, Comp. Struct., 75, 305-312. Dvorkin, E.N. & K.J. Bathe (1994), “A continuum mechanics based four-node shell element for general nonlinear analysis”, Eng. Comput., 1, 77-88. Dvorkin, E.N., M.A. Cavaliere & M.B. Goldschmit (1995), “A three field element via augmented Lagrangian for modelling bulk metal forming processes”, Computat. Mech., 17, 2-9. Dvorkin, E.N., M.A. Cavaliere & M.B. Goldschmit (2003), “Finite element models in the steel industry. Part I: simulation of flat products manufacturing processes”, Comp. Struct., 81, 559-573. Dvorkin, E.N., M.A. Cavaliere, M.B. Goldschmit & P.M. Amenta (1998), “On the modeling of steel product rolling processes”, Int. J. Forming Processes (ESAFORM), 1, 211-242. Dvorkin, E.N., M.A. Cavaliere, M.B. Goldschmit, O.Marini & W.Stroppiana (1997), “2D finite element parametric studies of the flat rolling process”, J. Mater. Proc. Technol., 68, 99-107.
References
249
Dvorkin, E.N., A. Cuitiño & G. Gioia (1989), “A concrete material model based on non-associated plasticity and fracture”, Eng. Comput., 6, 281294. Dvorkin, E.N., M.B. Goldschmit, D. Pantuso & E.A. Repetto (1994), “Comentarios sobre algunas herramientas utilizadas en la resolución de problemas no-lineales de mecánica del continuo”, Rev. Int. Met. Numéricos Cálculo Diseño Ing., 10, 47-65. Dvorkin, E.N., D. Pantuso & E.A. Repetto (1992), “2D finite strain elastoplastic analysis using a quadrilateral element based on mixed interpolation of tensorial components”, Proceedings of the International Congress on Numerical Methods in Engineering and Applied Sciences, (Ed. H. Alder et al.), Concepción, Chile, 144-157. Dvorkin, E.N., D. Pantuso & E.A. Repetto (1993), “Finite strain elastoplastic analysis interpolating Hencky strains and displacements”, Proceedings of the Third Pan American Congress of Applied Mechanics, (Ed. M. Crespoda Silva et al.), São Paulo, Brazil, 271-274. Dvorkin, E.N., D. Pantuso & E.A. Repetto (1994), “A finite element formulation for finite strain elasto-plastic analysis based on mixed interpolation of tensorial components”, Comput. Methods Appl. Mech. Eng., 114, 35-54. Dvorkin, E.N., D. Pantuso & E.A. Repetto (1995), “A formulation of the MITC4 shell element for finite strain elasto-plastic analysis”, Comput. Methods Appl. Mech. Eng., 125, 17-40. Dvorkin, E.N. & E.G. Petöcz (1993), “An e ective technique for modelling 2D metal forming processes using an Eulerian formulation”, Eng. Comput., 10, 323-336. Dvorkin, E.N. & S.I. Vassolo (1989), “A quadrilateral 2D finite element based on mixed interpolation of tensorial components”, Eng. Comput., 6, 217224. Eringen, A.C. (1967), Mechanics of Continua, Wiley, New York. Eterovic, A.L. & K.J. Bathe (1990), “A hyperelastic based large strain elastoplastic constitutive formulation with combined isotropic kinematic hardening using the logarithmic stress and strain measures”, Int. J. Num. Meth. Engrg., 30, 1099-1114. Flügge, W. (1972), Tensor Analysis and Continuum Mechanics, SpringerVerlag, Berlin. Fraeijs de Veubeke, B. F. (2001) “Displacement and equilibrium models in the finite element method”, Reprinted in Int. J. Num. Meth. Engng., 52, 287-342. Fung, Y.C. (1965), Foundations of Solid Mechanics, Prentice Hall, EnglewoodCli s, New Jersey. Fung, Y.C. & P. Tong (2001), Classical and Computational Solid Mechanics, World Scientific, Singapore.
250
Nonlinear continua
Green, A.E. & W. Zerna (1968), Theoretical Elasticity, 2nd. edn., Oxford University Press. Hildebrand, F.B. (1976), Advanced Calculus for Applications, 2nd. edn., Prentice Hall, Englewood-Cli s, New Jersey. Hill, R. (1950), The Mathematical Theory of Plasticity, Oxford University Press. Hill, R. (1978), “Aspects of invariance in solid mechanics”, Adv. Appl. Mechs., 18, 1-75. Hodge, P.G., K.J. Bathe & E.N. Dvorkin (1986), “Causes and consequences of nonuniqueness in an elastic/perfectly plastic truss”, ASME, J. Appl. Mech., 53, 235-241. Ho , N.J. (1956), The Analysis of Structuress, Wiley. Johnson, W. & P.B. Mellor (1973), Engineering Plasticity, Van Nostrand Reinhold Co., London. Kobayashi, S., S.-I. Oh & T. Altan (1989), Metal Forming and the Finite Element Method, Oxford University Press. Koji´c, M., & K.J. Bathe (2005), Inelastic Analysis of Solids and Structures, Springer-Verlag, Berlin Heidelberg. Lamaitre, J. & J.-L. Chaboche (1990), Mechanics of Solid Materials, Cambridge University Press. Lanczos, C. (1986), The Variational Principles of Mechanics, Dover, Mineola, N.Y.. Lang, S. (1972), Di erential Manifolds, Addison-Wesley, MA. Lee, E.H. (1969), “Elastic-plastic deformations at finite strains”, J. Appl. Mech., 36, 1-6. Lee, E.H. & D.T. Liu (1967), “Finite strain elastic-plastic theory with application to plane-wave analysis”, J. Appl. Phys., 38, 19-29. Love, A.E.H. (1944), A Treatise on the Mathematical Theory of Elasticity, Dover, New York. Lubliner, J. (1985), Thermomechanics of Deformable Bodies, Dept. of Civil Eng., University of California at Berkeley. Lubliner, J. (1990), Plasticity Theory, Macmillan, New York. Luenberger, D.G. (1984), Linear and Nonlinear Programming, Wiley, Reading MA. Malvern, L.E. (1969), Introduction to the Mechanics of a Continuous Medium, Prentice Hall, Englewood Cli s, New Jersey. Marsden, J.E. & T.J.R. Hughes (1983), Mathematical Foundations of Elasticity, Prentice Hall, Englewood-Cli s, New Jersey. McClintock, F. & A. Argon (1966), Mechanical Behavior of Materials, Addison Wesley.
References
251
McConnell, A.J. (1957), Applications of Tensor Analysis, Dover Publications Inc., New York. Mendelson, A. (1968), Plasticity: Theory and Applications, Macmillan, New York. Moran, B., M. Ortiz & C.F. Shih (1990), “Formulation of implicit finite element method for multiplicative finite deformation plasticity”, Int. J. Num. Methods Eng., 29, 483-514. Oden J.T. (1979), Applied Functional Analysis, Prentice Hall, EnglewoodCli s, New Jersey. Oden, J.T. & J.N. Reddy (1976), Variational Methods in Theoretical Mechanics, Springer-Verlag, Berlín. Ogden, R.W. (1984), Non-Linear Elastic Deformations, Dover, Mineola, N.Y.. Ottosen, N.S. (1986), “Thermodynamic consequences of strain softening in tension”, J. Eng. Mech., ASCE, 112, 1152-1164. Panton, R.L. (1984), Incompressible Flow, Wiley, New York. Pèric, D., D.R.J. Owen & M.E. Honnor (1992), “A model for finite strain elasto-plasticity based on logarithmic strains: Computational issues”, Comput. Methods Appl. Mech. Eng., 94, 35-61. Perzyna, P. (1966), “Fundamental problems in viscoplasticity”, Adv. Appl. Mech., 9, Academic Press, New York. Pian, T.H.H. & P. Tong (1969), “Basis of finite element methods for solid continua”, Int. J. Num. Methods Eng., 1, 3-28. Pijaudier-Cabot , G., Z.P. Baˇzant & M. Tabbara (1988), “Comparison of various models for strain-softening”, Eng. Comput., 5, 141-150. Pinsky, P.M., M. Ortiz & K.S. Pister (1983), “Numerical integration of rate constitutive equations in finite deformation analysis”, Comput. Methods Appl. Mech. Eng., 40, 137-158. Pipkin, A.C. (1972), Lectures on Viscoelasticity Theory, Springer-Verlag, New York. Rolph III, W.D. & K.J. Bathe (1984), “On a large strain finite element formulation for elasto-plastic analysis”, in: K. J. Willan, Constitutive Equations: Macro and Computational Aspects, Winter Annual Meeting, ASME, New York, 131-147. Santaló, L.A. (1961), Vectores y Tensores con sus Aplicaciones, EUDEBA, Buenos Aires. Schweizerhof, K. & E. Ramm (1984), “Displacement dependent pressure loads in nonlinear finite element analyses”, Comput. Struct., 18, 1099 - 1114. Segel, L.A. (1987), Mathematics Applied to Continuum Mechanics, Dover, Mineola, N.Y..
252
Nonlinear continua
Simo, J.C. (1988), “A framework for finite strain elasto-plasticity based on maximum plastic dissipation and the multiplicative decomposition”. “Part I: Continuum formulation”, Comput. Methods Appl. Mech. Engrg., 66, 199-219. “Part II: Computational aspects”, Comput. Methods Appl. Mech. Eng., 68, 1-31. Simo, J.C. (1991), “Algorithms for static and dynamic plasticity that preserve the classical return mapping schemes of the infinitesimal theory”, SUDAM Report 91-4, Stanford University, Stanford, California. Simo, J.C. & T.J.R. Hughes (1986), “On the variational foundations of assumed strain methods”, J. Appl. Mechs., ASME, 53, 51-54. Simo, J.C. & T.J.R. Hughes (1998), Computational Inelasticity, SpringerVerlag, New York. Simo, J.C. & J.E. Marsden (1984), “On the rotated stress tensor and the material version of the Doyle-Ericksen formula”, Arch. Rat. Mechs. Anal., 86, 213-231. Simo, J.C. & M. Ortiz (1985), “A unified approach to finite deformation elastoplastic analysis based on the use of hyperelastic constitutive equations”, Comput. Methods Appl. Mech. Eng., 49, 221-245. Simo, J.C. & K.S. Pister (1984), “Remarks on rate constitutive equations for finite deformation problems: Computational aspects”, Comput. Methods Appl. Mech. Eng., 46, 201-215. Simo, J.C. & R. L. Taylor (1991), “Quasi-incompressible finite elasticity in principal stretches. Continuum basis and numerical algorithms”, Comput. Methods Appl. Mech. Eng., 85, 273-310. Slattery, J.C. (1972), Momentum, Energy and Mass Transfer in Continua, McGraw-Hill, New York. Snyder, M.D. (1980), An e ective solution algorithm for finite element thermoelastic-plastic and creep analysis, Ph.D. Thesis, Department of Mechanical Engineering, Massachusetts Institute of Technology. Sokolniko , I.S. (1956), Mathematical Theory of Elasticity, McGraw-Hill. Sokolniko , I.S. (1964), Tensorial Analysis, Wiley & Sons. Strang, G. (1980), Linear Algebra and its Applications, 2nd. edn., Academic Press, New York. Synge, J.L. & A. Schild (1949), Tensor Calculus, Dover Publications Inc., New York. Thorpe, J.F. (1962), “On the momentum theorem for a continuous system of variable mass”, Am. J. Phys., 30. Truesdell, C. (1966), The Elements of Continuum Mechanics, Springer-Verlag, Berlin. Truesdell, C. & W. Noll (1965), “The non-linear field theories of mechanics”, Encyclopedia of Physics, III/3, (Ed. S. Flügge), Springer-Verlag, Berlin.
References
253
Truesdell, C. & R. Toupin (1960), “The classical field theories”, Encyclopedia of Physics, III/1, (Ed. S. Flügge), Springer-Verlag, Berlín. Vermeer, P.A. & R. de Borst (1984), “Non-associated plasticity for soils, concrete and rock”, Heron, 29, 3. Washizu, K. (1982), Variational Methods in Elasticity and Plasticity, Pergamon Press, Oxford. Weber, G. & L. Anand (1990), “Finite deformation constitutive equations and a time integration procedure for isotropic, hyper-elastic viscoplastic solids”, Comput. Methods Appl. Mech. Eng., 79, 173-202. Zienkiewicz, O.C., P.C. Jain & E. Oñate (1977), “Flow of solids during forming and extrusion: some aspects of numerical solutions”, Int. J. Solid Struct., 14, 15-28.
Index
acceleration, 10 convected, 104 material, 11 admissible displacements, 184 admissible transformation, 213 Almansi deformation tensor, 35, 49, 58 pull-back, 43 associated plastic flow, see associative plastic flow associative plastic flow, 144 back-stress tensor, 142, 161 balance of energy, 109 Eulerian (spatial) formulation, 109 Lagrangian (material) formulation, 112 localized material form, 112 localized spatial form, 111 balance of moment of momentum, 105 Eulerial (spatial) formulation, 105 localized spatial form, 107 symmetry of stress measures, 107 balance of momentum Eulerian (spatial) formulation, 96 Lagrangian (material) formulation, 103 localized material form, 104 localized spatial form, 97 balance of momentum principle, 95 balance principles, 85 base vectors, 216 contravariant, 218 covariant, 216 Bernstein formula, 157
Bianchi identity, 243 body-attached loads, 187 Bridgman experimental observations, 140, 144 buckling, 188, 199 Cartesian coordinates, 5, 213 Cauchy elastic material, see elastic material model Cauchy stress tensor, 69—72, 78 symmetry, 107 Cauchy Theorem, 71 chemical energy, 109 classical objectivity, see objectivity Clausius-Duhem inequality, 162 compatibility, 61 configuration reference, 8, 10, 11, 22, 33—35 spatial, 10, 11, 25, 33, 35 configurations, 7 conjugate stress/strain rate measures, 72 consecutive rotations, 52 conservative loads, 195, 197 consistency equation, 150, 170 constant direction load, 187 constitutive relations, 115 continuity equation, 93 continuous body, 7 continuous media hypothesis, 7 kinematics, 7 contravariant transformation rule, 214 control surface, 88
256
Index
control volume, 88 convex yield surface, 142 coordinates convected, 13, 34 Eulerian, 52 fixed Cartesian, 11 Lagrangian, 52 material, 8, 14 spatial, 8, 11, 14 coordinates transformation, 213 corotational stress rate, 84 covariance, 44, 49 covariant derivative, 233 of a general tensor, 236 of a vector, 233 covariant rates, 58 covariant transformation rule, 215 cross product between vectors, 229 curvilinear coordinates, 5, 213
elastoplastic material model 1D case, 135 finite strains, 155 general formulation, 140 infinitesimal strains, 135 thermal e ects, 170 energy conjugate, 73, 75, 76, 79 energy dissipation, 162 entropy, 167 equilibrium, see balance of momentum principle equipresence, 116 equivalent plastic strain, 153 equivalent plastic strain rate, 152 equivalent stress, 152 essential boundary conditions, 205 Euclidean space, 62, 213 event, 45 fiber, 14 Finger deformation tensor, 25, 33, 58 first law of Thermodynamics, see balance of energy flow rule, 140, 142, 144, 177 follower load, 187 forces concentrated, 70 external, 67 internal, 67 per unit mass, 68 surface, 68 Fourier’s law, 169 free energy, 162, 165 frictional material, 148
damage mechanics, 115 decomposition left polar, 25 multiplicative, 23, 25 polar, 21 numerical algorithm, 28 right polar, 22 deformation gradient tensor, 13, 47 inverse, 14 multiplicative decomposition, 158 transpose, 14 density, 9 deviatoric components Cauchy stress tensor, 141 Green-Lagrange strain tensor, 126 displacement vector, 9 distribuited torques, 69 divergence of a tensor, 238 Doyle-Ericksen formula, 122 Drucker’s postulate, 142, 144, 145, 147 dyads, 224
generalized Gauss’ theorem, 88 gradient of a tensor, 237 Green deformation tensor, 21, 33 Green elastic material, see hyperelastic material model Green-Lagrange strain tensor, 34, 48 Green-Naghdi stress rate, 84
eigenvalues, 28—33 eigenvectors, 28—33, 230 elastic energy, 109, 120 elastic material model, 120 elasticity tensor, 123 spatial, 123 symmetries, 124
hardening law, 135, 140, 151, 162, 172, 175 heat flux, 110 heat source, 110 Helmholtz’s free energy, 167 Hencky strain tensor, 35, 56, 161 time derivative, 79
Index homeomorphism, 8 hydrostatic component Cauchy stress tensor, 141 hyperelastic material model, 120 hyperelasticity, 115, 120 hypoelastic material model, 121, 155 incompressible flow, 180 incremental formulation, 164, 189 infinitesimal strain tensor, 65 instant, 7 internal energy, 109 isocoric deformation, 21 isometric transformation, 45 isotropic hardening, 151, 161, 172 isotropic materials, 125 J2 -yield function, see von Mises yield function Jacobian, 213 of the transformation, 19 time rate, 86 Jaumann stress rate, 84 jump discontinuity, 90 condition, 93 kinematic constraints, 207, 209 kinematic evolution, 50 kinematic hardening, 151, 154, 161, 170, 175 kinetic energy, 73 Kirchho stress tensor, 74, 82, 84 Kotchine’s theorem, 93 Lagrange criterion, 88 Lagrange multipliers, 207 physical interpretation, 208 Lagrangian system, 51 Laplacian of a tensor, 239 Lee’s multiplicative decomposition, 158 Left Cauchy-Green deformation tensor, see Finger deformation tensor left stretch tensor, 25, 28, 48 physical interpretation, 26 pull-back, 43 Levi-Civita tensor, 229 Lie derivative, 56, 58, 82, 84 local action, 117 Logarithmic strain tensor, see Hencky strain tensor
257
mapping, 8 mass, 9 mass-conservation principle, 74, 93 Eulerian (spatial) formulation, 93 Lagrangian (material) formulation, 95 localized material form, 95 localized spatial form, 93 material isotropic, 79, 81 material derivative, 12 material particle, 7, 14 material surface, 88 material time derivative, 11, 12 material-frame indi erence, 116 mathematical model, 2 linear, 2 nonlinear, 2 metric, 219 Cartesian coordinates, 220 curvilinear coordinates, 220 metric tensor, 15, 57, 220, 228 contravariant components, 220 covariant components, 220 mixed components, 221 pull-backs of the spatial, 43 push-forward of the reference, 44 minimum potential energy principle, 197 momentum conservation principle, see balance of momentum principle Mooney-Rivlin material model, 131 motion, 8, 14 continuous body, 9, 10 Eulerian description, 11, 12 Lagrangian description, 10—12 regular, 8 moving control volume energy conservation, 111 mass conservation, 94 momentum conservation, 99 multiplicative decomposition of the deformation gradient, 158 n-poliad, 227 Nanson formula, 100 natural boundary conditions, 203, 205, 207
258
Index
neo-Hookean material model, 131—133 Newtonian fluids, 180 no-slip condition, 181 nonassociated plasticity, 144, 149, 151 nonconservative loads, 198 nonconvex yield surface, 147 nonpolar media, 70 notation, 5 numerical model, 2 objective physical law, 50 rates, 58 stress rate, 61, 81 objectivity, 44 classical, 47 criteria, 47 observation frame, see reference frame Ogden hyperelastic material model, 129 Oldroyd stress rate, 81, 82 orthotropic material, 125 perfect fluid, 98 Euler equation, 98 perfectly plastic material, 147 permanent deformations, see plastic deformations permutation tensor, see Levi-Civita tensor physical components, 244 physical phenomena observation, 1 quantification, 1 Piola identity, 102 Piola Kirchho stress tensor first symmetry, 107 second symmetry, 107 Piola-Kirchho stress tensor first, 74 second, 76, 83 plastic deformation, 135 plastic dissipation, 143, 164 maximization, 143, 164 Kuhn-Tucker conditions, 143, 164 plasticity, 115 point, see material particle polar decomposition, see decomposition
polar media, 70 postbuckling, 201 potential energy, 195 power, 72 principle of maximum plastic dissipation, 143 principle of stationary potential energy, 195 principle of virtual power, 194 principle of virtual work, 183 geometrically nonlinear problems, 186 projection theorem, see reciprocal theorem of Cauchy proper transformation, 214 pull-back, 36, 75, 79 strain measures, 43 tensor components, 40 vector components, 36 push-forward, 42 strain measures, 43 quotient rule, 232 Rayleigh-Ritz method, 205 reciprocal theorem of Cauchy, 72 reference frame, 45 Reynolds’ transport theorem, 85 discontinuity surface, 90 generalized, 88 Riemann-Christo el tensor, 62, 240 right Cauchy-Green deformation tensor, see Green deformation tensor right stretch tensor, 22, 28, 48 physical interpretation, 26 rigid boundary conditions , see essential bounday conditions rigid rotation, 15 rigid translation, 15 rotation tensor, 23, 26, 48 physical interpretation, 26 rotor of a tensor, 240 Serrin representation, 32 shear modulus, 126 softening material, 137, 147 space-attached loads, 187 spatial derivative, 12 spin tensor, see vorticity tensor stable materials, 144 strain measures, 33
Index strain rate e ect, 176 strain rate tensor, 51 strain rates, 50 stress tensor, 79 stresses, 67 stresses power, 73 symmetry of stress measures, 107 tangential constitutive tensor, 150 tensor analysis, 213 tensors covariant, 59 Eulerian, 47, 58 isotropic, 125, 156 Lagrangian, 47, 50 n-order, 227 orthogonal, 23 physical components, 245 second-order, 223 eigenvalues and eigenvectors, 225 symmetric, 22 two-point, 14, 23, 47, 50, 74 thermal energy, 109 thermo-elastoplastic constitutive model, 170 thermoelastic constitutive model, 167 time, 7 time rates, 50 total Lagrangian formulation, 190 total-Lagrangian Hencky material model, 166 traction, 70 transformation isometric, 45
259
Truesdell stress rate, 82 updated Lagrangian formulation, 190, 192 variational calculus, 183 variational consistency, 210 variational methods, 183 variations, 184 vector analysis, 213 vector components, 216 vectors, 215 velocity, 10 material, 10 velocity gradient tensor, 50 Veubeke-Hu-Washizu variational principles, 209 constitutives constraints, 211 kinematic constraints, 209 virtual displacements, 184 virtual strains, 185 virtual work, 185 viscoelasticity, 115 viscoplasticity, 115, 176 volumetric component Green-Lagrange strain tensor, 126 volumetric modulus, 126 von Mises yield function, 140, 141 vorticity tensor, 51 work hardening, 147 yield criterion, 135, 144, 161, 170 yield surface, 140, 144, 148, 171, 177 Young’s modulus, 126
