Abstract
The objective of continuum mechanics is to develop mathematical models to analyze the behavior of idealized three-dimensional bodies.
Access provided by Autonomous University of Puebla. Download chapter PDF
Keywords
These keywords were added by machine and not by the authors. This process is experimental and the keywords may be updated as the learning algorithm improves.
The objective of continuum mechanics is to develop mathematical models to analyze the behavior of idealized three-dimensional bodies. The idealization is related to the hypothesis of a continuum, that is the matter is continuously distributed and fills the entire region of a body, e.g. Haupt (2002). The continuum mechanics is based on balance equations and assumptions regarding the kinematics of deformation and motion. Inelastic behavior is described by means of constitutive equations which relate multi-axial deformation and stress states. Topological details of microstructure are not considered. Processes associated with microstructural changes like hardening, recovery, ageing and damage can be taken into account by means of hidden or internal state variables and corresponding evolution equations. Various models developed within the continuum mechanics of solids can be applied to the structural analysis in the inelastic range.
The classical continuum mechanics of solids takes into account only translational degrees of freedom for motion of material points. The local mechanical interactions between material points are characterized by forces. Moment interactions are not considered. Furthermore, it is assumed that the stress state at a point in the solid depends only on the deformations and state variables of a vanishingly small volume element surrounding the point. To account for the heterogeneous deformation various extensions to the classical continuum mechanics were proposed. Micropolar theories assume that a material point behaves like a rigid body, i.e. it has translation and rotation degrees of freedom. The mechanical interactions are due to forces and moments. Constitutive equations are formulated for force and moment stress tensors. Micropolar theories of plasticity are presented in Forest et al. (1997), Altenbach and Eremeyev (2012), Eremeyev et al. (2012), Altenbach and Eremeyev (2014), among others. Inelastic deformation process is highly heterogeneous at the microscale and several effects cannot be described by the classical continuum mechanics accurately. For example, the dependence of the yield strength on the mean grain size and on the mean size of precipitates, see Sect. 1.3, are not considered within the classical theories since they do not possess intrinsic length scales. To analyze such effects, phase mixture, non-local and gradient-enhanced continuum theories are developed. Examples for phase mixture models of inelastic deformation are presented in Naumenko and Gariboldi (2014), Naumenko et al. (2011). Strain gradient and micromorphic theories are discussed in Fleck and Hutchinson (1997), Gao et al. (1999), Forest (2009). Here a gradient or the rotation (curl) of the inelastic strain are considered as additional degrees of freedom. Non-local and phase field theories of damage and fracture were recently advanced to capture initiation and propagation of cracks in solids (Miehe et al. 2010; Schmitt et al. 2013).
This chapter provides basic equations of the classical three-dimensional continuum mechanics. To keep the presentation brief and transparent many details of mathematical derivations are omitted. Several rules of the direct tensor calculus, tensor analysis and special topics related to the theory of tensor functions and invariants are presented in Appendices A–B.5.
With regard to non-linear continuum mechanics there is a number of textbooks, for example Altenbach (2015), Bertram (2012), Eglit and Hodges (1996), Haupt (2002), Lai et al. (1993), Maugin (2013), Smith (1993), Truesdell and Noll (1992).
4.1 Motion, Derivatives and Deformation
4.1.1 Motion and Derivatives
Let \(\varvec{\mathcal {R}}\) be the position vector for a point P in a reference state of a solid, Fig. 4.1 and \(\pmb r\) be the position vector of this point (designated by \(P'\)) in the actual configuration. The displacement vector \(\pmb u\) connects the points P and \(P'\), Fig. 4.1. The position vector \(\varvec{\mathcal {R}}\) can be parameterized with the Cartesian coordinate system including the orthonormal basis \(\pmb i\), \(\pmb j\), \(\pmb k\) and the coordinates X, Y, Z, i.e.
In many cases it is more convenient to use curvilinear coordinates, for example cylindrical, spherical, skew etc. Specifying the curvilinear coordinates by \(X^1=q^1,X^2=q^2,X^3=q^3\), see Appendix B.1 the position vector is parameterized as follows
The directed line element in a differential neighborhood of P is
where \(\varvec{\mathcal {R}}_i\) is the local basis and \(\varvec{\mathcal {R}}^i\) is the dual basis, Appendix B.1. The motion of the continuum is defined by the following mapping
The basic problem of continuum mechanics is to compute the function \({\pmb \varPhi }\) for all vectors \(\varvec{\mathcal {R}}\) within the body in the reference configuration, for the given time interval \(t_0\le t \le t_n\) as well as for given external loads and temperature. It is obvious that \(\varvec{\mathcal {R}}={\pmb \varPhi }(\varvec{\mathcal {R}},t)\). The displacement vector \(\pmb u\) is defined as follows (Fig. 4.1)
The vector \(\pmb r\) can be specified with the basis \(\pmb i,\pmb j, \pmb k\) as follows
with the actual Cartesian coordinates x, y, z. The directed line element in a differential neighborhood of \(P'\) in the actual configuration is
where \(\pmb r_i\) is the local basis and \(\pmb r^i\) is the dual basis in the actual configuration.
To analyze the motion it is useful to introduce the rates of change of functions with respect to the coordinates \(X^i\) and time t. Consider a tensor-valued function \(\pmb f(X^i,t)\). The total differential of \(\pmb f\) for the fixed time variable is
From Eq. (4.1.2)\(_2\) we obtain
The operator \(\mathop {\pmb \nabla }\limits ^{\scriptscriptstyle 0}\) is the Hamilton (nabla) operator with dual basis vectors of the reference configuration
With \(\pmb f=\varvec{\mathcal {R}}\) Eq. (4.1.6) yields
Alternatively, one may use the spatial description by considering \(\pmb f\) to be the function of \(\pmb r\) and t. For the fixed time variable we may compute the total differential of \(\pmb f\) as follows
where
is the Hamilton (nabla) operator with the dual basis of the actual configuration.
The velocity field \(\pmb v\) is defined as follows
The description where \(\pmb f\) is a function of \(\pmb R\) and t is sometimes called Lagrangian or material. On the other hand if \(\pmb f\) is a function of \(\pmb r\) and t, the description is called Eulerian or spatial. As the mapping \(\pmb \varPhi \) is assumed invertible
both the descriptions are equivalent in the sense that if \(\pmb f\) is known as a function of \(\varvec{\mathcal {R}}\) and t, one may use the transformation (4.1.12) to get
Assuming that both \(\pmb v\) and \(\pmb f\) are functions of \(\pmb r\) and t the material time derivative is defined as follows
4.1.2 Deformation Gradient and Strain Tensors
Setting \(\pmb f=\pmb r\) into Eq. (4.1.6) we obtain
The second rank tensor
is called deformation gradient . With \(\pmb u=\pmb r-\varvec{\mathcal {R}}\) and (4.1.8) the deformation gradient can be expressed trough the displacement gradient as follows
Once the deformation gradient is given, one may find the line element \(\mathrm {d}\pmb r\) in the differential neighborhood of the point \(P'\) of the actual configuration for the given line element \(\mathrm {d}\varvec{\mathcal {R}}\) of the reference configuration. Consider three line elements \(\mathrm {d}\varvec{\mathcal {R}}_a\), \(\mathrm {d}\varvec{\mathcal {R}}_b\) and \(\mathrm {d}\varvec{\mathcal {R}}_c\) in the neighborhood of P such that
where \(\mathrm {d} V_0\) is the elementary volume of the parallelepiped spanned on \(\mathrm {d}\varvec{\mathcal {R}}_a\), \(\mathrm {d}\varvec{\mathcal {R}}_b\) and \(\mathrm {d}\varvec{\mathcal {R}}_c\). With Eqs. (4.1.15) and (A.4.7) we can compute the elementary volume of the actual configuration
Hence
The condition \(\det \pmb F>0\) guarantees that the inverse \(\pmb F^{-1}\) exists. It can be computed as follows
Indeed
Consider two line elements \(\mathrm {d}\varvec{\mathcal {R}}_a\), \(\mathrm {d}\varvec{\mathcal {R}}_b\), \(\mathrm {d}\varvec{\mathcal {R}}_a\times \mathrm {d}\varvec{\mathcal {R}}_b\ne \pmb 0\) in the neighborhood of P. Let
be the infinitesimal oriented area element including the area of the parallelogram \(\mathrm {d}A_0\) having \(\mathrm {d}\varvec{\mathcal {R}}_a\) and \(\mathrm {d}\varvec{\mathcal {R}}_b\) as sides and the unit normal \(\pmb N\). With the identity (A.4.8)\(_1\) one may compute the corresponding area element in the deformed configuration
or
With the deformation gradient the following relations between nabla operators (4.1.7) and (4.1.10) can be derived
As a result we obtain
Once \(\pmb F\) is given, one may compute the local strains. To this end consider a line element \(\mathrm {d}\varvec{\mathcal {R}}_a=\pmb M \mathrm {d}l_{a_0}\) in the neighborhood of the point P, where the unit vector \(\pmb M\) is the direction of the element (direction of the strain measurement) and \(\mathrm {d}l_{a_0}\) is the corresponding length. In the actual configuration \(\mathrm {d} \pmb r_a={\pmb m} \mathrm {d}l_a\). In the course of deformation both the orientation and the length of the element are changing. The local stretch and the local normal strain can be computed as follows
With the given deformation gradient and
one may compute
Hence
where \(\pmb C\) is the right Cauchy-Green tensor . For three orthogonal directions specified by the unit vectors \(\pmb e_X\), \(\pmb e_Y\) and \(\pmb e_Z\) Eq. (4.1.23) provides the corresponding stretches
These equations provide three components of the tensor \(\pmb C\) with respect to the orthonormal basis. To define the remaining components consider two orthogonal line elements given by the vectors \(\mathrm {d} \varvec{\mathcal {R}}_a=\pmb M \mathrm {d}l_{a_0}\) and \(\mathrm {d} \varvec{\mathcal {R}}_b=\pmb N \mathrm {d}l_{b_0}\) in the neighborhood of the point P, where \(\pmb N\) and \(\pmb M\), \(\pmb N\pmb {\cdot }\pmb M=0\) are unit vectors. \(\mathrm {d}l_{a_0}\) and \(\mathrm {d}l_{b_0}\) are reference lengths of the elements. The corresponding line elements in the actual configuration are \(\mathrm {d}\pmb r_a={\pmb m} \mathrm {d}l_{a}\) and \(\mathrm {d}\pmb r_b={\pmb n} \mathrm {d}l_{b}\). Let \(\alpha _{MN}\) be the angle between the vectors \(\mathrm {d}\pmb r_a\) and \(\mathrm {d}\pmb r_b\). The local shear strain is defined as \(\gamma _{MN}=\frac{\pi }{2}-\alpha _{MN}\). The scalar product of the vectors \(\mathrm {d}\pmb r_a\) and \(\mathrm {d}\pmb r_b\) yields
For the given deformation gradient \(\pmb F\)
The scalar product yields
With Eq. (4.1.24) we obtain
Equation (4.1.26) provides the MN-component of the tensor \(\pmb C\). Since \(\pmb M\) and \(\pmb N\) are two arbitrary orthogonal unit vectors, one, may compute six components of the tensor \(\pmb C\) by taking the orthogonal unit vectors \(\pmb e_X\), \(\pmb e_Y\) and \(\pmb e_Z\) as directions of the shear strain measurement. Since the tensor \(\pmb C\) is symmetric only three of them are independent, i.e.
The Cauchy-Green tensor is one example of many strain tensors that can be introduced in the non-linear continuum mechanics. To present several examples let us apply the polar decomposition theorem (see Appendix A.4.18) to the deformation gradient
where \(\pmb R\) is the rotation tensor . \(\pmb U\) and \(\pmb V\) are right and left stretch tensors respectively. These positive definite symmetric tensors have the following spectral representations
where \(\lambda _i>0\) are principal stretches . The orthonormal unit vectors \({\mathop {\pmb N}\limits ^{\scriptscriptstyle \pmb U}}_i\) and \({\mathop {\pmb n}\limits ^{\scriptscriptstyle \pmb V}}_i\) are principal directions of the tensors \(\pmb U\) and \(\pmb V\), respectively. From (4.1.27) the following relations can be obtained
Examples of strain tensors related to \(\pmb U\) (sometimes called material strain tensors) are the Cauchy-Green strain tensor
the material Biot strain tensor
and the material Hencky strain tensor
Examples of strain tensors related to \(\pmb V\) (spatial strain tensors) are the Almansi strain tensor
where \(\pmb B=\pmb V^2=\pmb F\pmb {\cdot }\pmb F^T\) is the left Cauchy-Green tensor . Further examples are the spacial Biot strain tensor
and the spacial Hencky strain tensor
For many structural analysis applications the local strains can be assumed small. With \(\varepsilon _{MM}\ll 1\) and \(\gamma _{MN}\ll 1\) the left hand side of Eqs. (4.1.23) and (4.1.26) can be linearized as follows
With Eqs. (4.1.23) and (4.1.36) the normal strain in the direction \(\pmb M\) is
The shear strain can be computed as follows
With the Green-Lagrange strain tensor
the strains can be given as follows
For the given tensor \(\pmb G\) one may compute the strains with respect to any direction. For three orthogonal directions specified by the unit vectors \(\pmb e_X\), \(\pmb e_Y\) and \(\pmb e_Z\) the six components can be computed as follows
Although the normal and shear strains are assumed small, the difference between the unit vectors like \(\pmb M\) and \(\pmb m\) defined in the initial and actual configurations may be essential. To formulate geometrically-linear theory we have additionally to assume infinitesimal rotations.Footnote 1 The linearized rotation tensor \(\pmb R\) can be given as follows
where \(\pmb \varphi \) is the vector of infinitesimal rotations . Then with Eqs. (4.1.27) and (4.1.16) the following linearized relations can be established
The tensor \(\pmb \varepsilon \) is called tensor of infinitesimal strains .
4.1.3 Velocity Gradient, Deformation Rate, and Spin Tensors
The time derivative of the deformation gradient . can be computed with (4.1.15) as follows
With (4.1.11)
Hence
With the relation between nabla operators (4.1.20)\(_2\) Eq. (4.1.40) takes the form
The spatial velocity gradient \(\pmb L= (\pmb \nabla \pmb v)^\mathrm {T}\) can be computed as follows
The tensor \(\pmb L\) can be additively decomposed into the symmetric and skew symmetric parts (see Appendix A.4.10)
where the symmetric part
is called the deformation rate tensorFootnote 2 while
is called vorticity vector .
The time derivative of \(J=\det \pmb F\) can be computed as follows
With (B.4.13) we obtain
Consequently
Taking the trace of Eq. (4.1.42)
With Eq. (4.1.44) we obtain
Applying the polar decomposition (4.1.27) and the relations
the velocity gradient can be computed as follows
For the rotation tensor \(\pmb R\) let us introduce the angular velocity vector \(\pmb \varOmega _{\pmb R}\) and the spin tensor \(\pmb \varOmega _{\pmb R}\times \pmb I\) as follows. According to the definition of the orthogonal tensor, see Appendix A.4.17, we obtain
The skew-symmetric tensor \(\dot{\pmb R}\pmb {\cdot }\pmb R^\mathrm {T}\) is called the left spin tensor or simply spin tensor. With the associated vector \(\pmb \varOmega _{\pmb R}\) we obtain
where \((\ldots )_\times \) denotes the vector invariant or Gibbs cross of the second rank tensor, see Appendix A.4.15. The vector \(\pmb \varOmega _{\pmb R}\) is called the left angular velocity vector of rotation or simply angular velocity of rotation. This vector is widely used in the mechanics of rigid bodies, e.g. Altenbach et al. (2007, 2009), Zhilin (1996). Equation (4.1.46) can be given as follows
Taking the vector invariant of Eq. (4.1.48) the vorticity vector can be computed as follows
The symmetric part of Eq. (4.1.48) is
Equation (4.1.50) can be put in the following form
or
Let us take the time derivatives of stretch tensors applying spectral representations (4.1.28)
Consider a triple of fixed orthogonal unit vectors \(\pmb e_i\) and the rotation tensor \(\pmb P_{\pmb U}\) such that
Hence
or
For the rotation tensors \(\pmb P_{\pmb U}\) and \(\pmb P_{\pmb V}\) the spin tensors and the angular velocity vectors can be introduced as follows
The time derivative of Eq. (4.1.53)\(_2\) yields
Hence the following relationship between the angular velocity vectors can be established
With Eqs. (4.1.54) the rates of change of principal directions can be computed as follows
Consequently the rates of change of stretch tensors (4.1.52) take the following form
With equation (4.1.56) and
one may compute
Applying Eqs. (4.1.53), (4.1.55) it can be simplified as follows
Taking the vector invariant of Eq. (4.1.57) and applying the identities (A.4.15) and (A.4.16) we obtain
where
According to (A.4.16) and the Cayley-Hamilton theorem the tensor \(\pmb A_{\pmb V}\) has the following representations
where \(J_{1_{\pmb V}}, J_{2_{\pmb V}}\) and \(J=J_{3_{\pmb V}}\) are principal invariants of the tensor \(\pmb V\) as defined by Eqs. (A.4.11). The spectral form of the tensor \(\pmb A_{\pmb V}\) is
With Eqs. (4.1.49) and (4.1.58) the following relationship between the angular velocities can be obtained
The relationship (4.1.60) can also be derived with the following decomposition
Therefore the velocity gradient is
With Eqs. (4.1.28), (4.1.47) and (4.1.56), Eq. (4.1.61) takes the form
where
Taking the vector invariant of Eq. (4.1.62) provides the relationship (4.1.60).
With the identity (A.4.8)\(_2\) the tensor \(\pmb L_{\pmb \varOmega }\) can be represented as follows
The right dot product of Eq. (4.1.62) with \(\pmb V^2\) yields
With the decomposition of the velocity gradient (4.1.43), Eq. (4.1.64) takes the following form
Taking the vector invariant of Eq. (4.1.65) yields
From Eqs. (4.1.60) and (4.1.66) we obtain
With Eq. (4.1.59) one may verify the tensor \(\pmb I-1/2\pmb A_{\pmb V}\) is non-singular. Hence
Applying Eq. (4.1.59) the following spectral representation of the tensor \(\pmb K_{\pmb V}\) can be established
Let us relate the tensor \(\pmb D\) to the time derivative of the Hencky strain tensor \(\pmb h\). To this end consider the symmetric part of Eq. (4.1.62)
The time derivative of the Hencky strain tensor (4.1.35) can be computed as follows
Inserting into Eq. (4.1.69) yields
The tensor
has the following representation
Assuming that the tensor \(\pmb V\) has distinct principal values \(\lambda _i\) let us consider the following identity
where the components of vector \(\pmb c\) are related to the components of vector \(\pmb b\) as follows
Hence
Applying the identity (A.4.14) we obtain
Consequently
With Eqs. (4.1.63), (4.1.71), (4.1.73) and (4.1.74) the tensor \(\pmb D\) is related to the rate of the Hencky strain tensor \(\pmb h\) as follows
where
The tensor \(\pmb A_{\pmb h}\) has the following spectral representation
In Xiao et al. (1997) the tensor \(\pmb \varOmega _{\pmb h}\times \pmb I\) is called logarithmic spin. With Eqs. (4.1.55), (4.1.67) and (4.1.75) the vector \(\pmb \varOmega _{\pmb h}\) can be computed as follows
where
Equation (4.1.76) is firstly derived by Xiao et al. (1997) in a different notation. The tensor \(\pmb K_{\pmb h}\) has the following spectral representation
4.2 Conservation of Mass
The mass of an infinitesimal part of the body is
where \(\rho \) and \(\rho _0\) is the density in the actual and the reference configurations, respectively. With Eq. (4.1.17) the conservation of mass (4.2.77) takes the form
4.3 Balance of Momentum
The momentum of an infinitesimal part of the solid is defined as follows
The momentum for a part of the solid with the volume \(V_\mathrm {p}\) in the in the actual configuration is
The balance of momentum or the first law of dynamics states that the rate of change of momentum of a body is equal to the total force acting on the body.
4.3.1 Stress Vector
Figure 4.2 illustrates a body under the given external loads. To visualize the internal forces let us cut the body in the actual configuration by a plane. The orientation of the plane is given by the unit normal vector \(\pmb n\). In the differential neighborhood of a point P consider an infinitesimal area element \(\mathrm {d}A\). To characterize the mechanical action of the part II on the part I of the body let us introduce the force vector \(\mathrm {d}\pmb T_{\mathrm {II-I}}=\mathrm {d}\pmb T_{(\pmb n)}\) as shown in Fig. 4.2. On the other hand the force vector \(\mathrm {d}\pmb T_{\mathrm {I-II}}=\mathrm {d}\pmb T_{(-\pmb n)}\) models the mechanical action of the part I on the part II. The intensity of these mechanical actions can be characterized by the stress vectors \(\pmb \sigma _{(\pmb n)}\) and \(\pmb \sigma _{(-\pmb n)}\). Both the magnitude and the direction of the stress vector depend on the position within the body. Within the infinitesimal area element \(\mathrm {d}A\) the stress vector is assumed constant such that
One may prove that
4.3.2 Integral Form
Let us cut a part with the volume \(V_{\mathrm {p}}\) and the surface area \(A_{\mathrm {p}}\) from the body, as shown in Fig. 4.3. The mechanical actions on the part of the body can be classified as follows
-
body forces, for example force of gravity, electric or magnetic forces acting on a part of the mass \(\mathrm {d}m=\rho \mathrm {d}V\). This type of action is described with the force density vector \(\pmb f\) such that the elementary body force is \(\mathrm {d}\varvec{\mathcal {G}}=\pmb f dm=\pmb f\rho dV\)
-
surface forces \(\mathrm {d}\pmb T_{(\pmb n)}=\pmb \sigma _{(\pmb n)}\mathrm {d}A\) acting on the surface elements \(\mathrm {d}A\) of \(A_{\mathrm {p}}\). These forces characterize the mechanical action of the environment (remainder of the body) on the given part \(V_{\mathrm {p}}\).
The resultant force vector is
The balance of momentum for the part of the solid can be formulated as follows
4.3.3 Stress Tensor and Cauchy Formula
The balance of momentum (4.3.81) can be applied for any part of the body. Consider an infinitesimal tetrahedron (\(A_{\mathrm {p}}\rightarrow 0\), \(V_{\mathrm {p}}\rightarrow 0\)) as a part of the body, Fig. 4.4. The orthonormal vectors \(\pmb e_1\), \(\pmb e_2\) and \(\pmb e_3\) are introduced to fix the orientation of the tetrahedron. The mechanical action of the environment on the tetrahedron cut from the body is characterized by forces and corresponding stress vectors. The cut planes, the corresponding areas as well as stress and force vectors are given in the Table 4.1.
For the infinitesimal tetrahedron the volume integrals in Eq. (4.3.81) have lower order of magnitude compared to the surface integral such that
Hence
Taking into account (4.3.80)
or
In addition the following equation is valid for any part of the volumeFootnote 3
Applying (4.3.85) to the tetrahedron yields
Therefore
Inserting \(\mathrm {d}A_i\) (\(i=1,2,3\)) into Eq. (4.3.84) we obtain
This can be simplified as follows
With the tensor
Eq. (4.3.88) takes the following form
Equation (4.3.90) is the Cauchy formulaFootnote 4 that allows one to compute the stress vector for any plane with the unit normal \(\pmb n\) if the Cauchy stress tensor \(\pmb \sigma \) is given .
4.3.4 Local Forms
With the Cauchy formula (4.3.90) and the integral theorem (B.3.5)\(_2\) the surface integral in (4.3.81) is transformed as follows
Now the balance of momentum takes the form
Since Eq. (4.3.92) is valid for any part of the solid, the following local form of the balance of momentum can be established
With the identity (4.1.18) the surface integral (4.3.91) can be transformed as follows
where
is the Piola-Kirchhoff stress tensor . With Eqs. (4.3.94) and (4.2.78) the balance of momentum can be formulated as follows
The corresponding local form is
4.4 Balance of Angular Momentum
With respect to the point O the angular momentum and the resultant moment vectors for a part of the body are defined as followsFootnote 5
The balance of angular momentum or the second law of dynamics states that the rate of change of angular momentum of a body is equal to the resultant moment acting on the body. The surface integral in Eq. (4.4.98) can be transformed applying (B.3.5)\(_2\) as follows
Applying the identity (B.2.3) we obtain
The balance of angular momentum can be formulated as follows
or
Taking into account the balance of momentum (4.3.93) this results in
4.5 Balance of Energy
The total energy \(E_\mathrm {p}\) of the part of the body, is defined as a sum of the kinetic energy \(\mathrm {K}_\mathrm {p}\) and the internal energy \(\mathrm {U}_\mathrm {p}\) as follows
where \(\mathcal {K}\) and \(\mathcal {U}\) are densities of the kinetic and the internal energy, respectively. The energy balance equation or the first law of thermodynamics states that the rate of change of the energy of a body is equal to the mechanical power plus the rate of change of non-mechanical energy, for example heat, supplied into the body. The energy balance equation is
where \(\mathrm {L}_\mathrm {p}\) is the mechanical power and \(\mathrm {Q}_\mathrm {p}\) is the rate of change of non-mechanical energy supply . The mechanical power of forces introduced in Sect. 4.3.2 is defined as follows
With Eqs. (4.3.90) and (B.3.5)\(_2\) the surface integral in (4.5.103) is transformed to
With the identity (B.2.2) we obtain
The mechanical power can be now given as follows
The energy balance equation (4.5.102) takes the form
With the balance of momentum (4.3.93), Eq. (4.5.106) simplifies to
The rate of change of the energy supply includes the contributions through the outer surface and within the volume of the part p
Equation (4.5.107) takes the following form
Equation (4.5.109) is valid for any part of the body. Considering an infinitesimal tetrahedron the energy balance reduces to
Applying the procedures discussed in Sect. 4.3.3 one may derive the following equation
where \(\pmb q\) is the heat flow vector. With (B.3.5)\(_1\) and (4.5.110) the surface integral can be transformed into the volume one as follows
Equation (4.5.108) takes the form
Equation (4.5.112) is valid for any part of the deformed body. Hence
With the identity (4.1.18) the surface integral (4.5.111) can be transformed as follows
where by analogy to the Piola-Kirchhoff stress tensor the following heat flow vector can be introduced
Now it is not difficult to derive the local form of the energy balance per unit volume of the body in the reference configuration
4.6 Entropy and Dissipation Inequalities
The second law of thermodynamics states that the entropy production of a body is non-negative. This statement is given as the Clausius-Planck inequality
where S is the entropy and T is the absolute temperature. The entropy of the part of the body is defined as follows
where \(\mathcal {S}\) is the entropy density. For the part of the body we define
Applying Eqs. (4.5.110) and (B.3.5)\(_1\) we obtain
With Eqs. (4.6.118) and (4.6.120) the entropy inequality (4.6.117) can be formulated as follows
Since (4.6.121) is valid for any part of the body the local form of the entropy inequality is
With the identity (B.2.1)
Multiplying both sides of (4.6.122) by T yields the Clausius-Duhem inequality
The energy balance equation (4.5.113) can be formulated as follows
Inserting into the entropy inequality (4.6.123) yields the dissipation inequality
Introducing the Helmholtz free energy density \(\varPhi =\mathcal {U}-ST\) the dissipation inequality (4.6.125) can be put into the following form
With Eqs. (4.2.78), (4.3.95) and (4.5.115) as well as the relationships between the gradients (4.1.20) the dissipation inequality (4.6.126) can be given with respect to the reference configuration as follows
Notes
- 1.
In many cases strains can be infinitesimal, but rotations finite. One example is a thin plate strip which can be bent into a ring such that the strains remain infinitesimal but cross section rotations are large.
- 2.
The tensor \(\pmb D\) is in general not a time derivative of a strain tensor.
- 3.
This can be verified applying the integral theorem (B.3.4)\(_1\) with \(\varphi =1\).
- 4.
In some books of continuum mechanics and applied mathematics the stress tensor is defined as \({\large \pmb \sigma } =\pmb \sigma _{(\pmb e_1)}\otimes \pmb e_1+\pmb \sigma _{(\pmb e_2)}\otimes \pmb e_2+\pmb \sigma _{(\pmb e_3)}\otimes \pmb e_3\) such that the Cauchy formula is \(\pmb \sigma _{(\pmb n)}= {\large \pmb \sigma }\pmb {\cdot }\pmb n\). Formally this definition differs from (4.3.89) by transpose. It might be more convenient, as it is closer to the matrix algebra. For engineers dealing with internal forces it is more natural to use (4.3.89). Indeed, to analyze a stress state we need to cut the body first and to specify the normal to the cut plane. Only after that we can introduce the internal force. The sequence of these operations is clearly seen in (4.3.89).
- 5.
With regard to structural analysis applications discussed in this book it is enough to identify the angular momentum as the moment of momentum and the resultant moment as the moment of forces. In contrast, within the micropolar theories material points are equipped by tensor of inertia. The resultant moment includes surface and body moments which are not related to moment of forces, e.g. Altenbach et al. (2003), Eringen (1999), Nowacki (1986).
References
Altenbach H (2015) Kontinuumsmechanik: Einführung in die materialunabhängigen und materialabhängigen Gleichungen. Springer
Altenbach H, Eremeyev V (2012) Generalized Continua - from the Theory to Engineering Applications. Springer, CISM International Centre for Mechanical Sciences
Altenbach H, Eremeyev V (2014) Strain rate tensors and constitutive equations of inelastic micropolar materials. Int J Plast 63:3–17
Altenbach H, Naumenko K, Zhilin PA (2003) A micro-polar theory for binary media with application to phase-transitional flow of fiber suspensions. Continuum Mech Thermodyn 15:539–570
Altenbach H, Naumenko K, Pylypenko S, Renner B (2007) Influence of rotary inertia on the fiber dynamics in homogeneous creeping flows. ZAMM-J Appl Math Mech/Zeitschrift für Angewandte Mathematik und Mechanik 87(2):81–93
Altenbach H, Brigadnov I, Naumenko K (2009) Rotation of a slender particle in a shear flow: influence of the rotary inertia and stability analysis. ZAMM-J Appl Math Mech/Zeitschrift für Angewandte Mathematik und Mechanik 89(10):823–832
Bertram A (2012) Elasticity and plasticity of large deformations, 3rd edn. Springer, Berlin
Eglit M, Hodges D (1996) Continuum mechanics via problems and exercises: theory and problems. World Scientific
Eremeyev VA, Lebedev LP, Altenbach H (2012) Foundations of micropolar mechanics. Springer Science & Business Media
Eringen AC (1999) Microcontinuum field theories, vol. I. In: Foundations and solids. Springer, New York
Fleck NA, Hutchinson JW (1997) Strain gradient plasticity. In: Hutchinson JW, Wu TY (eds) Advances in applied mechanics, vol 33. Academic Press, New York, pp 295–361
Forest S (2009) Micromorphic approach for gradient elasticity, viscoplasticity, and damage. J Eng Mech 135(3):117–131
Forest S, Cailletaud G, Sievert R (1997) A Cosserat theory for elastoviscoplastic single crystals at finite deformation. Arch Mech 49:705–736
Gao H, Huang Y, Nix WD, Hutchinson JW (1999) Mechanism-based strain gradient plasticity - I. Theory. J Mech Phys Solids 47(6):1239–1263
Haupt P (2002) Continuum mechanics and theory of materials. Springer, Berlin
Lai WM, Rubin D, Krempl E (1993) Introduction to continuum mechanics. Pergamon Press, Oxford
Maugin G (2013) Continuum mechanics through the twentieth century: a concise historical perspective. In: Solid mechanics and its applications. Springer
Miehe C, Hofacker M, Welschinger F (2010) A phase field model for rate-independent crack propagation: robust algorithmic implementation based on operator splits. Comput Meth Appl Mech Eng 199(45–48):2765–2778
Naumenko K, Gariboldi E (2014) A phase mixture model for anisotropic creep of forged Al-Cu-Mg-Si alloy. Mater Sci Eng: A 618:368–376
Naumenko K, Altenbach H, Kutschke A (2011) A combined model for hardening, softening and damage processes in advanced heat resistant steels at elevated temperature. Int J Damage Mech 20:578–597
Nowacki W (1986) Theory of asymmetric elasticity. Pergamon Press, Oxford
Schmitt R, Müller R, Kuhn C, Urbassek H (2013) A phase field approach for multivariant martensitic transformations of stable and metastable phases. Arch Appl Mech 83:849–859
Smith DR (1993) An introduction to continuum mechanics. Kluwer, Dordrecht
Truesdell C, Noll W (1992) The non-linear field theories of mechanics, 2nd edn. Springer, Berlin
Xiao H, Bruhns OT, Meyers A (1997) Logarithmic strain, logarithmic spin and logarithmic rate. Acta Mechanica 124(1–4):89–105
Zhilin PA (1996) A new approach to the analysis of free rotations of rigid bodies. ZAMM-J Appl Math Mech/Zeitschrift für Angewandte Mathematik und Mechanik 76(4):187–204
Author information
Authors and Affiliations
Corresponding author
Rights and permissions
Copyright information
© 2016 Springer International Publishing Switzerland
About this chapter
Cite this chapter
Naumenko, K., Altenbach, H. (2016). Three-Dimensional Continuum Mechanics. In: Modeling High Temperature Materials Behavior for Structural Analysis. Advanced Structured Materials, vol 28. Springer, Cham. https://doi.org/10.1007/978-3-319-31629-1_4
Download citation
DOI: https://doi.org/10.1007/978-3-319-31629-1_4
Published:
Publisher Name: Springer, Cham
Print ISBN: 978-3-319-31627-7
Online ISBN: 978-3-319-31629-1
eBook Packages: EngineeringEngineering (R0)