Abstract
This study presents a novel computational framework for designing optimal dissipative (damping) metamaterials under time-dependent loading conditions at finite deformations. In this framework, finite strain computational homogenization is integrated with a density-based multimaterial topology optimization. In addition, a thermodynamically consistent finite strain viscoelasticity model is incorporated together with an analytical path-dependent sensitivity analysis. Optimization formulations with and without stiffness and mass constraints are considered, and various new damping metamaterial designs are obtained that combine soft viscoelastic and stiff hyperelastic material phases. Multiscale stability analysis using the Bloch wave analysis and rank-1 convexity checks is also carried out to investigate stability of the optimized designs. Stability analyses demonstrate that the inclusion of voids or soft material phases can make a metamaterial more prone to lose micro and macro-stability. Furthermore, the concept of tunable metamaterials is explored wherein metamaterial’s response is steered towards a stable deformation path by tailoring the design with a preselected micro buckling mode.
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The presented work is supported in part by the US National Science Foundation through Grant CMMI-1762277. Any opinions, findings, conclusions, and recommendations expressed in this paper are those of the authors and do not necessarily reflect the views of the sponsors.
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Replication of results
Appendices A, B and C provide the supplementary information that is needed to replicate the results presented in this study.
Appendices
Appendix A:: Finite strain viscoelasticity model implementation
In this appendix, numerical implementation of the finite strain viscoelastic model is presented. In the context of strain-driven finite element analysis, given data at an integration point: Fk and \(\boldsymbol {b}_{k}^{e}\) at previous step k, and F at current step k + 1, the goal is to find the unknown variables: P, be and the consistent tangent moduli at the current step k + 1. Note that the subscript k + 1 for the current step, the element number, and integration point number are removed for clarity. In addition to standard tensor notations, the following nonstandard tensor notations are used:
where A and B are any 2nd-order tensors and \(\boldsymbol {\mathcal {A}}\) and \(\mathbb {A}\) are any 3rd- and 4th-order tensors, respectively.
The viscoelastic model consists of equilibrium and non-equilibrium parts. The equilibrium part is handled in the same way as the hyperelastic model. For the non-equilibrium part, the material interpolation cannot be applied outside the material subroutine since the internal variable be is not known and has to be solved from a set of nonlinear constitutive equations where interpolated material parameters are used. In the following derivations, the material parameters κ, μq, and ηd are interpolated based on the material interpolation given in Section 4.3.
1.1 A.1 Integration of rate equations
The internal variable given in (35) is integrated using the exponential map integrator (Weber and Anand 1990). With \({\mathcal{L}}_{v}[\boldsymbol {b}^{e}]=\boldsymbol {F}.\dot {\overline {{\boldsymbol {C}^{v}}^{-1}}}.\boldsymbol {F}^{T}\) where Cv = FvT.Fv, (35) can be written as
Using the backward exponential integrator, (A.2) is integrated as
where the subscript k denotes the term evaluated at the last time step tk, with the time interval Δt = tk+ 1 − tk. Noticing that \(\exp [\boldsymbol {Y}^{-1}.\boldsymbol {Z}.\boldsymbol {Y}]=\boldsymbol {Y}^{-1}.\exp [\boldsymbol {Z}].\boldsymbol {Y}\) for any 2nd-order tensor Y and Z (Y is invertible) and the relation \(\boldsymbol {b}^{e}=\boldsymbol {F}.{\boldsymbol {C}^{v}}^{-1}.\boldsymbol {F}^{T}\), (A.3) can be simplified to
with \({\boldsymbol {b}^{e}}^{tr}={\boldsymbol {F}^{e}}^{tr}.{\boldsymbol {F}^{e}}^{{tr}^{T}}\) where \({\boldsymbol {F}^{e}}^{tr}\triangleq \boldsymbol {F}_{\delta }.\boldsymbol {F}_{k}^{e}\) and \(\boldsymbol {F}_{\delta }=\boldsymbol {F}.\boldsymbol {F}_{k}^{-1}\). Due to the isotropy, the non-equilibrium stress τneq and the tensor be are coaxial, which results in the coaxiality of tensor betr with τneq and be. As a result, it is possible to express the evolution rule in the principal space. Denote the elastic principal stretch at the current step as \({\lambda _{a}^{e}}\), while \({{\lambda _{a}^{e}}}^{tr}\) (a = 1, 2, 3) for the trial step, which are the square-root of the eigenvalues of tensors be and betr, respectively. The non-equilibrium principal stresses are denoted by \(\tau _{a}^{neq}\), which are the eigenvalues of the tensor τneq. Employing logarithmic strain, where \({\varepsilon _{a}^{e}}{\triangleq \ln \lambda _{a}^{e}}\) and \({{\varepsilon _{a}^{e}}}^{tr}\triangleq {{\ln \lambda _{a}^{e}}}^{tr}\), (A.4) can be expressed in the principal space as
where \(p^{neq}=(\tau _{1}^{neq}+\tau _{2}^{neq}+\tau _{3}^{neq})/3\) represents the pressure which equals \(\frac {1}{3}\text {tr}\left (\tau ^{neq}\right )\).
1.2 A.2 Stress tensor and consistent tangent moduli
For the non-equilibrium part, since the elastic Finger tensor be is not known, the non-equilibrium Kirchhoff stress τneq and be have to be calculated by using Eq. (33)3 and (A.5). This set of nonlinear equations are solved using Newton-Raphson (NR) method. Due to the coaxiality of be and τneq, (33)3 can be expressed in the principal space as
with the principal space spanned by \(\boldsymbol {G}_{a}^{e}\) which are the same as \({\boldsymbol {G}_{a}^{e}}^{tr}\) that span the principal space of betr (see (A.4)). Combining (A.5) and (A.6), the unknown variables \(\tau _{a}^{neq}\) and \({\varepsilon _{a}^{e}}\) are solved using the Newton-Raphson method. Taking \(\tau _{a}^{neq}\) as implicit functions of \({\varepsilon _{a}^{e}}\) determined by (A.6), the unknown variables are reduced to \({\varepsilon _{a}^{e}}\) and the set of nonlinear equations to be solved becomes
with the Jacobian matrix calculated, by employing (A.6), as
where κ, μq, and αq (q = 1,..., N) are parameters related to the non-equilibrium strain energy. Tangent modulus for the non-equilibrium part is obtained as
where the derivative ∂τneq/∂betr is computed using chain rule
in which \({\boldsymbol {\varepsilon }^{e}}^{tr}={\sum }_{a=1}^{3} {{\varepsilon _{a}^{e}}}^{tr}\boldsymbol {G}_{a}^{e}\) and the term ∂τneq/∂εetr can be derived from the (A.6) and (A.7) following the procedure given in de Souza Neto et al. (2011). The term ∂εetr/∂betr is computed in the same way, since εetr and betr are coaxial.
Appendix B:: Explicit derivatives required for the adjoint sensitivity analysis
For the objective and constraint functions, beside the energy dissipation (\(f_{0}=-\overline {W}_{d}\)) which depends on the solution and auxiliary variables, all the other constraints, e.g., material volume constraint and initial stiffness constraint, are only functions of the density field and their sensitivities are not path-dependent, and thus easy to compute. This appendix gives the derivatives that are used in the path-dependent sensitivity calculation of f0. For illustration purposes, the material interpolation scheme assuming void phase for Material-0 (Section 4.3.1) is considered in the sensitivity derivation in this appendix. In the following derivations, the tensor form and matrix-vector form are both utilized for notational simplicity and the appropriate form should be clear from the context. Moreover, to simplify the derivation process, the following functions are defined
where the functions ζκ(ρ1) and ζμ(ρ1) are evaluated using the associated material parameters, e.g., g2(ρ1, ρ2) and g3(ρ1, ρ2) are evaluated using Material-1 parameters, g4(ρ1, ρ2) and g5(ρ1, ρ2) are using equilibrium part of the viscoelastic material (Material-2), while g6(ρ1, ρ2) and g7(ρ1, ρ2) are based on non-equilibrium part of the viscoelastic material.
1.1 B.1 Derivatives of f0
After time and spatial domains discretization, the homogenized energy dissipation defined in (39) can be approximated by
where \(\mathbb {D}\) depends on the density variables \({\rho _{1}^{e}}\) and \({\rho _{2}^{e}}\); \(\boldsymbol {\tau }_{e_{s}}^{neq}\) is the Kirchhoff stress of the non-equilibrium viscoelastic phase at s th integration point in e th element; and Δtk = tk − tk− 1 is the time interval between step (k − 1) and step k. This leads to
The derivatives ∂f0/∂ρ1 and ∂f0/∂ρ2 are arranged as
with their components computed based on chain rule as
where \(\mu _{0}^{neq}\) is the initial shear modulus of the non-equilibrium viscoelastic solid phase, ηd is the interpolated value, and \(\hat {\psi }^{neq}\) and \(\tilde {\psi }^{neq}\) are the volumetric and isochoric non-equilibrium viscoelastic strain energy of solid phase.
The derivative \(\partial f_{0}/\partial \boldsymbol {v}^{k}\) is arranged as
where element number and integration point indices on elastic Finger tensor be are avoided with the understanding that the derivative \(\partial \boldsymbol {\tau }_{e_{s}}^{neq}/\partial \boldsymbol {b}^{e}\) is evaluated at the s th integration point inside e th element.
1.2 B.2 Derivatives of Rk
Due to the linear energy interpolation (Section 4.4) and F-bar formulation (Section 4.5), the 1st PK stress P is computed as
where r = r(ρ1, u) is a function of ρ1 and u, and \(\boldsymbol {P}_{0}^{b}\), \(\boldsymbol {P}_{1}^{b}\), \(\boldsymbol {P}_{2}^{b,eq}\), and \(\boldsymbol {P}_{2}^{b,neq}\) are 1st PK stresses contributed from different material phases, where the superscript “b” is used to denote that they are evaluated based on Fb. Based on this, it is straightforward that
where \(\boldsymbol {\nabla }_{\boldsymbol {X}}^{0}\) denotes the gradient operator evaluated at the centroid of the element. Also,
where B and B0 are the shape functions derivative matrices evaluated at the integration point and the centroid, respectively. Besides, due to the dependence of Fb on ρ1 and u, the following derivatives are obtained
1.2.1 B.2.1 Derivatives of \(\partial \boldsymbol {R}^{k}/\partial \boldsymbol {\rho }_{1}\) and \(\partial \boldsymbol {R}^{k}/\partial \boldsymbol {\rho }_{2}\)
The explicit dependence of Rk on ρ1 comes from the linear energy interpolation parameter γ(ρ1) as well as the interpolated constitutive model parameters. Thus, the derivative \(\partial \boldsymbol {R}^{k}/\partial \boldsymbol {\rho }_{1}\) is computed as
in which \(\mathbb {A}_{0}^{b}\), \(\mathbb {A}_{1}^{b}\), and \(\mathbb {A}_{2}^{b,eq}\) are the tangent moduli evaluated from each constitutive model with material interpolation, i.e., \(\mathbb {A}_{0}^{b}\triangleq \partial \boldsymbol {P}_{0}^{b}/\partial \boldsymbol {F}^{b}\), \(\mathbb {A}_{1}^{b}\triangleq \partial \boldsymbol {P}_{1}^{b}/\partial \boldsymbol {F}^{b}\) and \(\mathbb {A}_{2}^{b,eq}\triangleq \partial \boldsymbol {P}_{2}^{b,eq}/\partial \boldsymbol {F}^{b}\); \(\frac {\partial \boldsymbol {P}^{b}}{\partial \rho _{1}}\big |_{\boldsymbol {F}^{b} \text {fixed}}\) is computed by
where
where “s” in the subscript denotes that the term is evaluated with the non-interpolated solid material parameters. Again, the upper hat denotes the volumetric part while upper tilde denotes the isochoric part, e.g., \(\hat {\boldsymbol {P}}_{2,s}^{b,eq}=\partial \hat {\psi }_{2}^{eq}/\partial \boldsymbol {F}^{b}\), where \(\hat {\psi }_{2}^{eq}\) is evaluated with solid phase parameters. It should be noted that in sensitivity analysis the calculation of \(\hat {\boldsymbol {P}}_{2,s}^{b,neq}\) and \(\tilde {\boldsymbol {P}}_{2,s}^{b,neq}\) are based on \(\hat {\psi }_{2}^{neq}(\boldsymbol {b}^{e})\) and \(\tilde {\psi }_{2}^{neq}(\boldsymbol {b}^{e})\) where solid material phase parameters are used, however, the computation of be is based on the interpolated material parameters. Since be is chosen as independent variable, its dependence on ρ1 and ρ2 fields is not explicitly accounted. On the other hand, the dependence of Rk on ρ2 comes from the constitutive model parameters. As a result, the derivative \(\partial \boldsymbol {R}^{k}/\partial \boldsymbol {\rho }_{2}\) is computed as
1.2.2 B.2.2 Derivatives of \(\partial \boldsymbol {R}^{k}/\partial \hat {\boldsymbol {u}}^{k}\) and \(\partial \boldsymbol {R}^{k}/\partial \hat {\boldsymbol {u}}^{k-1}\)
The derivative \(\partial \boldsymbol {R}^{k}/\partial \hat {\boldsymbol {u}}^{k}\) is derived as
where the term ∂Pb/∂Fb is calculated in (B.15). Also, Rk does not depend on \(\hat {\boldsymbol {u}}^{k-1}\) explicitly and
1.2.3 B.2.3 Derivatives of ∂Rk/∂vk and ∂Rk/∂vk− 1
Since in the free energy only \(\psi _{2}^{neq}(\boldsymbol {b}^{e})\) depends on the auxiliary variable (v ≡be), the derivative ∂Rk/∂vk can be derived as
Without dependence of Rk on vk− 1
1.3 B.3 Derivatives of Hk
1.3.1 B.3.1 Derivatives of \(\partial \boldsymbol {H}^{k}/\partial \boldsymbol {\rho }_{1}\) and \(\partial \boldsymbol {H}^{k}/\partial \boldsymbol {\rho }_{2}\)
The derivatives \(\partial \boldsymbol {H}^{k}/\partial \boldsymbol {\rho }_{1}\) and \(\partial \boldsymbol {H}^{k}/\partial \boldsymbol {\rho }_{2}\) are obtained as
where
and
in which \(\tilde {\tau }_{a}^{neq}=\tau _{a}^{neq}-p^{neq}\) is the isochoric part of the principal non-equilibrium Kirchhoff stress and the relationship \({\boldsymbol {b}^{e}}^{tr}=\boldsymbol {F}_{\delta }^{b}.\boldsymbol {b}_{k-1}^{e}.\boldsymbol {F}_{\delta }^{b^{T}}\) with \(\boldsymbol {F}_{\delta }^{b}\triangleq \boldsymbol {F}^{b}.\boldsymbol {F}_{k-1}^{b^{-1}}\) is used in the derivation (where Fb is at step k), and the derivative \(\partial \tilde {\tau }_{a}^{neq}/{\partial \rho _{A}^{e}}\) is calculated by
where the subscript “s” in \(\tilde {\tau }_{a,s}^{neq}\) means that it is computed from the solid phase.
1.3.2 B.3.2 Derivatives of \(\partial \boldsymbol {H}^{k}/\partial \hat {\boldsymbol {u}}^{k}\) and \(\partial \boldsymbol {H}^{k}/\partial \hat {\boldsymbol {u}}^{k-1}\)
The derivative \(\partial \boldsymbol {H}^{k}/\partial \hat {\boldsymbol {u}}^{k}\) is obtained as
Similarly, the derivative \(\partial \boldsymbol {H}^{k}/\partial \hat {\boldsymbol {u}}^{k-1}\) is obtained in the same way but with
1.3.3 B.3.3 Derivatives of ∂Hk/∂vk and ∂Hk/∂vk− 1
The derivative ∂Hk/∂vk is obtained as
where \(\mathbb {I}_{4}^{s}\) is the symmetric identity 4th-order tensor, i.e., \(\mathbb {I}_{4}^{s}\triangleq \frac {1}{2}(\boldsymbol {I}\boxtimes \boldsymbol {I}+\boldsymbol {I}\boxdot \boldsymbol {I})\), \(\boldsymbol {I}\rightarrow \) second-order identity tensor and the derivatives \(\partial (\exp [-2 {\Delta } t_{k}\boldsymbol {A}])/\partial \boldsymbol {\tau }^{neq}\) and ∂τneq/∂be are computed in the principal space. Finally, the derivative ∂Hk/∂vk− 1 is formulated in the same way as ∂Hk/∂vk, but with
Appendix C: Verifications of the path-dependent sensitivity analysis
In this appendix, the path-dependent sensitivity calculation given in Section 5 and Appendix B is verified for two types of material interpolations as given in Section 4.3 for different candidates chosen for material-0. The first verification, referred to as verification-1, considers the material interpolation given in Section 4.3.1 with void phase chosen as material-0. The second verification, referred to as verification-2, considers the material interpolation in Section 4.3.2 with a soft hyperelastic phase chosen as material-0.
1.1 C.1 Sensitivity verification-1: Void for material-0
For verification-1, a parallelogram-shaped RUC with a random design shown in Fig. 15a is used. The density vectors ρ1 and ρ2 are plotted in Fig. 15c. The macroscopic deformation loading considers (68) to (70) with 𝜃 = 0∘, Λ = 1.4, f = 0.009s− 1, and t ∈ [0, 1/f]. The sensitivity comparison between the proposed adjoint method and the central difference method (with perturbation \({\Delta }\rho _{1}={\Delta }\rho _{2}={10}^{-6}\)) is shown in Fig. 16 where good matches can be observed with relative error around 10− 6 to 10− 8. Here, the relative error is computed as the absolute value of the ratio of the difference between the central difference results and the adjoint results to the central difference results.
1.2 C.2 Sensitivity verification-2: Soft hyperelastic phase for material-0
For verification-2, a hexagon-shaped RUC with prescribed design shown in Fig. 15b is used. The design is with the same density vectors ρ1 and ρ2 shown in Fig. 15c. The macroscopic deformation loading considers (68) to (70) with 𝜃 = 45∘, Λ = 1.4, f = 0.009s− 1 and t ∈ [0, 1/f]. The sensitivity comparison between the proposed adjoint method and the central difference method (with perturbation \({\Delta }\rho _{1}={\Delta }\rho _{2}={10}^{-6}\)) is shown in Fig. 17 where again good matches can be observed with relative error around 10− 6 to 10− 8.
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Zhang, G., Khandelwal, K. Topology optimization of dissipative metamaterials at finite strains based on nonlinear homogenization. Struct Multidisc Optim 62, 1419–1455 (2020). https://doi.org/10.1007/s00158-020-02566-8
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DOI: https://doi.org/10.1007/s00158-020-02566-8