Multiobjective structural optimization of honeycomb cells
Xu Zhang^{1} , Zhaoming Su^{2} , Wei Li^{3} , Xuejuan Niu^{4} , Zituo Wang^{5}
^{1, 2, 4, 5}Tianjin Key Laboratory of Advanced Mechatronics Equipment Technology, Tiangong University, Tianjin, 300387, China
^{3}School of Energy and Safety Engineering, Tianjin Chengjian University, Tianjin, 300384, China
^{3}Corresponding author
Journal of Vibroengineering, Vol. 24, Issue 4, 2022, p. 714725.
https://doi.org/10.21595/jve.2022.22210
Received 15 September 2021; received in revised form 20 December 2021; accepted 17 January 2022; published 30 June 2022
This paper develops an optimum cell structure design method considering the inplane tensile/compression and shear properties to improve the stiffness and strength of the honeycomb core. The equivalent elastic modulus in the $X$ or $Y$ direction and shear modulus in the $XY$ plane are derived using Energy Method for hexagonal, quadrilateral and concave hexagonal cells, and are compared with the results in the related literatures. The multiobjective optimization model in which the vertical wall length, wall thickness and inner angle of the cell are taken as design variables is solved by Genetic Algorithm to maximize the equivalent elastic moduli. The static and dynamic characteristics of the honeycomb cores with original and optimized cells are studied using Finite Element Method. The results show that after the cell optimization, the maximum displacement, stress and strain obviously decrease, thus improving the structural performance of the honeycomb core. The research provides significant guidance for the design of the cell structure.
 A cell considering inplane tensile/compression and shear properties is optimized.
 The results confirm structural performance improvements.
 The research provides significant guidance for the design of cell structure.
Keywords: honeycomb cell, structural optimization, elastic modulus.
1. Introduction
The metallic and polymeric honeycomb cores widely used in panel structures, energy absorbers and insulation layers are formed by periodic permutation and combination of prismatic cellular microstructures [13]. Their tensile/compression and shear properties can be improved effectively by the cell structure optimization [4, 5]. Hence, much effort is usually spent on the optimization of geometric parameters of the cell.
Qin et al. [6] optimized the cell wall thickness and its variation gradient index using Nondominated Sorting Genetic Algorithm (NSGA) to maximize the energy absorption ratio and minimize the collision force peak. Zhang et al. [7] optimized the cell size of a honeycomb structure by NSGA to maximize the energy absorption efficiency. Qiu et al. [8] optimized the size and key point coordinates of a hexagonal cell using Genetic Algorithm (GA) to minimize the flexibility of a chiral honeycomb panel. Wang et al. [9] optimized the relative density and size of the cell to improve the heat dissipation capacity of a composite sandwich honeycomb panel. Zhang et al. [10] optimized the cell wall thickness of an aluminum honeycomb using software Hyperstudy and LSDYNA integrated optimization technique. Sorohan et al. [11] adopted the optimization module of ANSYS software to optimize the cell geometric parameters of a hexagonal honeycomb core with outofplane isotropic properties. Cinar et al. [12] optimized the thickness, diameter and inner angle of a threedimensional cell using GA combined with a finite element solver to minimize the natural frequency difference square sum of the honeycomb panel. Gholami et al. [13] and Namvar et al. [14] optimized the cell structure parameters by Particle Swarm Optimization and GA to minimize the deflection of a honeycomb core under uniformly distributed normal load and static load, respectively.
To date, it has not been investigated that on the premise of ensuring the honeycomb core light weighting, the cell structure is optimized to improve the tensile/compression and shear moduli in inplane. The present study firstly derives the formulas of the equivalent elastic moduli of three types of cells by Energy Method, and analyzes the calculation accuracy by comparison with the results of Refs. [15] and [16]. Then, the multiobjective optimization model is established to maximize the equivalent elastic moduli, and the size and shape of the cell are optimized using GA. Finally, the structural performance of original and optimized honeycomb cores are investigated using statics and modal analysis.
2. Equivalent elastic modulus of the cell
The inclined wall length $l$, vertical wall length $\alpha l$, wall thickness $\beta l$ and inner angle $\theta $ of the basic cell, and the honeycomb core thickness $\eta l$ are shown in Fig. 1. The nondimensional treatment for the inclined wall length is produced, that is, $\left[l\right]=1$, and the dimensionless quantities of the vertical wall length, wall thickness and honeycomb core thickness are $\alpha $, $\beta $, $\eta $, respectively.
According to $\theta >0\xb0$, $\theta =0\xb0$ and $\theta <0\xb0$, the cell is divided into three types: hexagon cell, quadrilateral cell and concave hexagon cell, and the quarter structure and size parameters are shown in Fig. 2. The tensile and compressive stress in the $X$ or $Y$ direction and shear stress in the $XY$ plane generate when the force acts in the honeycomb core plane. The equivalent elastic and shear moduli are derived, and the processes are the same for hexagon, quadrilateral and concave hexagon cells. The concave hexagonal cell is chosen as a testbed to illustrate the calculation of material constants.
Fig. 1. Honeycomb core
a) Honeycomb core
b) Basic cell
Fig. 2. Quarter structure and size parameters of hexagonal, quadrilateral and concave hexagonal cells
a)$\theta >0\xb0$
b)$\theta =0\xb0$
c)$\theta <0\xb0$
2.1. Equivalent elastic modulus in the $\mathbf{X}$ direction
The basic cell is subjected to a normal stress along the $X$ direction, ${\sigma}_{X}$, when the tensile deformation of the honeycomb core occurs, as shown in Fig. 3(a). The displacement of a quarter of the cell is calculated due to the symmetry, and is the same as that of the inclined wall under the combined action of stretching and bending. The vertical wall is regarded as a fixedend constraint in view of the interaction between cells, and then the inclined wall is simplified to be a cantilever beam model, as shown in Fig. 3(b). The tensile load ${F}_{X}$ and bending load ${M}_{X}$ are expressed by:
Fig. 3. Concave hexagonal cell subjected to ${\sigma}_{X}$ and its equivalent model.
a) Concave hexagonal cell subjected to ${\sigma}_{X}$
b) Equivalent cantilever beam model
The axial force ${F}_{XN}\left(x\right)$ and bending moment ${M}_{XZ}\left(x\right)$ of the inclined wall OA are as follows:
The total deformation energy under the coupling action of ${F}_{X\mathrm{N}}\left(x\right)$ and ${M}_{XZ}\left(x\right)$, ${U}_{X}$, is as follows:
where ${U}_{{M}_{XZ}}$and ${U}_{{F}_{XN}}$ are the deformation energies produced by ${M}_{XZ}\left(x\right)$ and ${F}_{XN}\left(x\right)$, respectively; ${E}_{s}$ is the elastic modulus of matrix material; ${I}_{Z}$ and $A$ are the moment of inertia and the area of the section.
The displacement of the cell along the $X$ direction, ${\delta}_{X}$, is obtained by Castigliano’s Theorem:
The strain along the $X$ direction, ${\epsilon}_{X}$, is as follows:
The equivalent elastic modulus along the $X$ direction, ${E}_{X}^{*}$, is expressed according to Hooke’s Law:
For hexagonal and quadrilateral cells, the equivalent elastic modulus along the $X$ direction is written as:
2.2. Equivalent elastic modulus in the Y direction
The equivalent elastic modulus in the $Y$ direction is calculated based on the cantilever beam model when the cell is subjected to a normal stress along the $Y$ direction, ${\sigma}_{Y}$, as shown in Fig. 4. The tensile load ${F}_{Y}$ and bending load ${M}_{Z}$ are expressed by:
Fig. 4. Concave hexagonal cell subjected to ${\sigma}_{Y}$ and its equivalent model
a) Concave hexagonal cell subjected to ${\sigma}_{Y}$
b) Equivalent cantilever beam model
The axial force ${F}_{YN}\left(x\right)$ and bending moment ${M}_{YZ}$ of the inclined wall OA are as follows:
The total deformation energy under the coupling action of ${F}_{YN}\left(x\right)$ and ${M}_{YZ}$, ${U}_{Y}$, is as follows:
The displacement of the cell along the $Y$ direction, ${\delta}_{Y}$, is obtained by Castigliano’s Theorem:
The strain along the $Y$ direction, ${\epsilon}_{Y}$, is as follows:
The equivalent elastic modulus along the $Y$ direction, ${E}_{Y}^{*}$, is expressed according to Hooke’s law:
For hexagonal and quadrilateral cells, the equivalent elastic modulus along the $Y$ direction is written as:
2.3. Equivalent shear modulus in the $\mathbf{X}\mathbf{Y}$ plane
The displacement of the cell subjected to the shear stress $\tau $ in Fig. 5(a) is obtained by calculating that of point B. Similarly, the vertical wall is regarded as a fixedend constraint, and the cell is simplified to a symmetric beam with antisymmetric loads, as shown in Fig. 5(b). The load on point B, ${F}_{XY}$, is expressed by:
The displacement caused by the shear deformation, ${\delta}_{XY}$, is obtained by Castigliano’s Theorem:
Fig. 5. Concave hexagonal cell subjected to $\tau $ and its equivalent model
a) Concave hexagonal cell subjected to $\tau $
b) Equivalent symmetric beam model
The inplane shear strain ${\gamma}_{XY}$ is as follows:
The equivalent shear modulus ${G}_{XY}^{*}$ is expressed according to Hooke’s law:
For hexagonal and quadrilateral cells, the equivalent shear modulus is written as:
2.4. Validation of equivalent elastic and shear moduli
Table 2 gives the values of ${E}_{X}^{\mathrm{*}}$, ${E}_{Y}^{\mathrm{*}}$ and ${G}_{XY}^{\mathrm{*}}$ from the presented method, method of Ref. [15] and experiment of Ref. [16] for the cells with the parameters in Table 1. The calculated results from the methods of this paper and Ref. [15] are within the range of experimental values for Sample 1, while ${E}_{Y}^{\mathrm{*}}$ from the method of Ref. [15] is out of the range of experimental values for Sample 2. This is because Ref. 15 does not consider the tensile deformation of the cell wall. The displacement caused by the tensile deformation can be ignored due to the thinner wall of Sample 1, and need be taken into account as the wall thickness of Sample 2 is closer to the inclined wall length. Hence, the presented method has good accuracy.
Table 1. Size and performance parameters of Sample cells in Ref. 16
Size and performance parameters  Sample 1  Sample 2 
$l$ / mm  6  2.5 
$\alpha l$ / mm  6  2.5 
$\beta l$ / mm  0.04  0.03 
$\theta $ / (°)  30  30 
${E}_{s}$ / GPa  72  72 
${\rho}_{s}$ / (kg.m^{3})  2700  2700 
${\upsilon}_{s}$  0.34  0.34 
Table 2. Calculated and experimental values of ${E}_{X}^{*}$, ${E}_{Y}^{*}$ and ${G}_{XY}^{*}$
Analysis method  Sample 1  Sample 2  
${E}_{X}^{*}$ / MPa  ${E}_{Y}^{*}$ / MPa  ${G}_{XY}^{*}$ / MPa  ${E}_{X}^{*}$ / MPa  ${E}_{Y}^{*}$ / MPa  ${G}_{XY}^{*}$ / MPa  
Presented method  0.045  0.049  0.005  0.262  0.283  0.030 
Method of Ref. 15  0.049  0.047  0.012  0.287  0.216  0.072 
Experiment of Ref. 16  0.0450.055  0.0430.053  —  0.2600.300  0.2700.310  — 
3. Optimization method of cell structure
The vertical wall length, wall thickness and inner angle of the basic cell are chosen as the design variables:
where $H$ is the vector of design variables.
The elastic modulus is an important index to measure the strength and stiffness of the honeycomb core. Hence, the design objective is to maximize the equivalent elastic and shear moduli:
where ${\lambda}_{1}$, ${\lambda}_{2}$, ${\lambda}_{3}$ are the weight coefficients, and ${\lambda}_{1}+{\lambda}_{2}+{\lambda}_{3}=1$.
Too thin or too thick cell wall increases the processing difficulty and results into the solid cell, respectively, and the cell will disappear if the inner angle is too great. Besides, the relative density ${\rho}_{s}^{*}$ is used to characterize the mass in design space. Hence, $\alpha $, $\beta $, $\theta $ and ${\rho}_{s}^{*}$ are bounded by:
where ${\rho}_{ori}^{*}$ is the relative density of the original cell.
The flow chart of the cell structure optimization is shown in Fig. 6. The multiobjective GA starts the search from a string set of solutions, generating a large number of noninferior solutions in one optimization thus avoiding the disadvantage that the integrated algorithm is easy to fall into a local optimum. For GA parameters, the crossover probability is 0.7, the mutation probability is 0.02, and the maximum iteration number is 100. To ensure the calculation accuracy, the design variables and optimized results keep 4 decimal places using binary encoding:
where ${H}_{\mathrm{m}\mathrm{a}\mathrm{x}}$ and ${H}_{\mathrm{m}\mathrm{i}\mathrm{n}}$ are the upper and lower limits of design variables, respectively; $n$ is accurate to the $n$^{th} decimal place; $t$ is the length of the encoded gene, and is 33.
Fig. 6. Flow chart of the cell structure optimization
The optimizer performance is illustrated in Fig. 6(a), and the good convergence is achieved after 19 iterations. The structural parameters are shown in Table 3, and Fig. 7 gives the original and optimized cells.
Fig. 7. Optimizer performance and cells
a) Optimizer performance
b) Original and optimized cells
Table 3. Structural parameters of optimized honeycomb cell
Optimized parameters  Initial values  Optimized values 
$\alpha l$ / mm  6.0000  5.5230 
$\beta l$ / mm  0.0400  0.0384 
$\theta $ / °  30.0000  16.6920 
${\rho}_{s}^{*}$  0.0153  0.0133 
4. Structure performance analysis of original and optimized honeycomb cores
The original and optimized cells are respectively tiled to form the honeycomb cores, and then the finite element models are established with APDL language in ANSYS environment and are meshed by shell93 element, as shown in Fig. 8. The statics and modal analysis are performed with an aim to study the effects of the cell optimization on the displacement, stress, strain, nature frequency and mode shape.
Fig. 8. Finite element models of original and optimized honeycomb cores.
a) Before the cell optimization
b) After the cell optimization
Fig. 9. Displacement, stress and strain distributions of original and optimized honeycomb cores
a) Displacement before the optimization
b) Displacement after the optimization
c) Stress before the optimization
d) Stress after the optimization
e) Strain before the optimization
f) Strain after the optimization
4.1. Statics analysis
The planes A1, A2 and A3 are fully constrained, and the uniform load of 1000 N along the positive direction of $Y$ is applied on the planes A4, A5 and A6. Fig. 9 gives the distributions of the displacement, stress and strain for original and optimized honeycomb cores. The nodal displacement is corrugated from the left to the right, and decreases. The maximum displacement occurs at the cell located in the bottomleft of the honeycomb core, and the maximum stress and strain are at the bottomleft cell connections. The maximum displacement, stress and strain decrease by 50.70 %, 51.69 % and 47.45 % after the cell optimization, respectively.
4.2. Modal analysis
The modal analysis is carried out by Lanczos algorithm, and the frequencies and mode shapes of original and optimized honeycomb cores are obtained. Table 4, Fig. 10 and Fig. 11 give only the first six frequencies and mode shapes due to the greater influence of the lower frequencies on the stability. The first six mode shapes of optimized honeycomb are the same as those of original honeycomb. The second, third, fourth and sixth order frequencies increase by 2.95 %, 13.38 %, 24.29 % and 2.95 % after the optimization, while the first and fifth order frequencies decrease by 2.28 % and 8.33 %.
Table 4. Frequencies and mode shapes of original and optimized honeycomb cores
Frequency order  Before the optimization  After the optimization  
Frequency / (Hz)  Mode shape  Frequency / (Hz)  Mode shape  
1st  167.39  Firstorder shimmy vibration  163.57  Firstorder shimmy vibration 
2nd  357.19  Firstorder torsional vibration  367.73  Firstorder torsional vibration 
3rd  832.18  Firstorder bending vibration  943.55  Firstorder bending vibration 
4th  1109.41  Secondorder bending vibration  1378.84  Secondorder bending vibration 
5th  1252.38  Secondorder shimmy vibration  1148.04  Secondorder shimmy vibration 
6th  1339.38  Secondorder torsional vibration  1378.84  Secondorder torsional vibration 
Fig. 10. Mode shapes of the original honeycomb core
c) Firstorder
b) Secondorder
c) Thirdorder
d) Fourthorder
e) Fifthorder
f) Sixthorder
Fig. 11. Mode shapes of the optimized honeycomb core
c) Firstorder
b) Secondorder
c) Thirdorder
d) Fourthorder
e) Fifthorder
f) Sixthorder
5. Conclusions
Based on the cantilever and symmetric beam models, the equivalent elastic and shear moduli of the basic cell are derived by Energy Method, respectively. Compared with the method of Ref. [15], the accuracies of the formulas are higher since the influences of tensile and bending deformations of the cell wall are considered. The cell structure parameters are optimized with the consideration of inplane tensile/compression and shear mechanical properties, and the displacement, stress, strain, frequency and vibration mode of original and optimized honeycomb cores are analyzed. The maximum displacement, stress and strain of the honeycomb core decrease by 50.70 %, 51.69 % and 47.45 % after the cell optimization, thus weakening the stress concentration and deformation and increasing the strength and stiffness. The natural frequencies of optimized honeycomb core mostly increase and are all beyond the excitation frequency range, indicating that the optimized structure is less prone to the resonance.
Acknowledgements
This work was supported by the National Natural Science Foundation of China (Grant No. 51805369), Science and Technology Planning Project of Tianjin (Grant No. 20YDTPJC00820) and Natural Science Foundation of Tianjin (Grant No. 18JCYBJC89000).
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Cited By
International Transactions on Electrical Energy Systems
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