Research Article | Open Access

Jianlin Zhong, Jie Ren, Dawei Ma, "Study on the Deformation and Stress Analysis of the Sponge/Rubber Adapter", *Mathematical Problems in Engineering*, vol. 2018, Article ID 9730540, 14 pages, 2018. https://doi.org/10.1155/2018/9730540

# Study on the Deformation and Stress Analysis of the Sponge/Rubber Adapter

**Academic Editor:**Alkis S. Paipetis

#### Abstract

The analysis of adaptors’ deformation and stress is an important prerequisite for the design of the adapters. This paper proposed the mathematical description and analytical method for the sponge cylinder and rubber cylinder under pressure. The analytical formulas on deformation and stress of interference fit between adapters and launchers are deduced. Also, the correctness of the analytical formula is verified by numerical simulation. Furthermore, the effect of precompression and the sponge’s thickness ratio on adapter’s deformation and stress is studied. The following results can be concluded: the results of numerical simulation are basically consistent with that of analytical formula. After installing the adapter into the launcher, the rubber layer will move inward as a whole, then the sponge layer and the rubber layer are subjected to radial and tangential compressive stress. When the precompression is smaller than 0.0075 or larger than 0.0015, the deformation and stress of adapter are approximately in proportion to precompression. If the precompression keeps constant, the deformation and stress of adapter will have extremum when the thickness ratio of sponge equals to a certain value.

#### 1. Introduction

In the cold launching system, there are elastic cushions for adapters between the missile and the metal cylinder. The adapter is usually glued by the sponge cylinder and the rubber cylinder [1–3], as shown in Figure 1. During the ejection of the missile, the friction between the adapter and the launcher could reduce the ejection height of the missile and is determined by the radial stress caused by the adapter’s compression deformation [4]. Therefore, the study of adapters’ deformation and stress has an important engineering application value for the design of adapters.

As the adapter’s deformation and stress analytical research is based on the study on sponge cylinder and the rubber cylinder, many studies have been conducted in recent years. The modeling of mechanical characteristics of sponge material is studied by Koohbor B et al. [5–7] and is verified with experiments. Liang et al. [8] simulate the damping performance of the sponge components using the neural network theory. Based on the study on identification process of mechanical properties of rubber materials, the constitutive equations for small strain and large strain are proposed by Hao H et al. [9, 10]. Lee H S et al. [11, 12] studied the deformation characteristics of rubber cylinders subjected to torsion, axial force, radial force, and skew load. The radial stiffness formula of rubber cylinder is derived by Horton J M [13], and the theoretical analytical formula and experimental data are compared and verified. Yu Z et al. [14, 15] give an analytical solution for the interference fit between superelastic incompressible rubber and linear elastic material under a certain plane strain condition. Nevertheless, there are few reports on the stress and deformation modes of the sponge/rubber adapters.

In this paper, the interference fit between the adapter and the launcher is simplified as an axisymmetric plane strain problem. Based on the Blatz-Ko strain energy function of the sponge material and the three time reduced polynomial constitutive model of rubber material, the differential equation description and the plane axisymmetric analytical solution of the sponge cylinder and the rubber cylinder are proposed. Then, the analytical formulas on deformation and stress of interference fit between adapters and launchers are deduced and the correctness of the analytical formula is verified by numerical simulation. Furthermore, the effect of precompression and the sponge’s thickness ratio on adapter’s deformation and stress is studied. The research methods and results in this paper can provide reference for the design of adapters

#### 2. Mathematical Description of Sponge Cylinder under Compression

##### 2.1. Differential Equation Description of Sponge Cylinder

According to the study of Ju et al. [16], Poisson’s ratio of sponge is approximately 0 when pressed, assuming that the load and boundary conditions are axisymmetric, it can be simplified as an axisymmetric plane strain problem. In the initial stage, the inner and out radius of sponge cylinder are, respectively, and , and then turn into and after deformation under the action of inner pressure of and out pressure of . The cylindrical coordinate system is adopted with the material coordinate of and the spatial coordinate of . Because of the axisymmetric plane strain problem, the deformation mode can be set aswhere is the elongation of the cylinder in direction.

According to (1), the main elongations of the deformation gradient are

Sponge and rubber can produce large nonlinear deformation. The strain energy function is usually used to describe the deformation properties of the material [14]. Sponge is a hyperelastic compressible material whose strain energy function is a function of 3 main elongations, namely, . The Cauchy stress in the 3 main elongation directions is [17]

The axisymmetric plane strain problem should satisfy the static equilibrium equation with ignorance of gravity [18].

Equation (3) is substituted into (4):

At present, the strain energy functions for compressible materials mainly consist of Ogden-Hill and Blatz-Ko strain energy function. The Blatz-Ko strain energy function has a simple form and can describe the deformation characteristics of compressible sponge material, and its strain energy function is [19]where is the shear modulus of sponge in a natural state.

Equation (6) is substituted into (5):where .

##### 2.2. Differential Equation Analysis

Set , and then take derivative of R to obtain

The expression of intermediate variable and (8) are substituted into (7):

The integral solution is applied on the ordinary differential equations (9), and the deformation function of the sponge cylinder can be obtained.

where and are integral constant and are related to boundary conditions.

The Cauchy stress in three directions could be obtained by combining (3) and (6).

##### 2.3. Dimensionless of Deformation and Stress

represents the dimensionless radius before deformation, represents dimensionless radius after deformation and () is the dimensionless stress, , , , and then (10) and (11) could be

#### 3. Mathematical Description of Rubber Cylinder under Compression

##### 3.1. Differential Equation Description of Rubber Cylinder

If the axial length is far greater than the thickness, in the axisymmetric problem, the axial direction of rubber cylinder can not be extended or shortened, so it can be simplified as axisymmetric plane strain problem, the calculation method of deformation mode, and main elongation are consistent with sponge cylinder. As rubber is superelastic material, its constitutive relation is defined by the partial derivative of the corresponding strain energy function [20, 21].

where is the Cauchy stress deviation, is volume ratio before and after deformation, is tensor deviation operator, is the strain energy density converted by unit volume before deformation, is the deformation gradient tensor, then , [22]; , ; , ; .

For incompressible sponge material, . In terms of axisymmetric plane strain problem, (15) can be written as

It could be obtained from (15) aswhere is the hydrostatic pressure.

Equation (4) is the partial derivative of present coordinate of ; combining with (2), it could be written as the equation of initial coordinate .

The differential equation of axisymmetric plane strain could be obtained by submitting (16) into (17).

##### 3.2. Differential Equation Analysis

In this paper, the three-reduced polynomial constitutive model is used as the strain energy function of the rubber material. Because the volume of the rubber is incompressible, the strain energy function of the rubber is as follows [23, 24]:

In terms of axisymmetric plane strain, and (19) is submitted into (18) to obtain

As the rubber is incompressible and combining with (2),

The deformation function of rubber cylinder could be obtained by integral.where is integral constant and is determined by the boundary condition.

Equations (21) and (22) are substituted into (20):

By integrating (23), the radial stress of rubber cylinder is as follows:where is integral constant and is determined by the boundary condition.

Combining (16) with (24), the tangential stress of the rubber cylinder is as follows:

##### 3.3. Dimensionless of Deformation and Stress

Setting , which represents the dimensionless radius before deformation, represents the dimensionless radius after deformation, represents the dimensionless stress, , , , and , where is the parameter of the Baltz-Ko constitutive model of the sponge. Then the corresponding deformation mode and stress can be written as

#### 4. Analysis of Interference Fit between Adapters and Launchers

##### 4.1. Geometric Description

Schematic diagram of interference fit between adapters and metal launchers is shown in Figure 2. The materials from inside to the outside are sponges, incompressible rubber, and isotropic metals and are, respectively, assigned as material 1, material 2, and material 3. The subscript numbers 1, 2, and 3 in variable correspond to material 1, material 2, and material 3. The variable with subscript I has relationships with inner surface of adapter, which with subscript M has relationships with adhesive surface; the variable related to outer surface of launchers is marked with subscript O.

The outer radius of launcher before deformation is and the inner radius is . Similarly, the adapter’s outer radius is before deformation, inner diameter is , and the adhesive surface radius is . The interference fit is adopted between rubber’s outer diameter and launcher’s inner diameter, and the precompression is . After the installation of adapter into the launcher, the radius after deformation is, respectively, as follows, for the launchers, the outer radius is and the inner is . For the adapter, the outer radius is , the adhesive radius is and the inner radius is . Nevertheless, and are all unknown and the outer surface pressure of launcher is 0.

##### 4.2. Axisymmetric Plane Strain Solution for Launcher

Considering that the mechanical properties of the launcher are isotropic and without volume force, the boundary value problem is attributed to [25–28]

where is the stress function and is the function of and under polar coordinates. For the axisymmetric issue, is the function of and has nothing with .

If the stress function is known, then its stress could be expressed as [25–28]

Considering the operator of , then (29) could be written as

The integrating on (32) to obtain

Then the corresponding stress component is as follows:

where , , , and are the integral constant, which are determined by the boundary condition and single value condition of displacement.

Considering the axial symmetry, the small deformation geometric function is as follows:

And the constitutive function of plane stress is as follows:

The strain component could be calculated by constitutive (35b) and then be submitted into boundary value (30). Due to the single value condition of the displacement, the and the integral constants can be obtained.

Assuming that , , and , the dimensionless is carried out on (36) and (37) to obtain

##### 4.3. Equation Solving of Interference Fit Problem

Before the adapter installing into the launcher, the sizes of adapter are, respectively, , , . The size of launcher before deformation is . As is known, is obtained after the adapter installing into launcher.

From (39), the relation between the inner surface pressure and the radial displacement of the launcher could be obtained.

The inner radius of launcher after deformation is

Equation (41) could be written as

where and .

According (22), the radius expression of adapter and adhesive surface after deformation is

After the deformation of adapter, the radial pressure of the outer diameter of the rubber layer and the inner diameter of the launcher must be equal. According to (24), the radial pressure expression of the inner layer of the launcher can be written out.

Equation (42) is submitted into (45), then

The following two equations can be obtained by bringing the initial internal and external radius of the material 1 in the adapter into (12).

Considering the radius of the adapter’s adhesive surface after deformation, (44) is brought into (13):

Due to the assumption that the body is rigid, the inner diameter of the adapter will not deform, so the inner diameter of the adapter is known and can be obtained:

As the spongy and rubber materials are in a continuous radial stress in the adhesive surface, a similar equation (46) can be written out.

According to , could be obtained at the cohesive surface, where . could be obtained based on (44); thus (51) could be written as (51).

Equations (46), (47), (48), (49), (50), and (51) are transformed properly, and they are rewritten into equations forms.where .

The nonlinear equation group (53) is calculated by using Newton-Raphson method [29, 30], and the , , , , , and could be obtained, and then the deformation and stress of the interference fit for the adapter and the launcher could be obtained.

##### 4.4. Example Verification and Analysis

The precompression of the adapter is 0.005161 in a certain missile launching system, the dimensionless sizes are , , , and . The material parameters of adapter and launcher are , , , , and . The finite element software ANSYS is adopted and the radial displacement, radial stress, and tangential stress curves of adapter and launcher are obtained, as shown in Figure 5.

From Figures 3–5, the displacement, radial stress, and tangential stress of analytical solution are consistent with that of the finite element. As a result, the analytic formula of interference fit of deformation and stress is deduced correctly in this paper, which is applicable to the sponge cylinder, the rubber cylinder, the adapter, and the launcher.

The maximum absolute value of adapter’s displacement is 0.0040772 in Figure 3, which appears on the adhesive surface and is larger than the precompression of adapter. As indicated, the rubber layer will move onward as a whole when the adapter is subjected to pressure. The maximum absolute value of adapter’s outer surface displacement is 0.0038593 with an inward movement. After the installation of adapter into the launcher, every point in the launcher moves outward; the maximum displacement of launcher appears on the interference fit surface with the value of 1.663775 × 10^{−5}, which is far smaller than that of adapter. The outer surface displacement of launcher is 1.66361 × 10^{−5}.

It could be concluded in Figure 4 that the absolute value of sponge’s radial stress in the adapter turns small from the inside to the outside, while that of rubber layer turns large. From inside to outside, the absolute value of radial stress in launcher reduced to 0, and the three materials are all subjected to compression. The absolute value of the radial stress of the inner adapter is 1.5141, that on the adapter surface is 1.4999, and that on the interference fit between the adapter and the launcher is 1.8462.

In view of Figure 5, the absolute value of tangential stress of inner sponge layer in the adapter is 0.36058, which increase along the radial direction, and that of outer sponge layer reaches 0.37337. For the absolute value of tangential stress in the rubber layer, it is 0.36058 in the inner surface and decreases radially and then reduces to 7.7368 on the outer surface. The tangential stress for the whole adapter is compressive stress while that of launcher is tensile stress. The tensile stress is 56.481 in the inner surface of launcher and decrease radically, which is 54.664 in the outer layer.

#### 5. Analysis on the Deformation and Stress Effects of Adapters

##### 5.1. Effect of Precompression on the Deformation and Stress

Figures 6–13 are effect curves of precompression , respectively, to radial stress of inner sponge (), to the tangential stress of inner sponge () and outer surface (), the radial displacement of outer sponge (), the radial stress of outer sponge (), the tangential stress of inner rubber () and outer surface (), the tangential stress of the outer rubber surface (), the radial displacement of inner launcher () and the outer radial displacement (), the tangential stress of the inner launcher (), and tangential stress of outer surface ().

From Figures 6–13, the effects of to , , , , , , , , and are divided onto three stages:

(1) When at the first stage, , , , , , , , , and is approximately proportion to the precompression . The absolute value of proportional coefficient is small and the precompression varies largely, while the corresponding stress and displacement change little.

(2) When at the second stage, with the change of precompression , the change rates of , , , , , , , , and are getting faster and faster.

(3) When at the third stage, the precompression changes little while the corresponding stress and displacement change largely.

##### 5.2. Effect of Thickness Ratio of the Sponge Layer on the Deformation and Stress

The thickness ratio of sponge layer is defined as , where is radial thickness of sponge layer and is the radial thickness of the rubber. is defined as the ratio of precompression of adapter to sponge layer’s thickness, is the precompression of adapter, and . When , 0.3, and 0.4, Figures 14–25 are, respectively, the effect curves of thickness ratio to the radial stress of the inner sponge surface (), the tangential stress of inner sponge (), the radial displacement of outer sponge surface (), the radial stress of outer sponge surface (), the tangential stress of outer sponge surface (), the tangential stress of inner rubber surface (), the radial stress of outer rubber surface (), the tangential stress of the outer rubber surface (), the radial displacement of the inner launcher surface (), the tangential stress of the inner launcher surface (), the radial displacement of outer launcher surface (), and tangential stress of outer surface ().

As shown in Figures 14, 15, 18, 20, and 20–25, the absolute values of stresses , , , , , , , and change with , which first increase and then decrease with the maximum extremum point. When , 0.3, 0.4, the horizontal ordinates of and with the maximum value are, respectively, 0.14499, 0.16984, and 0.20795. The horizontal ordinates of the corresponding maximum point of , , , , , and are, respectively, 0.10936, 0.13422, and 0.17482. Furthermore, the horizontal ordinate of the maximum point is smaller than that of and and increases with the . In view of Figures 16, 19, and 21, , , and are approximately in proportion to , when , is approximately linear with .

#### 6. Conclusions

In this paper, the deformation and stress analytical formula of interference fit among the sponge cylinder, rubber cylinder, the adapter, and the launcher is deduced based on the assumption of axisymmetric plane. The deformation of adapter and the stress analytical solution are obtained and are verified by numerical simulation. The effects of precompression and the thickness ratio of sponge layer on the adapter’s deformation and stress are studied. The following conclusions can be obtained.

(1) When the adapter carried out interference fit with launcher, the numerical simulation of radial displacement, radial stress, and tangential stress is consistent with that analytical solution, indicating that the derivation of the analytical formula for deformation and stress is correct.

(2) After the installation of adapter into the launcher, its outer surface moves inward and the displacement with the maximum absolute value appears on the adhesive surface. The rubber layer moves inward as a whole and each point in the launcher moves outward; the maximum displacement of the launcher is on the interference fit surface. For the sponge layer, the absolute value of the radial stress decreases from inside to outside, while for the rubber layer, the absolute value of the radial stress increases from inside to outside, and that of the launcher reduces from inside to outside until 0. The three materials are all subjected to pressure. In terms of the tangential stress, that of the sponge layer increases along the radius while that of rubber layer decreases. The tangential stress of adapter is compressive stress while that of the launcher is tensile stress and decreases radially.

(3) When the precompression is smaller than 0.0075 or larger than 0.0105, , , , , , , , , and are approximately in proportion to precompression . When is smaller than 0.0075, the absolute value of corresponding stress and displacement increases slightly, while is larger than 0.0105 that increases sharply.

(4) The absolute values of stresses , , , , , , , and vary with , which increase firstly and then decrease with a extremum. The horizontal ordinate increases with . , , and are approximately in proportion with , and when , is approximately linear with .

#### Appendix

The cylindrical coordinate system is adopted with the material coordinates of and the spatial coordinate of . Because of the axisymmetric plane strain problem, the deformation mode can be set aswhere is the elongation of the cylinder in direction.

According to (A.1), the main elongation of the deformation gradient is

Sponge is a hyperelastic compressible material whose strain energy function is a function of 3 main elongations; that is, . The Cauchy stress in the 3 main elongation directions is

The axisymmetric plane strain problem should satisfy the static equilibrium equation with ignorance of gravity.

Equation (3) is substituted into (4):

From (A.2),

Equation (A.6) is substituted into the equations (A.5):

From (A.7),

From (A.6),

Equation (A.9) is substituted into (A.8):

As , and is the single valued function:

Equation (A.11) is substituted into (A.10); take into consideration:

The Blatz-Ko strain energy function,

From (A.13),

Equation (A.14) is substituted into (A.10):

From (A.15),

#### Data Availability

The data used to support the findings of this study are available from the corresponding author upon request.

#### Conflicts of Interest

The authors state that there are no conflicts of interest regarding the publication of this paper.

#### Acknowledgments

The authors gratefully acknowledge the financial supports from Innovation Partnership Fund for Universities of China Aerospace Science and Technology Corporation (CASC) and Natural Science Funds for Young Scholar of Jiangsu Province (no. BK 20170837).

#### References

- K. Dominguez, “Methods of connecting testing equipment to a missile system,” Tech. Rep. 9,739,568, U.S. Patent, 2017. View at: Google Scholar
- A. B. Shelton, C. Martin, and W. A. Silva, “Computing aerodynamic damping of a generic missile with CFD,” in
*Proceedings of the AIAA Aerospace Sciences Meeting*, 2018. View at: Publisher Site | Google Scholar - M. S. R. Chandra Murty, P. K. Sinha, and D. Chakraborty, “Effect of rocket exhaust of canisterized missile on adjoining launching system,”
*Proceedings of the Institution of Mechanical Engineers, Part G: Journal of Aerospace Engineering*, vol. 231, no. 11, pp. 2085–2097, 2017. View at: Publisher Site | Google Scholar - S. Irish Angelin, S. Raja, N. Rajesh et al., “Ap-plicability of canister for barraging missiles,”
*International Review of Aerospace Engineering*, vol. 2, no. 6, pp. 86–90, 2015. View at: Google Scholar - B. Koohbor, A. Kidane, and W.-Y. Lu, “Characterizing the constitutive response and energy absorption of rigid polymeric foams subjected to intermediate-velocity impact,”
*Polymer Testing*, vol. 54, pp. 48–58, 2016. View at: Publisher Site | Google Scholar - B. Su, Z. Zhou, G. Xiao, Z. Wang, X. Shu, and Z. Li, “A pressure-dependent phenomenological constitutive model for transversely isotropic foams,”
*International Journal of Mechanical Sciences*, vol. 120, pp. 237–248, 2017. View at: Publisher Site | Google Scholar - C. Beckmann and J. Hohe, “A probabilistic constitutive model for closed-cell foams,”
*Mechanics of Materials*, vol. 96, pp. 96–105, 2016. View at: Publisher Site | Google Scholar - G. Liang and K. Chandrashekhara, “Neural network based constitutive model for elastomeric foams,”
*Engineering Structures*, vol. 30, no. 7, pp. 2002–2011, 2008. View at: Publisher Site | Google Scholar - D. Hao, D. Li, and Y. Liao, “A finite viscoelastic constitutive model for filled rubber-like materials,”
*International Journal of Solids and Structures*, vol. 64, pp. 232–245, 2015. View at: Google Scholar - J. Chen, M. Huang, and X. Wang, “Typical constitutive models of rubber materials and their ranges of application,”
*International Materials Reviews*, 2015. View at: Google Scholar - H. S. Lee, J. K. Shin, S. Msolli, and H. S. Kim, “Prediction of the dynamic equivalent stiffness for a rubber bushing using the finite element method and empirical modeling,”
*International Journal of Mechanics and Materials in Design*, pp. 1–15, 2017. View at: Google Scholar - N. Zhang, N. Hoang, and H. Du, “A novel dynamic absorber using enhanced magnetorheological elastomers for powertrain vibration control,”
*Advanced Materials Research*, vol. 47-50, pp. 117–120, 2008. View at: Publisher Site | Google Scholar - J. M. Horton and G. E. Tupholme, “Approximate radial stiffness of rubber bush mountings,”
*Materials and Corrosion*, vol. 27, no. 3, pp. 226–229, 2006. View at: Publisher Site | Google Scholar - Y. Zhou, Z. Zhuang, and H. Kezhi, “The solutions of axiymmetric plane stress for a hyperelastic material interference problem,”
*Engineering Mechanics*, vol. 21, no. 6, pp. 72–75, 2004. View at: Google Scholar - Y. Anani and G. H. Rahimi, “Field equations and general solution for axisymmetric thick shell composed of functionally graded incompressible hyperelastic materials,”
*International Journal of Mechanical Sciences*, 2017. View at: Google Scholar - M. L. Ju, H. Jmal, R. Dupuis, and E. Aubry, “Visco-hyperelastic constitutive model for modeling the quasi-static behavior of polyurethane foam in large deformation,”
*Polymer Engineering & Science*, vol. 55, no. 8, pp. 1795–1804, 2015. View at: Publisher Site | Google Scholar - M. El Hamdaoui, J. Merodio, and R. W. Ogden, “Loss of ellipticity in the combined helical, axial and radial elastic deformations of a fibre-reinforced circular cylindrical tube,”
*International Journal of Solids and Structures*, vol. 63, pp. 99–108, 2015. View at: Publisher Site | Google Scholar - E. Kirkinis, R. W. Ogden, and D. M. Haughton, “Some solutions for a compressible isotropic elastic material,”
*Journal of Applied Mathematics and Physics*, vol. 55, no. 1, pp. 136–158, 2004. View at: Publisher Site | Google Scholar | MathSciNet - Q. Zhang and J. A. Blume, “Surface wrinkling in generalized Blatz–Ko materials,”
*Extreme Mechanics Letters*, vol. 11, pp. 68–76, 2017. View at: Publisher Site | Google Scholar - H. Guo, W. Guo, and A. V. Amirkhizi, “Constitutive modeling of the tensile and compressive deformation behavior of polyurea over a wide range of strain rates,”
*Construction and Building Materials*, vol. 150, pp. 851–859, 2017. View at: Publisher Site | Google Scholar - H. Shokrollahi, F. Fallah, and M. H. Kargarnovin, “An approach in deformation and stress analysis of elasto-plastic sandwich cylindrical shell panels based on harmonic differential quadrature method,”
*Journal of Sandwich Structures and Materials*, vol. 19, no. 2, pp. 167–191, 2017. View at: Publisher Site | Google Scholar - Z. Yang, Y. Liu, B. Tian, and Y. Zhang, “Hot deformation and dynamic recrystallization of TiC(30vol%)/Cu-Al2O3 composites,”
*Acta Materiae Compositae Sinica*, vol. 32, no. 1, pp. 117–124, 2015. View at: Google Scholar - S. G. Cho, W. K. Park, and S. M. Yun, “Finite element analysis of lead rubber bearing by using strain energy function of hyper-elastic material,”
*Journal of The Korean Society of Civil Engineers*, vol. 36, no. 3, pp. 361–374, 2016. View at: Publisher Site | Google Scholar - M. Bahreman and H. Darijani, “New polynomial strain energy function; application to rubbery circular cylinders under finite extension and torsion,”
*Journal of Applied Polymer Science*, vol. 132, no. 13, 2015. View at: Google Scholar - N. Perez, “Theory of elasticity,” in
*Fracture Mechanics*, Springer International Publishing, 2017. View at: Publisher Site | Google Scholar - K. Gou, M. Mallikarjuna, K. R. Rajagopal, and J. R. Walton, “Modeling fracture in the context of a strain-limiting theory of elasticity: a single plane-strain crack,”
*International Journal of Engineering Science*, vol. 88, pp. 73–82, 2015. View at: Publisher Site | Google Scholar | MathSciNet - R. Ansari, A. Shahabodini, and M. Faghih Shojaei, “Nonlocal three-dimensional theory of elasticity with application to free vibration of functionally graded nanoplates on elastic foundations,”
*Physica E: Low-dimensional Systems and Nanostructures*, vol. 76, pp. 70–81, 2016. View at: Publisher Site | Google Scholar - A. Pourasghar and Z. Chen, “Thermoelastic response of CNT reinforced cylindrical panel resting on elastic foundation using theory of elasticity,”
*Composites Part B: Engineering*, vol. 99, pp. 436–444, 2016. View at: Publisher Site | Google Scholar - R. McGill and P. Kenneth, “Solution of variational problems by means of a generalized newton-raphson operator,”
*Aiaa Journal*, vol. 2, no. 10, p. 28, 2015. View at: Google Scholar - W. Nazeer, A. Naseem, S. M. Kang, and Y. C. Kwund, “Generalized Newton Raphson’s method free from second derivative,”
*Journal of Nonlinear Science and Applications*, vol. 9, no. 5, pp. 2823–2831, 2016. View at: Publisher Site | Google Scholar

#### Copyright

Copyright © 2018 Jianlin Zhong et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.