DSpace at VNU: Vibration and Nonlinear Dynamic Analysis of Imperfect Thin Eccentrically Stiffened Functionally Graded Plates in Thermal Environments

VNU Journal of Science: Mathematics – Physics, Vol 32, No (2016) 1-19 Vibration and Nonlinear Dynamic Analysis of Imperfect Thin Eccentrically Stiffened Functionally Graded Plates in Thermal Environments Pham Hong Cong, Nguyen Dinh Duc* University of Engineering and Technology, Vietnam National University, Hanoi, 144 Xuan Thuy, Cau Giay, Hanoi, Vietnam Received 20 August 2015 Revised 27 February 2016; Accepted 14 March 2016 Abstract: This paper presents an analytical approach to investigate the vibration and nonlinear dynamic response of imperfect thin eccentrically stiffened functionally graded material (FGM) plates in thermal environments using the classical plate theory, stress function and the Lekhnitsky smeared stiffeners technique Material properties are assumed to be temperature-dependent, and two types of thermal condition are investigated: the uniform temperature rise; and the temperature gradient through the thickness Numerical results for vibration and nonlinear dynamic response of the imperfect eccentrically stiffened FGM plates are obtained by the Runge-Kutta method The results show the influences of geometrical parameters, material properties, imperfections, eccentric stiffeners, and temperature on the vibration and nonlinear dynamic response of FGM plates The numerical results in this paper are compared with the results reported in other publications Keywords: Vibration, nonlinear dynamic response, thin eccentrically stiffened FGM plates, classical plate theory, thermal environments Introduction∗ Functionally graded materials (FGMs) are homogeneous composite and microscopic-scale materials with the mechanical and thermal properties varying smoothly and continuously from one surface to the other Typically, these materials are made from a mixture of metal and ceramic, or a combination of different metals by gradually varying the volume fraction of the constituent metals The properties of FGM plates are assumed to vary through the thickness of the structure Due to their high heat resistance, FGMs have many practical applications, such as use in reactor vessels, aircrafts, space vehicles, defense industries, and other engineering structures Therefore, many investigations have been carried out on the dynamic and vibration response of FGM plates Woo et al [1] investigated the nonlinear free vibration behavior of functionally graded plates; and Wu et al [2] published their results on the nonlinear static and dynamic analysis of _ ∗ Tel.: 84-915966626 Email: ducnd@vnu.edu.vn P.H Cong, N.D Duc / VNU Journal of Science: Mathematics – Physics, Vol 32, No (2016) 1-19 functionally graded plates Matsunaga [3] studied the free vibration and stability of FGM plates according to a 2D high order deformation theory Allahverdizadeh et al [4] studied the nonlinear free and forced vibration analysis of circular functionally graded plates Alijani et al [5] and Chorfi and Houmat [6] studied the nonlinear vibration response of functionally graded doubly-curved shallow shells Kim [7] studied the geometrically nonlinear analysis of functionally graded material (FGM) plates and shells using a four-node quasi-conforming shell element Mollarazi et al [8] studied analysis of free vibration of functionally graded material (FGM) cylinders by a meshless method Jahanghiry et al [9] have applied the stability analysis of FGM microgripper subjected to nonlinear electrostatic and temperature variation loadings Kamran Asemi et al [10] have investigated the threedimensional natural frequency analysis of anisotropic functionally graded annular sector plates resting on elastic foundations To date, the dynamic analysis of FGM plates with temperature-dependent material properties has received much attention from researchers Huang and Shen [11] studied the vibration and dynamic response of FGM plates in thermal environments and the material properties are assumed to be temperature-dependent Kim [12] studied the temperature-dependent vibration analysis of functionally graded rectangular plates by the finite element method, and the Rayleigh-Ritz procedure was applied to obtain the frequency equation Fakhari and Ohadi [13] studied the nonlinear vibration control of functionally graded plates with piezoelectric layers in thermal environments using the finite element method In their study, the material properties of FGMs have also been assumed to be temperaturedependent and graded in the thickness direction according to a simple power law distribution in terms of the volume fractions of the constituents We should mention that all the above results have been investigated under higher order shear deformation theory using the displacement functions FGM plates, like other composite structures, are usually reinforced by stiffening members to provide the benefit of added load-carrying static and dynamic capability with a relatively small additional weight penalty Investigation of the static and dynamic capability of eccentrically stiffened FGM structures has received comparatively little attention Bich et al studied the nonlinear postbuckling and dynamic response of eccentrically stiffened functionally graded plates [14] and panels [15] Duc [16] investigated the nonlinear dynamic response of imperfect eccentrically stiffened doubly-curved FGM shallow shells on elastic foundations It is noted that in all the publications mentioned above [14, 15, 16], the eccentrically stiffened FGM plates and shells are considered without temperature Duc et al [17, 18] investigated the nonlinear static post-buckling of imperfect eccentrically stiffened FGM doubly-curved shallow shells and plates resting on elastic foundations in thermal environments Bich et al [19] investigated the nonlinear vibration of imperfect eccentrically stiffened FGM doubly-curved shallow shells using the first order shear deformation theory Quan et al [20] investigated the nonlinear dynamic analysis and vibration of shear deformable eccentrically stiffened S-FGM cylindrical panels Duc and Cong [21] studied the nonlinear dynamic response of imperfect FGM plates, and Duc and Quan [22] studied doubly-curved shallow shells In the two studies, stiffeners had not been used, and the study by Duc and Cong [21] did not mention temperature-dependence Recently, Duc et al., [23] studied the nonlinear stability of shear deformable eccentrically stiffened functionally graded plates on elastic foundations with temperature-dependent properties There are no publications on the vibration and nonlinear dynamic response of FGM plates reinforced with eccentric stiffeners under temperature The most difficult part in this type of problem is to calculate the thermal mechanism of FGM plates as well as eccentric stiffeners under thermal loads This paper presents an analytical approach to investigate the vibration and nonlinear dynamic response of imperfect eccentrically stiffened FGM plates with temperature-dependent material properties in thermal environments using classical plate theory, the Lekhnitsky smeared stiffeners P.H Cong, N.D Duc / VNU Journal of Science: Mathematics – Physics, Vol 32, No (2016) 1-19 technique and Bubnov-Galerkin method The study also analysed the effect of temperature, imperfection, geometrical parameters, and volume fraction on the vibration and nonlinear dynamic response of imperfect eccentrically stiffened FGM plates Rectangular eccentrically stiffened FGM plate (ES-FGM) Consider a rectangular ES-FGM plate of length a , width b and thickness h A coordinate system ( x, y, z ) is chosen so that the ( x, y ) plane is on the middle surface of the plate and the z-axis is the thickness direction ( −h / ≤ z ≤ h / ) , as shown in Fig Fig Geometry and coordinate system of an eccentrically stiffened FGM plate The effective properties, modulus of elasticity E , mass density ρ , coefficient of thermal expansion α , and the coefficient of thermal conduction K of the FGM plate can be written as follows [17, 18, 24]: [ E ( z, T ), ρ ( z, T ),α ( z, T ), K ( z, T )] = [ Em (T ), ρm (T ),α m (T ), K m (T )]  2z + h  + [ Ecm (T ), ρcm (T ), α cm (T ), K cm (T )]    2h  k (1) in which the Poisson’s ratio is assumed constant (ν = const ) , Ecm (T ) = Ec (T ) − Em (T ), ρcm (T ) = ρc (T ) − ρ m (T ), α cm (T ) = α c (T ) − α m (T ), K cm (T ) = K c (T ) − K m (T ) and h is the thickness of the plate; ≤ k ≤ ∞ is the volume fraction index; and m and c denote metal and ceramic constituents, respectively Young’s modulus of elasticity E , thermal expansion coefficient α , coefficient of heat transfer K , and mass density ρ can be expressed as a function of temperature, as [24]: Pr = P0 ( P−1T −1 + + PT + P2T + PT ) (2) P.H Cong, N.D Duc / VNU Journal of Science: Mathematics – Physics, Vol 32, No (2016) 1-19 where T = T0 + ∆T ( z ) , T0 is room temperature; and P0 , P−1 , P1 , P2 , P3 are coefficients and dependent only on the constitutent material For brevity, this paper will denote T-D for the temperature-dependent case, and T-ID for the temperature-independent case Governing equations Using classical plate theory for thin plates and geometrical nonlinear cases, the strains at the middle surface and curvatures are related to the displacement components u, v, w in the x, y, z coordinate directions as [24]:  ∂u  ∂w 2  +     ∂x  ∂x     εx    − w, xx    kx     ∂v  ∂w        ε y  =  ∂y +  ∂y   ,  k y  =  − w, yy           γ xy   ∂u ∂v ∂w ∂w   k xy   − w, xy   + +   ∂y ∂x ∂x ∂y    (3) The strains across the plate thickness at a distance z from the mid-surface are:  kx   ε x   ε x0       0  ε y  =  ε y  + z  ky  γ  γ   2k xy   xy   xy    The strains from Eq (3) must be relative in the deformation compatibility equation: 2 ∂ 2ε x0 ∂ ε y ∂ γ xy ∂ w ∂ w ∂ w + − = − ∂y ∂x ∂x∂y ∂x∂y ∂x ∂y (4) (5) Hooke’s law for a plate, including the thermal effects, is: (σ p x σ xyp E ( z,T ) [(ε x , ε y ) + ν ( ε y , ε x ) − (1 + ν )α ( z, T ) ∆T ( z )(1,1)] −ν E ( z,T ) = γ xy 2(1 + ν ) ,σ yp ) = (6) and for the stiffeners [24] is: (σ xst , σ yst ) = E0 (ε x , ε y ) − E0 α (T )∆T (1,1) − 2ν (7) Where ∆T is the temperature rise in the plate, and ∆T = ∆T ( z ) in the general case E ( z , T ) and α ( z, T ) are defined by Eq (2) E0 (T ) and α (T ) are Young’s modulus and the thermal expansion coefficient of stiffeners The FGM plate reinforced by eccentric longitudinal and transverse stiffeners is shown in Fig.1 E0 is the elasticity modulus in the axial direction of the corresponding stiffener, which is assumed to be identical for both types of longitudinal and transverse stiffeners In order to provide continuity between the plate and stiffeners, it is assumed that the stiffeners are made of full P.H Cong, N.D Duc / VNU Journal of Science: Mathematics – Physics, Vol 32, No (2016) 1-19 metal ( E0 = Em ) if putting them at the metal-rich side of the plate, and conversely, full ceramic stiffeners ( E0 = Ec ) at the ceramic-rich side of the plate The contribution of stiffeners can be accounted for using the Lekhnitsky smeared stiffeners technique Then integrating the stress-strain equations and their moments through the thickness of the plate, the expressions for force and moment resultants of an eccentrically stiffened FGM plate are obtained [24]: E0T A1T )ε x + P12ε y0 + ( J11 + F1T )k x + J12 k y + Φ1 T s1 N x = ( P11 + N y = P12ε x0 + ( P22 + E0T A2T )ε y + J12 k x + ( J 22 + F2T )k y + Φ1 s2T N xy = P66γ xy0 + J 66 k xy (8a) ET I T M x = ( J11 + F )ε + J12ε + ( H11 + T )k x + H12 k y + Φ s1 T x y M y = J12ε x0 + ( J 22 + F2T )ε y0 + H12 k x + ( H 22 + E0T I 2T )k y + Φ s2T M xy = J 66γ xy0 + H 66 k xy where: P11 = P22 = E1 E1 Eν , P12 = , P66 = −ν −ν 2(1 + ν ) E2 Eν E2 , J12 = 2 J 66 = 2(1 +ν ) −ν −ν E3 Eν E3 H11 = H 22 = ,H = ,H = −ν 12 −ν 66 2(1 + ν ) J11 = J 22 = h E ( z )α ( z )∆T ( z ) dz −ν Φ1 = − ∫ 2h − h h − Φ2 = −∫ (8b) E ( z )α ( z ) z ∆T ( z ) dz −ν E (T)  Ecm (T )kh  E1 =  E m (T)+ cm h , E = , k +  2( k + 1)(k + 2)   Em (T ) E3 =   12 +E cm (T)( 1  − + ) h , k + k + 4k +  T I1T = F1T T d (h ) d1T (h1T )3 T T T + A1T ( z1T ) , I = 2 + A2 ( z2 ) 12 12 E0 A1T z1T E0 A2T z2T T = , F2 = s1T s2T z1T = h1T + hT T h2T + hT , z2 = 2 P.H Cong, N.D Duc / VNU Journal of Science: Mathematics – Physics, Vol 32, No (2016) 1-19 in which d1T = d1 (1 + α m ∆T ( z )), d 2T = d (1 + α m ∆T ( z )), z1T = z1 (1 + α m ∆T ( z )), z2T = z2 (1 + α m ∆T ( z )), T (9) T s = s1 (1 + α m ∆T ( z )), s = s2 (1 + α m ∆T ( z )) where s1 , s2 are the spacings of the longitudinal and transverse stiffeners; I1 , I , z1 , z2 are the second moments of the cross-section areas and the eccentricities of the stiffeners with respect to the middle surface of the plate, respectively; and the width and thickness of the longitudinal and transverse stiffeners are denoted by d1 , h1 and d , h2 , respectively The quantities A1 , A2 are the crosssectional areas of the stiffeners The nonlinear motion equation of the ES-FGM plate based on classical plate theory with Volmir’s 2 assumption [25] u