Accepted Manuscript
Three-dimensional exact solution for the free vibration of arbitrarily thick func-tionally graded rectangular plates with general boundary conditions
Guoyong Jin, Zhu Su, Shuangxia Shi, Tiangui Ye, Siyang Gao
PII: S0263-8223(13)00498-4DOI: http://dx.doi.org/10.1016/j.compstruct.2013.09.051Reference: COST 5383
To appear in: Composite Structures
Please cite this article as: Jin, G., Su, Z., Shi, S., Ye, T., Gao, S., Three-dimensional exact solution for the freevibration of arbitrarily thick functionally graded rectangular plates with general boundary conditions, CompositeStructures (2013), doi: http://dx.doi.org/10.1016/j.compstruct.2013.09.051
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1
Three-dimensional exact solution for the free vibration of arbitrarily
thick functionally graded rectangular plates with general boundary
conditions
Guoyong Jin, Zhu Su*, Shuangxia Shi, Tiangui Ye, Siyang Gao
College of Power and Energy Engineering, Harbin Engineering University,
Harbin, 150001, P. R. China
Corresponding author: Zhu Su
College of Power and Energy Engineering
Harbin Engineering University
Harbin, 150001, P. R. China
86-451-82569458 (phone),
2
Abstract
A new three-dimensional exact solution for the free vibrations of arbitrarily thick
functionally graded rectangular plates with general boundary conditions is presented. The
three-dimensional elasticity theory is employed to formulate the theoretical model. According
to a power law distribution of the volume of the constituents, the material properties change
continuously through the thickness of the functionally graded plates. Each of displacements
of the plates, regardless of boundary conditions, is expanded as a three-dimensional (3-D)
Fourier cosine series supplemented with closed-form auxiliary functions introduced to
eliminate all the relevant discontinuities with the displacements and its derivatives at the
edges. Since the displacement fields are constructed adequately smooth throughout the entire
solution domain, an exact solution is obtained based on Rayleigh-Ritz procedure by the
energy functions of the plate. The excellent accuracy and reliability of the current solutions
are demonstrated by numerical examples and comparison of the present results with those
available in the literature, and numerous new results for thick FG plates with elastic boundary
conditions are presented. The effects of gradient indexes are also illustrated.
Keywords: functionally graded plates; three-dimensional elasticity theory; elastically
restrained edge; free vibration
3
1. Introduction
Functionally graded materials (FGMs) are a new class of composites structures that are
designed so that material properties vary smoothly and continuously along desired directions.
This is achieved by gradually varying the volume fraction of the constituent materials,
usually in the thickness direction only. The continuity of the material properties can
overcome problems arising from conventional laminated composite structures such as lager
inter-laminar stresses. Therefore, FGMs have attracted much interest since they were first
introduced by Japanese scientists in 1984. In recent years, the increasing utilization of FG
materials has motivated more intensive research activities. The FG plates are widely used in
various engineering applications, such as aircraft, space vehicles and nuclear, and in some
case they are frequently subjected to dynamic loads, which may cause fatigue damage and
severe reductions in the strength and stability of the structures. Therefore a thorough
understanding of their vibration characteristics is essential for designers and engineers.
As far as the plate deformation theories in previous studies are concerned, there are a
significant number of two-dimensional (2-D) theories. A partial classification of 2-D models
is briefly introduced here, including classical plate theory (CPT), first-order shear
deformation plate theory (FSDT), higher-order deformation plate theory (HSDT). More
detailed descriptions regarding the development of researches on this subject may be found in
several monographs respectively by Quta [1], Reddy [2], Carrera [3] and some survey articles
[4-7]. The CPT which is the simplest theory neglects the effects of shear and normal
deformations in the thickness direction. There are some studies regarding FG plates which are
4
based on the CPTs [8-13]. Although this theory gives sufficiently accurate results for thin
plates, it is not valid for the vibration analysis of the moderately thick and thick plates. In
order to eliminate the deficiency of the CPT, the effects of transverse shear deformations is
considered, and the FSDT were developed. There exist a large number of studies regarding
FG plates based on FSDTs [14-21]. Since the transverse shear strains in the FSDT are
assumed to be constant in the plate thickness, the shear correction factors are introduced to
adjust the transverse shear stiffness. However, the value of the shear correction factor is not a
constant but changes with material properties, loading case, boundary conditions. To avoid
the use of the shear correction factors and have a better prediction the FG thick plates, a
number of HSDTs based on the assumption of high-order variations of in-plane
displacements through the plate thickness are used [22-28]. Actually, those two-dimensional
theories reduce the dimensions of the plate problems from three to two by making certain
hypotheses on the stress and strain in the thickness direction. These assumptions greatly
simplify the formulation and solution in the analytical and computational methods, but they
also introduce errors at the same time. Since no hypotheses are assumed for the distribution
field of the deformations and stresses in the three-dimensional (3-D) elasticity theory and
contributions of all stresses and strains are considered by accounting for all the elastic
constants, the most accurate representation for the vibration analysis of plates can be obtained
by using the 3-D elasticity theory. Some investigations were carried out based on 3-D
elasticity theory [29-40]. In present work, in order to obtain highly accurate vibration result
for thick FG plates, the three-dimensional elasticity theory is just employed to formulate the
5
theoretical model.
Apart from the aforementioned plate theories, it has also been of great interest for
researchers to develop an accurate and efficient method which can be used to determine the
vibration behaviors of FG plates. Great research efforts have been devoted to this subject in
the past few years. So far, many computational methods are available for the vibration
analysis of FG plates, such as Ritz method [14,34, 36, 38], meshless method [18, 26],
extended Kantorovich method (EKM) [20], finite element method (FEM) [21, 22, 40],
meshless local Petrov-Galerkin (MLPG) method [27, 28], power series method [33],
differential quadrature (DQ) method [37], etc. Most of these methods were subsequently
extended to analyze the dynamic behaviors of FG plates from isotropic plates.
From the review of the literature, most of the previous studies on the FG plates are
confined to the classical boundary conditions, such as free, simply-supported and clamped
and their combinations. However, a variety of possible boundary restraining encountered in
practice engineering applications may not always be classical in nature, and there will always
be some elasticity along the supports, and there is a considerable lack of corresponding
researches regarding the free vibrations of the FG rectangular plates subjected to elastic
boundary conditions.
The objective of the present paper is to provide an accurate and reliable method for
three-dimensional vibration analysis of arbitrarily thick FG rectangular plates with arbitrary
boundary conditions including classical boundary conditions and elastic boundary conditions.
The present work can be considered as an extension of the authors’ previous works [41-43].
6
In this present work, the formulations are based on the three-dimensional elasticity theory.
According to a power law distribution of the volume of the constituents, the material
properties change continuously through the thickness of the functionally graded plates. Each
of displacements of the plates, regardless of boundary conditions, is expanded as a standard
three-dimensional Fourier cosine series supplemented with closed-form auxiliary functions
introduced to eliminate all the relevant discontinuities with the displacement and its
derivatives at the edges. Since the displacement field is constructed adequately smooth
throughout the entire solution domain, an exact solution can be obtained based on
Rayleigh-Ritz method by the energy functions of the plate. Compared with most of the
existing methods, the current method can be applicable to arbitrary boundary conditions
without requiring any special procedures or schemes. The excellent accuracy and reliability
of the current solutions are demonstrated by numerical examples and comparison of the
present results with those available in the literature, and numerous new results for FG plates
with elastic boundary conditions are presented, which can serve as the benchmark solutions
for other numerical methods in the future. The effects of gradient indexes are also illustrated.
2. Theoretical formulations
2.1 Description of the model
The physical dimensions and co-ordinate system of a 3-D FG plate under consideration
are shown in Fig.1(a). The length, width, thickness of functionally graded plate are
represented by a, b and h respectively. The plate geometry and dimensions are defined with
respect to a Cartesian coordinate system (x, y, z), introduced such that the bottom and top
7
surfaces of the plate lie in the plane z=0 and z=h. The displacements of the plate in the x, y
and z directions are denoted by u, v and w, respectively. The general boundary conditions are
represented as three of independent linear springs (ku, kv and kw) placed at the ends, and
different boundary conditions can be obtained by setting proper spring stiffness. For example
a clamped boundary can be obtained by assigning the springs’ stiffness at infinity, and a free
boundary can be obtained by assigning the springs’ stiffness at zero.
Consider FG plates made from a mixture of two material phases, for example, a metal
and a ceramic as shown in Fig. 1(b). Herein, the top surface of the plate is ceramics-rich
whereas the bottom surface is metal-rich. Young’s modulus and density per unit volume are
assumed to vary continuously through the plate thickness according to a power-law
distribution as
( ) ( )c m c mE z E E V E= − + (1)
( ) ( )c m c mz Vρ ρ ρ ρ= − + (2)
in which the subscripts c and m represent the ceramic and metallic constituents, respectively,
and the volume fraction Vc may be given by
(0 )( ) pc
zV z h
h= ≤ ≤ (3)
where z is the thickness coordinate , and p is the gradient index and takes only positive values.
The value of p equal to zero represents a fully ceramic, whereas infinite p indicates a fully
metallic plate. Since the small variations of the Poisson’s ratio, µ, it is assumed to be constant.
Typical values for metal and ceramics used in the FG plates are listed in Table 1.
2.2 Kinematic relations and Constitutive relation
8
According to the linear, small-strain elasticity theory, the strain components, εij (i,j=x, y,
z), are defined in terms of displacements as:
, , ,
, ,
xx yy zz
xy xz yz
u v w
x y z
u v u w v w
y x z x z y
ε ε ε
γ γ γ
∂ ∂ ∂= = =
∂ ∂ ∂
∂ ∂ ∂ ∂ ∂ ∂= + = + = +
∂ ∂ ∂ ∂ ∂ ∂
(4)
Based on Hooke’s law, the stress-displacement relations are defined as:
( ) 2 ( ) ( ) ( ) 0 0 0
( ) ( ) 2 ( ) ( ) 0 0 0
( ) ( ) ( ) 2 ( ) 0 0 0
0 0 0 ( ) 0 0
0 0 0 0 ( ) 0
0 0 0 0 0 ( )
xx xx
yy yy
zz zz
xy xy
xz xz
yz yz
z G z z z
z z G z z
z z z G z
G z
G z
G z
λ λ λ
λ λ λ
λ λ λ
σ ε
σ ε
σ ε
σ γ
σ γ
σ γ
+
+ +
= (5)
for FG plate, since the properties vary through the thickness of the plate with a desired
variation of volume fractions, λ(z) and G(z) are expressed as:
( ) ( )( ) , ( )
(1 )(1 2 ) 2(1 )
E z E zz G z
µλ
µ µ µ= =
+ − + (6)
In this study, the general boundary condition along each edge will be described in term
of three sets of restraining springs. Accordingly, the boundary conditions become
0 0 0, , ( 0)xx xy xzux vx wxk u k v k w xσ σ σ= = = = (7)
, , ( )uxa xx vxa xy wxa xzk u k v k w x aσ σ σ= = = = (8)
0 0, , ( 0)yy xy wyo yzuy vyk u k v k w yσ σ σ= = = = (9)
, , ( )yy xy yzuyb vyb wybk u k v k w y bσ σ σ= = = = (10)
where kux0, kvx0, kwx0, kuxa, kvxa and kwxa denote the six sets springs stiffness along the
9
edges x=0 and x=a while kuy0, kvy0, kwy0, kuyb, kvyb and kwyb denote the another six sets
springs stiffness along the edges y=0 and y=b.
2.3 Admissible displacement functions
Constructing of appropriate admissible displacement functions is of crucial importance
in the present method. In practice, the displacements of the plate are often expanded in the
terms of the beam functions under the same boundary conditions. Thus, there requires a
specific customized set of beam functions for each type of boundary conditions. This results
in that the use of this approach is inconvenient and will result in very tedious calculations.
Instead of the beam functions, one can also use other forms of admissible functions such as
simple or orthogonal polynomial and trigonometric functions. The lower order polynomials
cannot form a complete set, and the higher order polynomials trend to become numerically
unstable due to the computer round-off errors. Since the Fourier functions constitute a
complete set and exhibit an excellent numerical stability, a Fourier series representation may
be able to avoid these difficulties. However, the conventional Fourier series expression will
have a convergence problem along the boundary conditions except for a few simple boundary
edges. When the displacements of the plate are expressed in standard Fourier series, there
may be discontinuities in the displacements’ derivatives at the edges. Thus, the solution may
not converge or converge slowly. In order to overcome the difficulty, a modified Fourier
series method was previously proposed for the vibration analysis of elastically supported
isotropic beams [44] and thin plates [45, 46]. Most recently, it was extended by the authors to
analyze the composite laminated shell structures [41, 42] and double-panel cavity structure
10
[43] with general boundary conditions. In this present work, this method is further extended
to the vibration analysis of arbitrarily thick functionally graded rectangular plates. Therefore,
to satisfy the general boundary conditions of the thick 3-D rectangular plates, three
displacement functions of the plate are expanded as a modified 3-D Fourier series with
closed-form auxiliary functions:
0 0 0
1 1 2 20 0
3 1 4 20 0
5 1 6 20 0
cos cos cos
[ ( ) ( )]cos cos
( , , , )
[ ( ) ( )]cos cos
[ ( ) ( )]cos cos
mnt mx ny tzm n t
mx nymn z mn zm n
mx tzmt y mt ym t
ny tznt x nt xn t
A x y z
a z a z x y
u x y z t
a y a y x z
a x a x y z
λ λ λ
ξ ξ λ λ
ξ ξ λ λ
ξ ξ λ λ
∞ ∞ ∞
= = =
∞ ∞
= =
∞ ∞
= =
∞ ∞
= =
+ +
=
+ +
+ +
∑∑∑
∑∑
∑∑
∑∑
jwte
(11.a)
0 0 0
1 1 2 20 0
3 1 4 20 0
5 1 6 20 0
cos cos cos
[ ( ) ( )]cos cos
( , , , )
[ ( ) ( )]cos cos
[ ( ) ( )]cos cos
mnt mx ny tzm n t
mx nymn z mn zm n
mx tzmt y mt ym t
ny tznt x nt xn t
B x y z
b z b z x y
v x y z t
b y b y x z
b x b x y z
λ λ λ
ξ ξ λ λ
ξ ξ λ λ
ξ ξ λ λ
∞ ∞ ∞
= = =
∞ ∞
= =
∞ ∞
= =
∞ ∞
= =
+ +
=
+ +
+ +
∑∑∑
∑∑
∑∑
∑∑
jwte
(11.b)
0 0 0
1 1 2 20 0
3 1 4 20 0
5 1 6 20 0
cos cos cos
[ ( ) ( )]cos cos
( , , , )
[ ( ) ( )]cos cos
[ ( ) ( )]cos cos
mnt mx ny tzm n t
mx nymn z mn zm n
mx tzmt y mt ym t
ny tznt x nt xn t
C x y z
c z c z x y
w x y z t
c y c y x z
c x c x y z
λ λ λ
ξ ξ λ λ
ξ ξ λ λ
ξ ξ λ λ
∞ ∞ ∞
= = =
∞ ∞
= =
∞ ∞
= =
∞ ∞
= =
+ +
=
+ +
+ +
∑∑∑
∑∑
∑∑
∑∑
jwte
(11.c)
where ω denotes the natural frequency of the plate and 1j = − , /mx m aλ π= , /ny n bλ π= ,
/tz t hλ π= , and Amnt, Bmnt, Cmnt are the Fourier coefficients of three-dimensional Fourier
series expansions for the three displacement, respectively. a1mn, a2mn, a3mt, a4mt, a5nt, a6nt, b1mn,
11
b2mn, b3mt, b4mt, b5nt, b6nt, c1mn, c2mn, c3mt, c4mt, c5nt and c6nt are the supplemented coefficients of
the auxiliary functions. All of them need to be determined in future. The closed-form
auxiliary functions 1xξ , 2xξ , 1yξ , 2 yξ , 1zξ and 2zξ are respectively used to remove any
discontinuities potentially exhibited by the original displacement functions and their
derivatives at the edges x=0, x=a, y=0, y=b, z=0 and z=h. According to three-dimensional
elasticity theory, it is required that at least two-order derivatives of the three displacement
functions exist and continuous at any point on the plate. Therefore two auxiliary functions in
every direction are supplemented as demonstrated in Eqs.11(a)-(c). The closed-form auxiliary
functions are given as follow
2
2
1 2( ) ( 1) , ( ) ( 1)x xa
x x xx x x
a aζ ζ= − = − (12.a)
2
2
1 2( ) ( 1) , ( ) ( 1)y yb
y y yy y y
b bζ ζ= − = − (12.b)
2
2
1 2( ) ( 1) ( ) ( 1),z zh
z z zz z z
h hζ ζ= − = − (12.c)
It is easy to verify that
1 1
' '1 1(0) ( ) ( ) 0, (0) 1
x xx x a aζ ζ ζ ζ= = = = (13.a)
2 2
' '2 2(0) ( ) (0) 0, ( ) 1
x xx x a aζ ζ ζ ζ= = = = (13.b)
1 1
' '1 1(0) ( ) ( ) 0, (0) 1
y yy y b bζ ζ ζ ζ= = = = (13.c)
2 2
' '2 2(0) ( ) (0) 0, ( ) 1
y yy y b bζ ζ ζ ζ= = = = (13.d)
1 1
' '1 1(0) ( ) ( ) 0, (0) 1
z zz z h hζ ζ ζ ζ= = = = (13.e)
2 2
' '2 2(0) ( ) (0) 0, ( ) 1
z zz z h hζ ζ ζ ζ= = = = (13.f)
It can be proven mathematically that the series expansion given in Eq. (11) can be simply
12
differentiated, through term-by-term, to obtain uniformly convergent series expansions for up
to the second-order derivatives. It should be noted that in numerical calculations the three
series solutions have to be truncated numerically to M, N and T.
2.4 Energy functions and the solution procedure
The strain energy Π for FG rectangular plates is given in integral form by:
0 0 0
1( )
2
h b a
xx xx yy yy zz zz xy xy xz xz yz yz dxdydzσ ε σ ε σ ε σ γ σ γ σ γ+ + + + +Π = ∫ ∫ ∫ (14)
Substituting to Eq. (4), Eq. (5) and Eq. (6) into Eq. (14), the strain energy Π can be
written as follows:
2 2 2
0 0 0
2 2 2 2 2 2
1( 2 )[( ) ( ) ( ) ]
2
2 ( )
[( ) ( ) ( ) ( ) ( ) ( ) ]
2 ( )
h b au v w
Gx y z
u v u w v w
x y x z y z
u v u w v wG
y x z x z y
u v u w v wG dxdydz
y x z x z y
λ
λ
∂ ∂ ∂+ + +
∂ ∂ ∂
∂ ∂ ∂ ∂ ∂ ∂+ + +
∂ ∂ ∂ ∂ ∂ ∂
∂ ∂ ∂ ∂ ∂ ∂+ + + + + +
∂ ∂ ∂ ∂ ∂ ∂
∂ ∂ ∂ ∂ ∂ ∂+ + +
∂ ∂ ∂ ∂ ∂ ∂
Π = ∫ ∫ ∫
(15)
The potential energy P stored in the boundary springs can be expressed as:
2 2 20 0 0
0 0
2 2 20
0 0
1[( ) ( ) ( ) ]
2
1[ ) ( ) ( ) ]
2
h b
uxa vxa wxaux vx wx
h a
uyo vyo wyuyb vyb wyb
P k k u k k v k k w dydz
k k u k k v k k w dxdz
= + + + + +
+ + + + + +
∫ ∫
∫ ∫ (16)
The kinetic energy T of the FG plates is depicted as:
2 2 2
0 0 0
1[( ) ( ) ( ) ]
2
h b au v w
T dxdydzt t t
ρ∂ ∂ ∂
= + +∂ ∂ ∂∫ ∫ ∫ (17)
In order to determine the coefficients in the functions, the Rayleigh-Ritz method is
applied in present work, which is a powerful tool in the vibration analysis of structural
13
elements because of its simplicity and high accuracy. The Lagrangian energy function of the
plate can be expressed in terms of strain energy, kinetic energy and potential energy stored in
boundary edges as:
L T P= −Π− (18)
Substituting the above Eq. (11) into Eq. (18), and minimizing the Lagrangian energy
functional L with respect to the unknown coefficients
1 2 1 2 1 2 6, , , , , , , , , , )0 ( u mnt mn mn mnt mn mn mnt mn mn nt
u
A a a B b b C c c cL
αα
=∂
=∂
(19)
The problem will be transformed into a eigenvalue and eigenvector problem, and the
following governing eigenvalue equation in matrix form can be achieved
2[[ ] ] 0K M Xω− = (20)
where [ ] [ ] [ ]s pK K K= + , [ ]sK is the symmetric stiffness matrix obtained from the strain
energy, [ ]pK is the symmetric stiffness matrix obtained from the potential energy stored in
boundary edge, and [ ]M is the symmetric mass matrix obtained from the kinetic energy.
They can be written as:
[
[ ] 0 0
] 0 [ ] 0
0 0 [ ]
uu
vv
ww
M
M M
M
= (21.a)
[ ] [ ] [ ]
[ ] [ ] [ ]
[ ]
s
suu suv suw
svv svw
sww
K K K
K K K
sym K
= (21.b)
[ ] 0 0
[ ] 0 [ ] 0
0 0 [ ]
p
puu
pvv
pww
K
K K
K
=
(21.c)
The element of the stiffness matrix [ ]K and mass matrix [ ]M are given in Appendix
14
A. X is the column matrix composed of the unknown coefficients expressed in the
following form:
[ , , ]u v wX X X X Τ= (22)
where
000 100 1 200 2 300 3
5400 4 500 600 6
[ , , , , , , , , , , , , , ,
, , , , , , , , ]
umnt MNT MN MN MT
NTMT NT
X A A A a a a a a a
a a a a a a
=
000 100 1 200 2 300 3
5400 4 500 600 6
[ , , , , , , , , , , , , , ,
, , , , , , , , ]
vmnt MNT MN MN MT
NTMT NT
X B B B b b b b b b
b b b b b b
=
000 100 1 200 2 300 3
5400 4 500 600 6
[ , , , , , , , , , , , , , ,
, , , , , , , , ]
wmnt MNT MN MN MT
NTMT NT
X C C C c c c c c c
c c c c c c
=
Eq. (20) represents a standard characteristic equation. All the natural frequencies and
mode shapes can be obtained by solving Eq. (20). Each eigenvector is the set of Fourier series
coefficients for the corresponding mode. Then the displacements and force of the plate can be
obtained easily.
3. Numerical examples
In this section, numerical examples for the free vibration analysis of FG plates with
various gradient index and arbitrary boundary conditions are presented to validate the
accuracy and reliability of the present method. First, the determination of the spring stiffness
is investigated, and the convergence of the present method is checked by analyzing the FG
plates with four simply supported edges. Then, FG plates with various classical boundary
conditions and elastic boundary conditions are studied. Finally, the effects of gradient indexes
are discussed as well.
3.1 Determination of the spring stiffness
15
In this study, three sets of linear springs are used to simulate the given or typical
boundary conditions, and a clamped edge can be obtained by assigning the spring stiffness at
infinity. However, numerical computations cannot deal with infinite values, and it is
significant for the accuracy of the result to setting proper spring stiffness to clamped edge.
Therefore the determination of the spring stiffness is investigated. The effects of the spring
stiffness (ku, kv and kw) on the convergence of the first six non-dimensional frequency
parameters 2/ /c ca h Eω ρΩ = for SSSS square FG plates are shown in Table 2. The
thickness-side ratios (h/a) are take as 0.1, 0.2 and 0.5. The gradient indexes are taken to be 1.
The spring parameters vary from 5×1015
to 5×1019
. From the comparison, it shows that good
convergence of the solution is obtained by increasing the spring stiffness. The spring stiffness
185 10u v wk k k= = = × is the proper stiffness.
3.2 Convergence study
Theoretically, there are infinite terms in the modified Fourier series solution. However,
the series is numerically truncated and only finite terms are counted in actual calculations.
The convergence of the present method will be checked. The non-dimensional fundamental
frequency parameters 2/ /c ca h Eω ρΩ = of the FG plates with four simply supported edges
are presented in Table 3 for different truncation schemes. The geometry of the plates is given
as: a=b=1m, thickness-side ratios h/a= 0.1, 0.2 and 0.5, and the values of the gradient indexes
are taken to be 0, 1, 2, 4, 8 and 10. It is found that the results of this study show a monotonic
convergence trend. When the truncated numbers change from 14×14×7 to 16×16×8, the
difference of the frequency parameters does not exceed 0.3136% for the worst case, which is
16
acceptable. More accurate results may be obtained by further truncated numbers, but the
computational cost will be increased. Therefore, for the sake of both accuracy and
computational cost, the truncated number of the displacement expressions will be uniformly
selected as 14 14 7M N T× × = × × in the following numerical examples.
3.3 FG plates with classical boundary conditions
There are many possible boundary conditions at the ends of a rectangular FG plate and it
is impossible to undertake an all-encompassing survey of the vibrations for every case of
boundary condition. In this section, three types of classical boundary conditions often
encountered in practice are studied. Take edge x=0 for example, they are defined as follows:
Free boundary condition (F):
0, 0, 0xy xzxxσ σ σ= = =
Simply-supported boundary condition (S):
0, 0, 0xx v wσ = = =
Clamped boundary conditions (C):
0, 0, 0u v w= = =
The corresponding spring stiffness for the three types of classical boundaries is given in
Table 4. First, the accuracy of the present solution is demonstrated in Tables 5-7. Table 5
shows the first seven frequency parameters 2 /b h Dϖ ω ρ= for square isotropic plates with
different boundary conditions. The results are compared with other published solutions by
using the 3-D Ritz method with simple algebraic polynomials [29], the 3-D Ritz method with
general orthogonal polynomials using the Gram-Schmidt process [30], and the 3-D Ritz
17
method with general orthogonal polynomials [32]. The first five non-dimensional frequency
parameters 2/ /c ca h Eω ρΩ = of Al/Al2O3 square plates under simply-supported boundary
conditions with various thickness-side ratios and gradient indexes are presented in Table 6.
The present results are compared with those obtained by Huang et al [38] employing 3-D
elastic theory and a variational Ritz methodology. And the difference is very small, and does
not exceed 0.053% for the worst case. The non-dimensional natural frequency parameters
/m mh Eψ ω ρ= of SSSS square Al/ZrO2 plates are shown in Table 7. It is seen that the
present results are in good agreement with those obtained by higher-order theory [25] and
three-dimensional theory by employing the powers series method [33]. In general, the present
solutions agree very well with those available in the literature.
In Tables 8 and 9, the frequency parameters /m mh Eψ ω ρ= of FG plate with different
boundary conditions are illustrated. The symmetric boundary conditions, including SSSS,
SCSC and SFSF boundary conditions, and asymmetric boundary conditions, including SCSF,
SSSC and SSSF boundary conditions, are considered. It can be observed from Tables that the
values of the non-dimensional frequency parameters corresponding to different boundary
conditions have obvious difference. The frequencies of the FG plates with SSSF, SFSF and
SCSF boundary conditions is smaller, while the frequencies of the FG plate with SCSC and
SSSC boundary conditions is obviously larger. This is due to the fact that higher constraints
at the edges increase the flexural rigidity of the plate, leading to higher frequency response.
For the FG plates with h/a=0.5 and b/a=2, the frequency parameters of the plates under SSSS,
SCSC and SSSC are same. This is maybe due to that the effects of the free edges and
18
clamped edges at y=0 and y=b have little different with the increase of the thickness-side
ratios. 3-D mode shapes for SSSS, SFSF and SCSC square thick FG plate are depicted in
Figs. 2-4.
3.4 FG plates with elastic boundary conditions
The above numerical examples are presented as FG plates with classical boundary
conditions. The frequency parameters for arbitrary classical boundaries can be obtained easily
by setting the spring stiffness a proper value. What’s more the present method also can offer a
unified solution for elastic boundary conditions. In this section, five types of elastic boundary
conditions often encountered in practice are studied. There are five types of elastic boundary
conditions which are considered for the FG plates. Fist type of elastic boundary E1
is
considered to be that only x-axial displacement along the plate edge are elastically restrained
(i.e. u ≠ 0, v = w =0). Second type of elastic boundary E2 allows elastically restrained
displacement in the y axes direction (i.e. v ≠ 0, u = w =0). Only z-axial displacement are
elastically restrained, which is defined as third type of elastic boundary E3 (i.e. w ≠ 0, v = u =
0). When both x-axial displacement and y-axial displacement along the plate edge are
elastically restrained (i.e. u ≠ 0, v ≠ 0, w=0), the edge support is donated by E4. Fifth type of
elastic boundary E5 allows elastically restrained rotation in the all axes directions (i.e. u ≠ 0, v
≠ 0, v ≠ 0). The corresponding spring stiffness for five types of elastic boundaries is given as
follows:
E1: 10 181 10 , 5 10u v wk k k= × = = ×
E2: 10 181 10 , 5 10v u wk k k= × = = ×
19
E3: 10 181 10 , 5 10w u vk k k= × = = ×
E4: 10 181 10 , 5 10u v wk k k= = × = ×
E5:
101 10u v wk k k= = = ×
There are 125 different combinations of the five types of elastic boundary conditions due to
the rectangular plates have four ends. It is strenuous to analyze all conditions, and we only
consider that the four ends conditions of the FG plates are same.
The non-dimensional frequency parameters /m mh Eψ ω ρ= of the FG plates with
different elastic boundary conditions are shown in Tables 8 and 9. Five types of elastic
boundary conditions (i.e. E1 E
1 E
1 E
1, E
2 E
2 E
2 E
2, E
3 E
3 E
3 E
3, E
4 E
4 E
4 E
4 and E
5 E
5 E
5 E
5)
are studied. The thickness-side ratios are 0.1, 0.2, 0.5, and the gradient indexes are 0, 1, 2, 5.
Table 8 shows the frequency parameters of Al/Al2O3 plates and Table 9 shows the frequency
parameters of Al/ZrO2 plates. From the tables, we can see that the frequency parameters of
FG square plates with E1 E
1 E
1 E
1 and E
2 E
2 E
2 E
2 boundary conditions are similar. The two
sets of linear springs have same effects on the frequency of the FG square plates. For the FG
plates with b/a=2, the frequency parameters of FG square plates with E1 E
1 E
1 E
1 and E
2 E
2
E2 E
2 boundary conditions are also similar besides the frequency parameters of the FG plates
with h/a=0.1. This is maybe due to the effect of the thickness-side ratios on the frequency
parameters of the FG plates.
In contrast to most existing techniques, the current method can be universally
applicable to variety of boundary conditions including all the classical cases, elastic restraints.
The change of the boundary conditions is as easy as modifying material properties and
20
geometry dimensions without the need of making any change to the solution procedure. In
addition, the current solution can be readily applied to plates with more complex boundary
conditions like point supports, non-uniform elastic restraints, mix boundaries, partial supports
and their combinations.
3.5 Parametric studies
The last section, the present method is applied to investigate the free vibration of
rectangular plates with different gradient indexes. According to the Eqs. (3) and (4), the
variation of the volume fraction through the thickness is presented in Fig. 5. It can be seen
that the volume fraction Vc varies quickly near the lowest surface for p<1 and increases
quickly near the top surface for p>1. First, the variation of the fundamental natural frequency
parameter with the power law index for square Al/Al2O3 plates with h/a=0.5 is presented in
Fig. 6(a). SSSS, SCSC, SFSF, SSSF, SSSC and SSSF boundary conditions are studied. It can
be seen that the six curves show a similar behavior. The frequencies decrease as the gradient
index increases. When the gradient index is minor, the frequencies decrease quickly, while
when the gradient index gradually raises, the change of the frequencies decrease slowly. Fig.
6(b) shows the variation of the fundamental frequency parameters with the power law index
for square Al/Al2O3 plates with h/a=0.2. Figs. 6(c) and 6(d) show the variation of the
fundamental natural frequency parameter with the power law index for square Al/ZrO2 plates
when h/a=0.5 and 0.2. The frequency characteristics shown in these three Figs are similar to
those in Fig. 6(a).
21
4. Conclusions
In this paper, a unified and accurate solution method has been developed to deal with the
free vibration analysis of arbitrarily thick functionally graded plate with general boundary
based on the linear, small-strain 3D elasticity theory. Each of displacements of the plates,
regardless of boundary conditions, is expanded as a standard three-dimensional Fourier
cosine series supplemented with closed-form auxiliary functions introduced to eliminate all
the relevant discontinuities with the displacement and its derivatives at the edges.
Mathematically, such series expansions are capable of representing any functions, including
the exact displacement solutions. Rayleigh-Ritz method is applied to obtain solution by the
energy functions of the plates. One of the advantages of the current method is that it can be
applicable to a variety of boundary conditions achieved by setting the stiffness of restraining
springs without requiring any special procedures or schemes. The excellent accuracy of the
current solutions is demonstrated by numerical examples and comparison of the present
results with those available in the literature, and the effects of gradient indexes are illustrated.
New results for thick FG plates with elastic boundary conditions are presented, which may be
serve as benchmark solutions.
Appendix A. Detailed expressions for the stiffness matrix and mass matrix
The detailed expressions of the mass matrix and the first row of the stiffness matrix in
Eq. (20) are given as follows. To make the expressions simple and clear, some indexes are
pre-defined.
1 1 1( 1)( 1)( 1) ( 1)( 1) ( 1)( 1)( 1) ( 1)( 1)s t M N n M m q t M N n M m= − + + + − + + = − + + + − + +
22
1 1 1 1 1( 1)( 1)( 1) ( 1)( 1) ( 1)( 1)( 1) ( 1)( 1)s l M N n M m q l M N n M m= − + + + − + + = − + + + − + +
2 2 1 1 1( 1)( 1)( 1) ( 1)( 1) ( 1)( 1)( 1) ( 1)( 1)s l M T t M m q l M T t M m= − + + + − + + = − + + + − + +
3 3 1 1 1( 1)( 1)( 1) ( 1)( 1) ( 1)( 1)( 1) ( 1)( 1)s l N T t N n q l N T t N n= − + + + − + + = − + + + − + +
1 1 1
11,
0 0 0
( )cos cos cos cos cos cosa b h
uu s q mx ny tz m x n y t zM z x y z x y zdxdydzρ λ λ λ λ λ λ= ∫ ∫ ∫
11 1
12
, 1
0 0 0
( )( )cos cos cos cos cosuu s q l z
a b h
mx ny tz m x n yM zz x y z x y dxdydzζρ λ λ λ λ λ= ∫ ∫ ∫
2 11 1
13
,
0 0 0
( )( )cos cos cos cos cosuu s q l y z
a b h
mx ny tz m x tM yz x y z x zdxdydzζρ λ λ λ λ λ= ∫ ∫ ∫
3 1 1 1
14
,
0 0 0
( )( )cos cos cos cos cosuu s q l x y z
a b h
mx ny tz n tM xz x y z y zdxdydzζρ λ λ λ λ λ= ∫ ∫ ∫
1 1 1 1
21,
0 0 0
( ) ( )cos cos cos cos coslz
a b h
uu s q mx ny m x n y t zzM z x y x y zdxdydzζρ λ λ λ λ λ= ∫ ∫ ∫
1 1 11 1
22
,
0 0 0
( ) ( )( )cos cos cos cosuu s q lz l z
a b h
mx ny m x n yM z zz x y x y dxdydzζ ζρ λ λ λ λ= ∫ ∫ ∫
1 2 1 11
23
,
0 0 0
( ) ( ) cos( )cos cos cosuu s q lz l y t z
a b h
mx ny m xM z y zz x y x dxdydzζ ζ λρ λ λ λ= ∫ ∫ ∫
1 3 1 1 1
24
,
0 0 0
( ) ( )( )cos cos cos cosuu s q lz l x y z
a b h
mx ny n tM z xz x y y zdxdydzζ ζρ λ λ λ λ= ∫ ∫ ∫
2 1 1 1
31,
0 0 0
( ) ( )cos cos cos cos cosly
a b h
uu s q mx tz m x n y t zyM z x z x y zdxdydzζρ λ λ λ λ λ= ∫ ∫ ∫
2 1 11 1
32
,
0 0 0
( ) ( )( )cos cos cos cosuu s q ly l z
a b h
mx tz m x n yM y zz x z x y dxdydzζ ζρ λ λ λ λ= ∫ ∫ ∫
2 2 1 11
33
,
0 0 0
( ) ( )cos( )cos cos cosuu s q ly l y t z
a b h
mx tz m xM y y zz x z x dxdydzζ ζ λρ λ λ λ= ∫ ∫ ∫
23
2 3 1 1 1
34
,
0 0 0
( ) ( )( )cos cos cos cosuu s q ly l x y z
a b h
mx tz n tM y xz x z y zdxdydzζ ζρ λ λ λ λ= ∫ ∫ ∫
3 1 1 1
41,
0 0 0
( ) ( )cos cos cos cos cosa b h
uu s q ny tz m x n y t zlxM z x y z x y zdxdydzρ ζ λ λ λ λ λ= ∫ ∫ ∫
3 1 11 1
42
,
0 0 0
( )( ) ( )cos cos cos cosuu s q l z
a b h
ny tz m x n ylxM zz x y z x y dxdydzζρ ζ λ λ λ λ= ∫ ∫ ∫
3 2 1 11
43
,
0 0 0
( )cos( ) ( )cos cos cosuu s q l y t z
a b h
ny tz m xlxM y zz x y z x dxdydzζ λρ ζ λ λ λ= ∫ ∫ ∫
3 3 1 1 1
44
,
0 0 0
( )( ) ( )cos cos cos cosuu s q l x y z
a b h
ny tz n tlxM xz x y z y zdxdydzζρ ζ λ λ λ λ= ∫ ∫ ∫
uu vv wwM MM = =
1 1 1
1 1 1 1
1
1 1
1
0
0
11,
0 0 0
( 2 ) cos
( 1) )
(
[( 2 ) sin cos cos sin cos cos
sin cos cos sin cos
( cos cos cos cos
(
mx
m m
ux uxa
uy uyb
a b h
uu s q mx m x mx ny tz m x n y t z
ny n y ny tz m x n y t z
ny tz n y t z
G x
k
K G x y z x y z
y z x y z
k k y z y z
k
λ λ
λ λ λ λ λ λ λ λ λ
λ λ λ λ λ λ λ
λ λ λ λ+
+
−
+
= +
+
+ +
+
∫ ∫ ∫
1
1 11) )cos cos cos cos ]n n
mx tz m x t zx z x z dxdydzλ λ λ λ+−
1
1
1
1 1
1 1
1 1 1
12
, 1
0
0
1
0 0 0
( )
( 2 ) cos ( )
( 1) ) ( )
( 1
( cos cos cos
(
[( 2 ) sin cos cos sin cos
sin cos cos sin
uu s q l z
mx l z
m m
ux uxa l z
uy uyb
ny tz n y
a b h
mx m x mx ny tz m x n y
ny n y ny tz m x n y
K z
G x z
z
k
k k y z y
k
G x y z x y
y z x y
ζ
λ λ ζ
ζλ λ λ
λ λ λ λ λ λ λ λ
λ λ λ λ λ λ+
+ +
+ −
+ −
+
+
= +∫ ∫ ∫
1
1 1) ) cos ( )]cos cosn n
mx l ztz m xx zz x dxdydzλ ζλ λ+
2 1
1
1
1 1
1
1 1
1 1
13
,
'
0
0
1
0 0 0
( )
( 2 )( ) cos ( )
( 1) ) ( )
(0)
( cos cos cos
(
[( 2 ) sin cos cos sin cos
sin cos cos cosl y
uu s q l y z
mx z
m m
ux uxa l y
uy l y
ny tz t z
a b h
mx m x mx ny tz m x t
ny ny tz m x t
K y
G x y
yk k y z z
k
G x y z x z
y z x z
ζ
λ λ ζ
ζ
ζ
λ λ λ
λ λ λ λ λ λ λ λ
λ λ λ λ λ+
+ −
−
+
+ +
+
= +
+
∫ ∫ ∫
1 1 1cos ( ))cos cos cos cos ]
uyb l y mx tz m x t znyk b b x z x z dxdydzζ λ λ λ λλ
24
3 1
1
1 1 1 1
1 1
1 1 1
14 '
,
0
0 0 0
) ( )
( 2 ) cos ( )
(0) cos ( ))( cos cos cos cos
[( 2 )( sin cos cos cos cos
sin cos sin cos
uu s q l x y z
y mx l x y z
ux l x uxa mx l x ny tz n y t z
a b h
mx mx ny tz n t
ny n ny tz n t
K x
G x x
a ak k y z y z
G x y z y z
y z y z
ζ
λ λ ζ
ζ λ ζ λ λ λ λ
λ λ λ λ λ λ λ
λ λ λ λ λ λ+
+ +
= + −
+
∫ ∫ ∫
1
1 10 ( 1) )cos( cos cos cos ]n n
uy uyb mx tz m x t zk xk z x z dxdydzλ λ λ λ++ −+
1 1 1
1 1 1 1
1
11,
0 0 0
2 cos
[ sin cos cos cos sin cos
sin cos sin cos cos ]mx
a b h
uv s q mx n y mx ny tz m x n y t z
ny m x ny tz m x n y t zG x
K x y z x y z
y z x y z dxdydzλ
λλ λ λ λ λ λ λ λ
λ λ λ λ λ λ λ
=
+
∫ ∫ ∫
1
1
1 1
1 1 1
12
, 1 1
0 0 0
( )
2 cos ( )]
[ sin cos cos cos sin
sin cos sin cos
uv s q l z
mx l z
a b h
mx n y mx ny tz m x n y
ny m x ny tz m x n y
K z
G x z z
x y z x y
y z x y dxdydz
ζ
λ ζ
λλ λ λ λ λ λ λ
λ λ λ λ λ λ+
= ∫ ∫ ∫
2 1
1
1 1
1 1 1
13 '
,
0 0 0
) ( )
2 cos ( ) ]
[ ( sin cos cos cos cos
sin cos sin cos
l yuv s q z
mx l y z
a b h
mx mx ny tz m x t
ny m x ny tz m x t
K y
G x y
x y z x z
y z x z dxdydz
ζ
λ ζ
λ λ λ λ λ λ λ
λ λ λ λ λ λ
= −
+
∫ ∫ ∫
3 1
1
1 1
1 1
14
,
'
1
0 0 0
( )
2 ( )cos ( ) ]
[ sin cos cos sin cos
sin cos cos cos
uv s q l x y z
mx l x y z
a b h
mx n y mx ny tz n t
ny ny tz n t
K x
G x x
x y z y z
y z y z dxdydz
ζ
λ ζ
λλ λ λ λ λ λ λ
λ λ λ λ λ−
=
+
∫ ∫ ∫
1 1 1
1 1 1 1
1
11,
0 0 0
2 cos
[ sin cos cos cos cos sin
cos sin sin cos cos ]
t z
mx
a b h
uw s q mx t z mx ny tz m x n y
tz m x ny tz m x n y t zG x
K x y z x y z
y z x y z dxdydzλ
λλ λ λ λ λ λ λ λ
λ λ λ λ λ λ λ
=
+
∫ ∫ ∫
1
1
1 1
1 1 1
12 '
, 1
0 0 0
) ( )
2 cos ( )]
[ ( sin cos cos cos sin
cos sin sin cos
uw s q l z
mx l z
a b h
mx mx ny tz m x n y
tz m x ny tz m x n y
K z
G x z z
x y z x y
y z x y dxdydz
ζ
λ ζ
λ λ λ λ λ λ λ
λ λ λ λ λ λ+
= −∫ ∫ ∫
2 1
1
1 1
1 1 1
13
, 1
0 0 0
( )
2 cos ( ) ]
[ sin cos cos cos sin
cos sin sin cos
uw s q l y z
mx l y z
a b h
mx t z mx ny tz m x t
tz m x ny tz m x t
K y
G x y
x y z x z
y z x z dxdydz
ζ
λ ζ
λλ λ λ λ λ λ λ
λ λ λ λ λ λ
=
+
∫ ∫ ∫
3 1
1
1 1
1 1
14
,
'
1
0 0 0
( )
2 ( ) cos ( ) ]
[ sin cos cos cos sin
cos sin cos cos
uw s q l x y z
mx l x y z
a b h
mx t z mx ny tz n t
tz ny tz n t
K x
G x x
x y z y z
y z y z dxdydz
ζ
λ ζ
λλ λ λ λ λ λ λ
λ λ λ λ λ−
=
+
∫ ∫ ∫
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31
List of Collected Table and Figure Captions
Table 1 Material properties of the used FG plate.
Table 2 First six frequency parameters 2/ /c ca h Eω ρΩ = for SSSS square Al/Al2O3 plates
with different thickness-side ratio when p=1.
Table 3 The fundamental frequency parameters 2/ /c ca h Eω ρΩ = for simply-supported
square Al/Al2O3 plates.
Table 4 Value of spring stiffness for three types of classical boundary conditions
Table 5 The first seven frequency parameters 2 /b h Dϖ ω ρ= of square isotropic plates with
different boundary conditions.
Table 6 The non-dimensional frequency parameters 2/ /c ca h Eω ρΩ = of Al/Al2O3 square
plate with simply-supported boundary conditions.
Table 7 The non-dimensional frequency parameters /m mh Eψ ω ρ= of Al/ZrO2 square
plates with simple-supported boundary conditions (τ=h/a).
Table 8 The non-dimensional frequency parameters /m mh Eψ ω ρ= of Al/Al2O3 plates with
different classical boundary conditions.
Table 9 The non-dimensional frequency parameters /m mh Eψ ω ρ= of Al/ZrO2 plates with
different classical boundary conditions.
Table 10 The non-dimensional frequency parameters /m mh Eψ ω ρ= of Al/Al2O3 plates
with different elastic boundary conditions.
Table 11 The non-dimensional frequency parameters /m mh Eψ ω ρ= of Al/ZrO2 plates with
different elastic boundary conditions.
32
Fig. 1. Schematic diagram of the 3-D rectangular functionally graded plates: (a) the geometry
and coordinates; (b) FG plate of two material phases; (c) the boundary restraining springs.
Fig.2. Modes shapes of Al/Al2O3 plates with SSSS boundary condition when h/a=0.5 and
p=1: (a) m = 1; (b) m = 2; (c) m = 3; (d) m = 4; (e) m=5; (f) m=6.
Fig.3. Modes shapes of Al/Al2O3 plates with SFSF boundary condition when h/a=0.5 and
p=1: (a) m = 1; (b) m = 2; (c) m = 3; (d) m = 4; (e) m=5; (f) m=6.
Fig.4. Modes shapes of Al/Al2O3 plates with SCSC boundary condition when h/a=0.5 and
p=1: (a) m = 1; (b) m = 2; (c) m = 3; (d) m = 4; (e) m=5; (f) m=6.
Fig. 5. Variation of volume fraction Vc through the non-dimensions thickness of FG plates
Fig.6 Variation of the frequency parameters with the gradient index for FG square plates:(a)
Al/Al2O3 plates with h/a=0.5; (b) Al/Al2O3 plates with h/a=0.2; (c) Al/ZrO2 plates with
h/a=0.5; (d) Al/ZrO2 plates with h/a=0.2.
Table 1
Material properties of the used FG plate
Material Properties
E(GPa) μ ρ (kg/m3)
Aluminum(Al) 70 0.3 2702
Alumina(Al2O3) 380 0.3 3800
Zirconia(ZrO2) 200 0.3 5700
Table 2
First six frequency parameters 2 / /c ca h E for SSSS square Al/Al2O3 plates with
different thickness-side ratio when p=1.
h/a ku=kv
=kw
Ω1 Ω2 Ω3 Ω4 Ω5 Ω6
= kw
0.1 5×1015
4.4278 10.6305 10.6305 16.1998 16.1998 16.4065
5×1016
4.4281 10.6309 10.6309 16.2007 16.2007 16.4075
5×1017
4.4281 10.6309 10.6309 16.2008 16.2008 16.4076
5×1018
4.4281 10.6309 10.6309 16.2008 16.2008 16.4076
5×1019
4.4280 10.6309 10.6309 16.2008 16.2008 16.4076
0.2 5×1015
4.0994 8.0881 8.0881 9.1083 9.1083 11.4166
5×1016
4.0996 8.0886 8.0886 9.1085 9.1085 11.4166
5×1017
4.0996 8.0886 8.0886 9.1086 9.1086 11.4166
5×1018
4.0996 8.0886 8.0886 9.1086 9.1086 11.4166
5×1019
4.0996 8.0886 8.0886 9.1086 9.1086 11.4166
0.5 5×1015
2.9901 3.2011 3.2011 4.4672 4.4672 5.6301
5×1016
2.9902 3.2013 3.2013 4.4673 5.6303 5.6303
5×1017
2.9902 3.2013 3.2013 4.4673 5.6303 5.6303
5×1018
2.9902 3.2013 3.2013 4.4673 5.6303 5.6303
5×1019
2.9902 3.2013 3.2013 4.4673 5.6303 5.6303
Table 3
The fundamental frequency parameters 2 / /c ca h E for simply-supported square
Al/Al2O3 plates.
h/a Truncated
p=0 p=1 p=2 p=4 p=8 p=10
number
0.1 8×8×4 5.7989 4.4450 4.0325 3.8277 3.7058 3.6431
9×9×4 5.7978 4.4439 4.0314 3.8268 3.7050 3.6425
10×10×5 5.7855 4.4335 4.0212 3.8171 3.6955 3.6328
12×12×6 5.7818 4.4330 4.0179 3.8140 3.6927 3.6300
14×14×7 5.7794 4.4281 4.0158 3.8121 3.6909 3.6281
16×16×8 5.7786 4.4273 4.0151 3.8114 3.6902 3.6275
18×18×9 5.7779 4.4267 4.0145 3.8108 3.6897 3.6269
20×20×10 5.7776 4.4264 4.0142 3.8106 3.6895 3.6266
0.2 8×8×4 5.3097 4.1042 3.7013 3.4608 3.3142 3.2576
9×9×4 5.3096 4.1011 3.7011 3.4601 3.3141 3.2575
10×10×5 5.3060 4.1011 3.6982 3.4579 3.3110 3.2542
12×12×6 5.3050 4.1001 3.6972 3.4570 3.3101 3.2532
14×14×7 5.3043 4.0996 3.6967 3.4565 3.3096 3.2627
16×16×8 5.3041 4.0993 3.6964 3.4563 3.3094 3.2525
18×18×9 5.3039 4.0992 3.6963 3.4561 3.3093 3.2523
20×20×10 5.3038 4.0991 3.6962 3.4560 3.3092 3.2522
0.5 8×8×4 3.7616 2.9913 2.6672 2.3992 2.2236 2.1819
9×9×4 3.7616 2.9913 2.6672 2.3992 2.2236 2.1819
10×10×5 3.7608 2.9906 2.6665 2.3985 2.2226 2.1808
12×12×6 3.7605 2.9903 2.6662 2.3983 2.2224 2.1804
14×14×7 3.7603 2.9902 2.6661 2.3981 2.2222 2.1802
16×16×8 3.7602 2.9902 2.6660 2.3981 2.2221 2.1801
18×18×9 3.7602 2.9901 2.6660 2.3980 2.2221 2.1801
20×20×10 3.7602 2.9901 2.6660 2.3980 2.2221 2.1801
Table 4
Values of spring stiffness for three types of classical boundary conditions
Boundary Spring stiffness
condition ku kv kw
Free edge (F) 0 0 0
Simply-supported edge (S) 0
5×1018
5×1018
Clamped edge (C) 5×1018
5×1018
5×1018
Table 5
The first seven frequency parameters 2 /b h D of square isotropic plates with
different boundary conditions.
BC h/a method Modes
1 2 3 4 5 6 7
SSSS 0.1 present 19.098 45.636 45.636 64.384 64.384 70.149 85.500
Ref.[29] 19.090 45.622 45.622 64.383 64.383 70.112 85.502
Ref.[30] 19.090 45.619 45.619 64.383 64.383 70.104 85.488
0.2 present 17.528 32.192 32.192 38.488 38.488 45.526 55.802
Ref.[29] 17.528 32.192 32.192 38.502 38.502 45.526 55.843
Ref.[30] 17.526 32.192 32.192 38.483 38.483 45.526 55.787
0.5 present 12.426 12.877 12.877 18.210 23.009 23.009 25.753
Ref.[30] 12.426 12.877 12.877 18.210 23.007 23.007 25.753
CCCC 0.1 present 33.009 63.043 63.043 88.411 104.28 105.29 123.73
Ref.[29] 32.797 62.672 62.672 87.941 103.71 104.70 123.60
Ref.[30] 32.782 62.630 62.630 87.869 103.61 104.60 123.59
0.2 present 27.065 47.346 47.346 62.000 62.000 63.635 72.604
Ref.[29] 26.974 47.253 47.253 61.944 61.944 63.570 72.568
Ref.[30] 26.906 47.103 47.103 61.917 61.917 63.348 72.286
0.5 present 15.358 24.136 24.136 24.866 24.866 29.379 31.578
Ref.[30] 15.294 24.078 24.078 24.823 24.823 29.377 31.210
FFFF 0.1 present 12.728 18.956 23.346 31.965 31.965 55.493 55.493
Ref.[31] 12.726 18.955 23.347 31.965 31.965 55.493 55.493
0.2 present 11.710 17.433 21.252 27.648 27.648 40.192 42.775
Ref.[31] 11.710 17.433 21.252 27.647 27.647 40.191 42.776
0.5 present 8.7801 12.515 14.962 16.072 17.030 17.030 17.632
Ref.[31] 8.7802 12.515 14.962 16.073 17.030 17.030 17.631
Table 6
The non-dimensional frequency parameters 2 / /c ca h E of Al/Al2O3 square plate
with simply-supported boundary conditions.
h/a p method Mode
0.1 1 2 3 4 5
0 present 5.779 13.81 13.81 19.48 19.48
Ref.[38] 5.777 13.81 13.81 19.48 19.48
Diff.% 0.0346 0.0000 0.0000 0.0000 0.0000
1 present 4.428 10.63 10.63 16.20 16.20
Ref.[38] 4.426 10.63 10.63 16.20 16.20
Diff.% 0.0452 0.0000 0.0000 0.0000 0.0000
5 present 3.774 8.931 8.931 12.64 12.64
Ref.[38] 3.772 8.927 8.927 12.64 12.64
Diff.% 0.0530 0.0448 0.0448 0.000 0.000
0.2 0 present 5.304 9.742 9.742 11.65 11.65
Ref.[38] 5.304 9.742 9.742 11.65 11.65
Diff.% 0.0000 0.0000 0.0000 0.0000 0.0000
1 present 4.100 8.089 8.089 9.108 9.108
Ref.[38] 4.099 8.089 8.089 9.107 9.107
Diff.% 0.0244 0.0000 0.0000 0.0110 0.0110
5 present 3.405 6.296 6.296 7.344 7.344
Ref.[38] 3.405 6.296 6.296 7.343 7.343
Diff.% 0.0000 0.0000 0.0000 0.0136 0.0136
Table 7
The non-dimensional frequency parameters /m mh E of Al/ZrO2 square plates with
simple-supported boundary conditions (τ=h/a).
Method p=0 n=1 τ=0.2
1/ 10 τ=0.1 τ=0.05 τ=0.1 τ=0.2 n=2 n=3 n=5
Present 0.4658 0.0578 0.0159 0.0620 0.2285 0.2264 0.2271 0.2281
Ref.[25] 0.4658 0.0577 0.0158 0.0619 0.2285 0.2264 0.2270 0.2281
Ref.[33] 0.4658 0.0577 0.0153 0.0596 0.2192 0.2197 0.2211 0.2225
Table 8
The non-dimensional frequency parameters /m mh E of Al/Al2O3 plates with
different classical boundary conditions.
b/a h/a p Boundary conditions
SSSS SCSC SFSF SCSF SSSC SSSF
1 0.1 0 0.1135 0.1604 0.0562 0.0731 0.1339 0.0677
1 0.0870 0.1236 0.0430 0.0559 0.1029 0.0518
2 0.0789 0.1118 0.0390 0.0507 0.0932 0.0470
5 0.0741 0.1038 0.0368 0.0477 0.0871 0.0443
0.2 0 0.4169 0.5402 0.2141 0.2713 0.4731 0.2550
1 0.3222 0.4236 0.1645 0.2092 0.3681 0.1962
2 0.2905 0.3799 0.1488 0.1889 0.3310 0.1773
5 0.2676 0.3412 0.1388 0.1749 0.3014 0.1649
0.5 0 1.8470 1.9139 1.0652 0.9570 1.9139 0.9570
1 1.4687 1.5724 0.8342 0.7937 1.5499 0.7937
2 1.3095 1.4026 0.7464 0.7149 1.3796 0.7149
5 1.1450 1.2072 0.6687 0.6168 1.1961 0.6168
2 0.1 0 0.0719 0.0793 0.0568 0.0607 0.0751 0.0600
1 0.0550 0.0608 0.0435 0.0465 0.0575 0.0459
2 0.0499 0.0552 0.0395 0.0422 0.0522 0.0417
5 0.0471 0.0519 0.0372 0.0398 0.0492 0.0393
0.2 0 0.2713 0.2941 0.2166 0.1914 0.2814 0.1914
1 0.2088 0.2271 0.1665 0.1592 0.2169 0.1592
2 0.1888 0.2050 0.1507 0.1438 0.1960 0.1438
5 0.1754 0.1895 0.1405 0.1243 0.1817 0.1243
0.5 0 0.9570 0.9570 0.9570 0.4785 0.9570 0.4785
1 0.7937 0.7937 0.7937 0.3978 0.7937 0.3978
2 0.7149 0.7149 0.7149 0.3591 0.7149 0.3591
5 0.6168 0.6168 0.6168 0.3101 0.6168 0.3101
Table 9
The non-dimensional frequency parameters /m mh E of Al/ZrO2 plates with different
classical boundary conditions.
b/a h/a p Boundary conditions
SSSS SCSC SFSF SCSF SSSC SSSF
1 0.1 0 0.0673 0.0950 0.0333 0.0432 0.0793 0.0401
1 0.0620 0.0878 0.0306 0.0398 0.0732 0.0369
2 0.0617 0.0872 0.0306 0.0397 0.0728 0.0368
5 0.0629 0.0882 0.0312 0.0405 0.0740 0.0376
0.2 0 0.2469 0.3200 0.1268 0.1607 0.2803 0.1510
1 0.2285 0.2981 0.1170 0.1486 0.2602 0.1395
2 0.2264 0.2934 0.1164 0.1475 0.2570 0.1386
5 0.2281 0.2916 0.1180 0.1489 0.2572 0.1403
0.5 0 1.0941 1.1337 0.6310 0.5669 1.1337 0.5669
1 1.0258 1.0842 0.5882 0.5424 1.0789 0.5424
2 1.0013 1.0577 0.5779 0.5294 1.0507 0.5294
5 0.9804 1.0227 0.5730 0.5119 1.0227 0.5119
2 0.1 0 0.0426 0.0470 0.0337 0.0360 0.0445 0.0356
1 0.0392 0.0433 0.0310 0.0331 0.0410 0.0327
2 0.0391 0.0432 0.0309 0.0330 0.0408 0.0327
5 0.0399 0.0440 0.0316 0.0337 0.0417 0.0333
0.2 0 0.1607 0.1742 0.1283 0.1134 0.1667 0.1134
1 0.1484 0.1611 0.1184 0.1085 0.1540 0.1085
2 0.1474 0.1598 0.1178 0.1059 0.1529 0.1059
5 0.1492 0.1613 0.1194 0.1024 0.1546 0.1024
0.5 0 0.5669 0.5669 0.5669 0.2834 0.5669 0.2834
1 0.5424 0.5424 0.5424 0.2712 0.5424 0.2712
2 0.5294 0.5294 0.5294 0.2647 0.5294 0.2647
5 0.5119 0.5119 0.5119 0.2560 0.5119 0.2560
Table 10
The non-dimensional frequency parameters /m mh E of Al/Al2O3 plates with
different elastic boundary conditions.
b/a h/a p Boundary conditions
E1E
1E
1E
1 E
2E
2E
2E
2 E
3E
3E
3E
3 E
4E
4E
4E
4 E
5E
5E
5E
5
1 0.1 0 0.0635 0.0635 0.0615 0.0633 0.0536
1 0.0684 0.0684 0.0644 0.0681 0.0511
2 0.0703 0.0703 0.0649 0.0699 0.0496
5 0.0722 0.0722 0.0655 0.0717 0.0489
0.2 0 0.1270 0.1270 0.1257 0.1267 0.1209
1 0.1369 0.1369 0.1343 0.1363 0.1247
2 0.1405 0.1405 0.1371 0.1398 0.1250
5 0.1444 0.1444 0.1397 0.1433 0.1257
0.5 0 0.3175 0.3175 0.3163 0.3167 0.3141
1 0.3421 0.3421 0.3399 0.3405 0.3353
2 0.3511 0.3511 0.3482 0.3491 0.3421
5 0.3606 0.3606 0.3560 0.3578 0.3485
2 0.1 0 0.0549 0.0549 0.0515 0.0544 0.0410
1 0.0592 0.0592 0.0524 0.0544 0.0382
2 0.0556 0.0607 0.0522 0.0495 0.0368
5 0.0532 0.0623 0.0519 0.0497 0.0361
0.2 0 0.1099 0.1098 0.1075 0.1089 0.0974
1 0.1183 0.1183 0.1136 0.1167 0.0978
2 0.1214 0.1214 0.1153 0.1193 0.0973
5 0.1246 0.1245 0.1166 0.1219 0.0972
0.5 0 0.2746 0.2746 0.2728 0.2723 0.2668
1 0.2957 0.2956 0.2922 0.2916 0.2806
2 0.3033 0.3031 0.2985 0.2982 0.2844
5 0.3112 0.3109 0.3041 0.3044 0.2879
Table 11
The non-dimensional frequency parameters /m mh E of Al/ZrO2 plates with different
elastic boundary conditions.
b/a h/a p Boundary conditions
E1E
1E
1E
1 E
2E
2E
2E
2 E
3E
3E
3E
3 E
4E
4E
4E
4 E
5E
5E
5E
5
1 0.1 0 0.0517 0.0517 0.0487 0.0514 0.0390
1 0.0600 0.0600 0.0546 0.0595 0.0406
2 0.0637 0.0637 0.0572 0.0599 0.0418
5 0.0683 0.0683 0.0605 0.0609 0.0436
0.2 0 0.1033 0.1033 0.1014 0.1028 0.0944
1 0.1199 0.1199 0.1164 0.1191 0.1046
2 0.1275 0.1275 0.1231 0.1264 0.1094
5 0.1366 0.1366 0.1312 0.1353 0.1156
0.5 0 0.2584 0.2584 0.2566 0.2571 0.2532
1 0.2996 0.2996 0.2966 0.2975 0.2906
2 0.3184 0.3184 0.3145 0.3158 0.3073
5 0.3414 0.3414 0.3360 0.3380 0.3275
2 0.1 0 0.0446 0.0446 0.0397 0.0420 0.0292
1 0.0436 0.0517 0.0433 0.0389 0.0300
2 0.0435 0.0550 0.0450 0.0388 0.0307
5 0.0444 0.0589 0.0473 0.0396 0.0319
0.2 0 0.0893 0.0893 0.0858 0.0880 0.0742
1 0.1035 0.1035 0.0973 0.1014 0.0809
2 0.1099 0.1099 0.1024 0.1074 0.0843
5 0.1178 0.1177 0.1086 0.1147 0.0887
0.5 0 0.2232 0.2232 0.2204 0.2199 0.2121
1 0.2587 0.2586 0.2538 0.2534 0.2402
2 0.2747 0.2746 0.2686 0.2685 0.2529
5 0.2943 0.2941 0.2862 0.2866 0.2686
(a)
(b)
(c)
Fig. 1. Schematic diagram of the rectangular 3-D functionally graded plates: (a) the geometry
and coordinates; (b) FG plate of two material phases; (c) the boundary restraining springs.
(a) (b)
(c) (d)
(e) (f)
Fig.2. Modes shapes of Al/Al2O3 plates with SSSS boundary condition when h/a=0.5 and
p=1: (a) m = 1; (b) m = 2; (c) m = 3; (d) m = 4; (e) m=5; (f) m=6.
(a) (b)
(c) (d)
(e) (f)
Fig.3. Modes shapes of Al/Al2O3 plates with SFSF boundary condition when h/a=0.5 and
p=1: (a) m = 1; (b) m = 2; (c) m = 3; (d) m = 4; (e) m=5; (f) m=6.
(a) (b)
(c) (d)
(d)
Fig.4. Modes shapes of Al/Al2O3 plates with SCSC boundary condition when h/a=0.5 and
p=1: (a) m = 1; (b) m = 2; (c) m = 3; (d) m = 4; (e) m=5; (f) m=6.
Fig. 5. Variation of volume fraction Vc through the non-dimensions thickness of FG plates
0 0.2 0.4 0.6 0.8 10
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
1
p=10
p=5
p=3
p=1
p=0.5
p=0.3
p=0.1
Vc
z/h
(a) (b)
(c) (d)
Fig. 6. Variation of the frequency parameters with the gradient index for FG square plates:(a)
Al/Al2O3 plates with h/a=0.5; (b) Al/Al2O3 plates with h/a=0.2; (c) Al/ZrO2 plates with
h/a=0.5; (d) Al/ZrO2 plates with h/a=0.2.
0 2 4 6 8 100
0.2
0.4
0.6
0.8
1
1.2
1.4
1.6
1.8
2
The gradient index
Th
e fre
qu
en
cy p
ara
me
ter
SCSC
SSSC
SSSS
SCSF
SSSF
SFSF
0 2 4 6 8 100
0.1
0.2
0.3
0.4
0.5
The gradient index
Th
e fre
qu
en
cy p
ara
me
ter
SCSC
SSSC
SSSS
SCSF
SSSF
SFSF
0 2 4 6 8 100
0.2
0.4
0.6
0.8
1
The gradient index
Th
e fre
qu
en
cy p
ara
me
ter
SCSC
SSSC
SSSS
SCSF
SSSF
SFSF
0 2 4 6 8 100
0.05
0.1
0.15
0.2
0.25
0.3
0.35
0.4
0.45
0.5
The gradient index
Th
e fre
qu
en
cy p
ara
me
ter
SCSC
SSSC
SSSS
SCSF
SSSF
SFSF