# Modeling of Axially Loaded Nanowires Embedded in Elastic Substrate Media with Inclusion of Nonlocal and Surface Effects

Authors: Suchart Limkatanyu; Nattapong Damrongwiriyanupap; Woraphot Prachasaree; Worathep Sae-Long
Journal: Journal of Nanomaterials
 (2013)

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## Abstract

Nonlocal and surface effects are incorporated into a bar-elastic substrate element to account for small-scale and size-dependent effects on axial responses of nanowires embedded in elastic substrate media. The virtual displacement principle, employed to consistently derive the governing differential equation as well as the boundary conditions, forms the core of the displacement-based finite element formulation of the nanowire-elastic substrate element. The element displacement shape functions, analytically derived based on homogeneous solution to the governing differential equilibrium equation of the problem, result in the exact element stiffness matrix and equivalent load vector. Two numerical simulations employing the proposed model are performed to study characteristics and behavior of the nanowire-substrate system. The first simulation involves investigation of responses of the wire embedded in elastic substrate. The second examines influences of several system parameters on the contact stiffness and reveals the size-dependent effect on the effective Young's modulus of the system.


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## Body

## 1. Introduction

From early 1990s, science and technology advancement has shifted into the era of nanotechnology, thanks to the discovery of carbon nanotubes by Iijima [1] at NEC Laboratory, Tsukuba, Japan. Many researchers have since then turned their attention to this emerging technology.Nanostructure has attracted many scientists and engineers due to its superior physical properties and its vast area of novel applications [2]. To broaden its potential and to further understand its mechanical behaviors, experimental and/or theoretical studies at nanoscale are required.Experimental tests on nanostructures are extremely difficult to be conducted and are oftentimes prohibitively expensive. Numerical simulations have thus been widely used instead in the research community to characterize its mechanical properties and material responses. Generally in nanostructure modeling, there are two categories of numerical simulation approaches: atomistic approach and continuum-mechanics approach.The atomistic approach, as its name stipulates, focuses on atomic modeling and embraces several techniques, such as classical molecular dynamics [3], tight binding molecular dynamics [4], and density functional theory [5]. Simulation performed using the atomistic approach provides comprehensive details but is still hampered by high computational costs; hence only systems with small numbers of molecule and atom can be practically investigated using this approach [6].The alternative continuum-mechanics approach serves as another tool option to characterize the nanostructural response and is applicable to large-scale nanostructural system modeling. However, small-scale effect and size-dependent effect inherent to all nanosized structures have yet to be considered and incorporated into the classical continuum-mechanics theory.Small-scale effect is caused by long-range interatomic interactions while size-dependent effect is a result of energy correspondent to the atoms at the free surface of the nanosized structure. To account for these two effects, two nonclassical elasticity theories, nonlocal elasticity theory and surface elasticity theory, have later been incorporated into the classical continuum-mechanics theory.The nonlocal elasticity theory was initiated by Eringen [7–9] and Eringen and Edelen [10] and has been widely used to study bending, buckling, vibration, and wave propagation of nanostructure [11–18]. The essence of this theory is in its assertion that the stress at a reference point depends on the strain not only at a particular point but also at all other points throughout the elastic body. Interatomic forces and atomic length scale are considered in the material constitutive relation as nonlocal model parameters.The surface elasticity theory was first proposed by Gurtin and Murdoch [19, 20] and has been employed to represent the size-dependent effect caused by the surface stress and the surface elasticity at nanoscale. With the size of a structure approaching a nanoscale regime, the surface free energy caused by the surface stress and surface elasticity could no longer be neglected in comparison with the bulk energy as that in the classical continuum-mechanics theory due to the high surface-to-volume ratio.Several researchers have incorporated these two surface effects into the classical continuum-mechanics theory to study bending, buckling, vibration, and wave propagation of nanostructure, as afore mentioned [15, 17, 21–24].Nanowires have become popular with their superior mechanical, electrical, and thermal performance and have drawn considerable interests in nanoscience and nanoengineering. They have been found to fit a wide range of applications covering micro-/nanoelectromechanical systems (M/NEMS), biosensors, optoelectronics, and biotechnology [25–27]. Numerical studies done to date have mainly focused on bending of nanowires. For example, He and Lilley [22] incorporated Gurtin-Murdoch surface model into Euler-Bernoulli beam model to study surface effect on the bending behavior of nanowires; Jiang and Yan [28] enhanced the nanowire model of He and Lilley [22] using Timoshenko beam theory to account for the shear deformation; Liu et al. [24] combined the elastica theory with the Gurtin-Murdoch surface model to perform large-displacement analyses of nanowires including the surface effect; Juntarasaid et al. [15] subsequently improved the nonlinear nanowire model of Liu et al. [24] by including the nonlocal effect.In nanodevices, nanowires are usually integrated into larger structures through substrate media. Therefore, the interaction mechanism between the nanowire and the surrounding substrate media plays an important role in controlling the performance and characterizing the response of those nanodevices. Several researchers have recently investigated the problem of nanowires resting on elastic substrate media. For example, Zhang and Zhao [29] developed a nanowire model lying on an adhesive receding contact foundation; Khajeansari et al. [30] performed parametric studies of silver nanowires resting on Winkler-Pasternak elastic substrate media using an analytical solution to the problem; Malekzadeh and Shojaee [17] investigated surface and nonlocal effects on nonlinear free vibration of nanowires supported by an elastic medium using both Euler-Bernoulli beam theory and Timoshenko beam theory.In this research, an axially loaded nanowire embedded in an elastic substrate medium is of main interest. Although several numerical models have been developed to perform buckling analyses of nanowire-elastic substrate systems under compression [31–33], to the best knowledge of the authors, no studies under tension have yet to be found. Thus, such a numerical model in this paper is presented for the first time with the idea stemming from axially loaded pile problems [34].In the study, brief introductions to nonlocal elasticity theory and surface elasticity theory are firstly presented. The two theories are then employed to explain small-scale and size-dependent effects on the response of a nanowire embedded in an elastic substrate medium. The governing differential equilibrium and compatibility equations and constitutive relations of the problem are then presented. Subsequently the Navier-Cauchy governing equation and associated end-boundary force conditions are derived based on the virtual displacement principle and solved analytically to obtain the exact displacement interpolation functions. This notion stems from the Winkler-based beam model developed by Limkatanyu et al. [35]. Formulation of the nanowire-substrate element is also based on the virtual displacement principle.Two numerical simulations employing the proposed model are finally performed to study the characteristics and behaviors of the nanowire-substrate system; the first involves investigation of responses of the embedded nanowire and the second examines the influences of several system parameters on contact stiffness and shows the size-dependent effect on the effective Young’s modulus of the system.


## 2. Small-Scale and Size-Dependent Effects on Nanowires

Small-scale and size-dependent effects on the response of a nanowire embedded in an elastic substrate medium are incorporated into the proposed model through the following two nonclassical elasticity theories: (i) nonlocal elasticity theory and (ii) surface elasticity theory. Brief descriptions of these two nonclassical elasticity theories are as follows.


### 2.1. Nonlocal Elasticity Theory

In opposition to classical elasticity theory, nonlocality in the nonlocal elasticity theory implies that the stress field at a generic pointx in an elastic body is not only a function of the strain at a particular point but also a function of strains at other points throughout the body [10]. This nonlocal attribute of the nonlocal elasticity theory conforms well to the atomic theory of lattice dynamics as well as some experimental evidence on phonon dispersion [11].The nonlocal stress tensorσNL at a point x in a nonlocal elastic continuum can be represented as a weighted integral of strain contributions of all material points throughout the body:
(1)σNL=∫VK(|x′-x|,τ)σL(x′)dV(x′),
where K(|x′-x|,τ) is the elastic spatial kernel function and represents the nonlocal modulus; |x′-x| is the Euclidean distance between material points x and x′; the local classical stress tensor σL(x′) is the double-dot contraction between the fourth-order elastic tensor C(x′) and the strain tensor ε(x′); and the dimensionless material constant τ, as defined, is
(2)τ=e0aL,
where e0 is a calibrated material constant in obtaining a good correlation between the model results and analytical or experimental results; a and L represent, respectively, the internal and the external characteristic length. In this work, L represents the length of the nanowire.The integral form of the nonlocal constitutive relation of (1) makes the solution to the problem difficult. Eringen [8] thus presented the elastic spatial kernel function K(|x′-x|,τ) in the form of a modified Bessel function and subsequently converted the integral constitutive relation into an equivalent differential constitutive relation; thus
(3)σNL-(e0a)2∇2σNL=σL=C:ε,
where ∇2=∂2/∂x2+∂2/∂y2+∂2/∂z2 is the Laplace differential operator.Since only the normal stress in thex direction is of interest in this work, (3) can be simplified into a one-dimensional form as
(4)σxxNL-(e0a)2d2σxxNLdx2=Exxεxx,
where σxxNL and εxx are, respectively, the nonlocal normal stress and normal strain in the x direction and Exx is the Young’s modulus.


### 2.2. Surface Elasticity Theory

To account for surface effect on the nanowire response, the Gurtin-Murdoch continuum model [19] is employed. In this nonclassical continuum model, the nanowire cross-section is considered to be consisted of a solid core and an outer surface shell perfectly bonded to its core, as shown in Figure 1. Following the surface theory proposed by Cammarata [36], the outer surface is considered a mathematically zero thickness layer with a distinct elastic modulus from its core material. Since only normal stress in the x direction is of interest in this work, the residual surface stress σxxs and surface strain εxxs along the longitudinal direction are related through the degenerated form of the Shuttleworth’s equation [37] as
(5)σxxs=σxxs0+Exxsεxxs,
where Exxs is the surface elastic modulus and is usually obtained by atomistic simulations or experimental results and σxxs0 is the residual surface stress and is defined in terms of the surface energy density Ψ  as
(6)σxxs0=Ψ+∂Ψ∂εxxs|εxxs=0.(a) A nanowire with residual surface stress; (b) a circular cross section with a surface layer; (c) a rectangular cross section with a surface layer.
(a)
(b)
(c)


## 2.1. Nonlocal Elasticity Theory

In opposition to classical elasticity theory, nonlocality in the nonlocal elasticity theory implies that the stress field at a generic pointx in an elastic body is not only a function of the strain at a particular point but also a function of strains at other points throughout the body [10]. This nonlocal attribute of the nonlocal elasticity theory conforms well to the atomic theory of lattice dynamics as well as some experimental evidence on phonon dispersion [11].The nonlocal stress tensorσNL at a point x in a nonlocal elastic continuum can be represented as a weighted integral of strain contributions of all material points throughout the body:
(1)σNL=∫VK(|x′-x|,τ)σL(x′)dV(x′),
where K(|x′-x|,τ) is the elastic spatial kernel function and represents the nonlocal modulus; |x′-x| is the Euclidean distance between material points x and x′; the local classical stress tensor σL(x′) is the double-dot contraction between the fourth-order elastic tensor C(x′) and the strain tensor ε(x′); and the dimensionless material constant τ, as defined, is
(2)τ=e0aL,
where e0 is a calibrated material constant in obtaining a good correlation between the model results and analytical or experimental results; a and L represent, respectively, the internal and the external characteristic length. In this work, L represents the length of the nanowire.The integral form of the nonlocal constitutive relation of (1) makes the solution to the problem difficult. Eringen [8] thus presented the elastic spatial kernel function K(|x′-x|,τ) in the form of a modified Bessel function and subsequently converted the integral constitutive relation into an equivalent differential constitutive relation; thus
(3)σNL-(e0a)2∇2σNL=σL=C:ε,
where ∇2=∂2/∂x2+∂2/∂y2+∂2/∂z2 is the Laplace differential operator.Since only the normal stress in thex direction is of interest in this work, (3) can be simplified into a one-dimensional form as
(4)σxxNL-(e0a)2d2σxxNLdx2=Exxεxx,
where σxxNL and εxx are, respectively, the nonlocal normal stress and normal strain in the x direction and Exx is the Young’s modulus.


## 2.2. Surface Elasticity Theory

To account for surface effect on the nanowire response, the Gurtin-Murdoch continuum model [19] is employed. In this nonclassical continuum model, the nanowire cross-section is considered to be consisted of a solid core and an outer surface shell perfectly bonded to its core, as shown in Figure 1. Following the surface theory proposed by Cammarata [36], the outer surface is considered a mathematically zero thickness layer with a distinct elastic modulus from its core material. Since only normal stress in the x direction is of interest in this work, the residual surface stress σxxs and surface strain εxxs along the longitudinal direction are related through the degenerated form of the Shuttleworth’s equation [37] as
(5)σxxs=σxxs0+Exxsεxxs,
where Exxs is the surface elastic modulus and is usually obtained by atomistic simulations or experimental results and σxxs0 is the residual surface stress and is defined in terms of the surface energy density Ψ  as
(6)σxxs0=Ψ+∂Ψ∂εxxs|εxxs=0.(a) A nanowire with residual surface stress; (b) a circular cross section with a surface layer; (c) a rectangular cross section with a surface layer.
(a)
(b)
(c)


## 3. Governing Equations of Nanowires Embedded in Elastic Substrate Medium

### 3.1. Differential Equilibrium Equation: Direct Approach

Figure2(a) shows a nanowire-elastic substrate system.  This system comprises a bar representing a nanowire plus smeared tangential springs to account for the substrate interactive forces. In a direct manner, the governing differential equilibrium equation of the system can be derived as follows.(a) An axially loaded nanowire-elastic substrate system; (b) a differential segment of an axially loaded nanowire-elastic substrate system.
(a)
(b)A differential segmentdx taken from the nanowire-elastic substrate system is as shown in Figure 2(b). The axial equilibrium of the infinitesimal bar segment dx is written as
(7)dN(x)dx+px(x)-Ds(x)=0,
where N(x) is the bar-section force px(x) the longitudinal distributed load and Ds(x) the substrate interactive force.It is noteworthy to remark that this system is internally statically indeterminate and internal forces cannot be determined solely by an equilibrium condition since at any system section there are 2 internal force unknown fields,N(x) and Ds(x), while only one equilibrium equation is available.


### 3.2. Compatibility Equations

The bar-section strainεxx(x) and substrate deformation Δs(x) define the system sectional deformations, and are, respectively, the conjugate-work pairs of the bar-section force N(x) and substrate interactive force Ds(x). These two system sectional deformations are related to the bar axial displacement ux(x) through the following compatibility equations:
(8)εxx(x)=dux(x)dx,Δs(x)=ux(x).The bar compatibility condition follows the small strain assumption [38] while the substrate compatibility condition obeys the Winkler-foundation hypothesis [39].


### 3.3. Sectional Force-Deformation Relations

Imposing the bar-section equilibrium and constitutive relations of (4) and (5) and enforcing the bar section kinematics, the bar-section force N(x) can be expressed in terms of the bar-section strain εxx(x) as
(9)N(x)-(e0a)2d2N(x)dx2=(EA)*εxx(x)+σxxs0Γ,
where (EA)*=AExx+ΓExxs is the effective bar axial stiffness and accounts for the contributions from the solid core and the outer surface; A is the bar sectional area; and Γ is the bar perimeter.For cross-sections that are circular (Figure1(b)) and rectangular (Figure 1(c)), the effective bar axial stiffness (EA)* is
(10)(EA)*=Exxπ4D2+ExxsπD:circular=ExxBH+2Exxs(B+H):rectangular,
where D is the diameter in the circular cross section and B and H are, respectively, the width and the height in the rectangular section.The substrate interactive forceDs(x) is related to the substrate deformation Δs(x) as
(11)Ds(x)=ksΔs(x),
where ks is the elastic substrate stiffness, and is computed as the product of the substrate-stiffness coefficient Ks and bar perimeter Γ.The equilibrium, compatibility, and constitutive equations for the nanowire embedded in an elastic substrate medium presented above can be conveniently represented in the classical Tonti’s diagram of Figure3.Figure 3
Tonti’s diagram for nanowire embedded in elastic substrate medium: governing differential equations.


### 3.4. The Virtual Displacement Principle: Differential Equilibrium Equation and Natural Boundary Conditions

Virtual displacement equation is an integral expression of the system equilibrium and can be expressed in the general form as(12)δW=δWint+δWext=0,
where δW is the system total virtual work; δWint is the system internal virtual work; and δWext is the system external virtual work.In the case of a nanowire embedded in an elastic substrate medium,δWint and δWext can be expressed as
(13)δWint=∫LN(x)δεxx(x)dx+∫LDs(x)δΔs(x)dx,δWext=-∫Lpx(x)δux(x)dx-δUTP,
where px(x) is the applied distributed load; the vector U={U1U2}T contains displacements at the bar ends; and the vector P={P1P2}T contains the conjugate-work forces acting at the bar ends.Imposing the equilibrium condition of (7), compatibility condition of (8), and constitutive relation of (9) and (11), (12) can be rewritten as
(14)δW=∫L((EA)*+ks(e0a)2)dux(x)dxdδux(x)dxdx-∫L(e0a)2dpx(x)dxdδux(x)dxdx+∫Lσxxs0Γdδux(x)dxdx+∫Lksux(x)δux(x)dx-∫Lpx(x)δux(x)dx-δUTP=0.In order to move all differential operators to the axial displacementux(x), integration by parts is applied once to the first three terms of (14), resulting in the following expression:
(15)∫Lδux(x)[((EA)*+ks(e0a)2)d2ux(x)dx2000000000-ksux(x)+px(x)-(e0a)2d2px(x)dx2]dx+[δux(x)(((EA)*+ks(e0a)2)dux(x)dx0000000000000-(e0a)2dpx(x)dx+σxxs0Γdux(x)dx)]0L-δUTP=0.Following the Cartesian sign convention, (15) can be written as
(16)∫Lδux(x)[d2px(x)dx2((EA)*+ks(e0a)2)d2ux(x)dx2000000000-ksux(x)+px(x)-(e0a)2d2px(x)dx2]dx-δU1(P1-(((EA)*+ks(e0a)2)dux(x)dx00000000000000-(e0a)2dpx(x)dx+σxxs0Γ)x=0)-δU2(P2-(((EA)*+ks(e0a)2)dux(x)dx0000000000000-(e0a)2dpx(x)dx+σxxs0Γ)x=L)=0.Due to the arbitrariness ofδux(x), the governing differential equilibrium equation of the system described in terms of the axial displacement ux(x) is obtained:
(17)((EA)*+ks(e0a)2)d2ux(x)dx2-ksux(x)=(e0a)2d2px(x)dx2-px(x),forx∈(0,L).Equation (17) is also known as the Navier-Cauchy equation and is used to obtain the analytically derived displacement shape functions. It is noteworthy to mention that for the solution to (17), both nonlocal and surface effects affect the homogeneous part while only nonlocal effect modifies the particular part. When both nonlocal and surface effects are neglected, (17) becomes the governing differential equilibrium equation for a local bar embedded in an elastic medium widely used in the study of axially loaded pile problems.The natural boundary conditions are obtained by accounting for the arbitrariness ofδU in (16) as
(18)P1=(((EA)*+ks(e0a)2)dux(x)dx0000-(e0a)2dpx(x)dx+σxxs0Γdux(x)dx)x=0,P2=(((EA)*+ks(e0a)2)dux(x)dx0000-(e0a)2dpx(x)dx+σxxs0Γ)x=L.Unlike in classical problem of bar-foundation system, (18) indicates that the nonlocal parameter (e0a) renders the substrate medium stiffness ks as well as the applied distributed load px(x), presented in the natural boundary conditions. The residual surface stress σxxs0 also modifies the end-force boundaries.


## 3.1. Differential Equilibrium Equation: Direct Approach

Figure2(a) shows a nanowire-elastic substrate system.  This system comprises a bar representing a nanowire plus smeared tangential springs to account for the substrate interactive forces. In a direct manner, the governing differential equilibrium equation of the system can be derived as follows.(a) An axially loaded nanowire-elastic substrate system; (b) a differential segment of an axially loaded nanowire-elastic substrate system.
(a)
(b)A differential segmentdx taken from the nanowire-elastic substrate system is as shown in Figure 2(b). The axial equilibrium of the infinitesimal bar segment dx is written as
(7)dN(x)dx+px(x)-Ds(x)=0,
where N(x) is the bar-section force px(x) the longitudinal distributed load and Ds(x) the substrate interactive force.It is noteworthy to remark that this system is internally statically indeterminate and internal forces cannot be determined solely by an equilibrium condition since at any system section there are 2 internal force unknown fields,N(x) and Ds(x), while only one equilibrium equation is available.


## 3.2. Compatibility Equations

The bar-section strainεxx(x) and substrate deformation Δs(x) define the system sectional deformations, and are, respectively, the conjugate-work pairs of the bar-section force N(x) and substrate interactive force Ds(x). These two system sectional deformations are related to the bar axial displacement ux(x) through the following compatibility equations:
(8)εxx(x)=dux(x)dx,Δs(x)=ux(x).The bar compatibility condition follows the small strain assumption [38] while the substrate compatibility condition obeys the Winkler-foundation hypothesis [39].


## 3.3. Sectional Force-Deformation Relations

Imposing the bar-section equilibrium and constitutive relations of (4) and (5) and enforcing the bar section kinematics, the bar-section force N(x) can be expressed in terms of the bar-section strain εxx(x) as
(9)N(x)-(e0a)2d2N(x)dx2=(EA)*εxx(x)+σxxs0Γ,
where (EA)*=AExx+ΓExxs is the effective bar axial stiffness and accounts for the contributions from the solid core and the outer surface; A is the bar sectional area; and Γ is the bar perimeter.For cross-sections that are circular (Figure1(b)) and rectangular (Figure 1(c)), the effective bar axial stiffness (EA)* is
(10)(EA)*=Exxπ4D2+ExxsπD:circular=ExxBH+2Exxs(B+H):rectangular,
where D is the diameter in the circular cross section and B and H are, respectively, the width and the height in the rectangular section.The substrate interactive forceDs(x) is related to the substrate deformation Δs(x) as
(11)Ds(x)=ksΔs(x),
where ks is the elastic substrate stiffness, and is computed as the product of the substrate-stiffness coefficient Ks and bar perimeter Γ.The equilibrium, compatibility, and constitutive equations for the nanowire embedded in an elastic substrate medium presented above can be conveniently represented in the classical Tonti’s diagram of Figure3.Figure 3
Tonti’s diagram for nanowire embedded in elastic substrate medium: governing differential equations.


## 3.4. The Virtual Displacement Principle: Differential Equilibrium Equation and Natural Boundary Conditions

Virtual displacement equation is an integral expression of the system equilibrium and can be expressed in the general form as(12)δW=δWint+δWext=0,
where δW is the system total virtual work; δWint is the system internal virtual work; and δWext is the system external virtual work.In the case of a nanowire embedded in an elastic substrate medium,δWint and δWext can be expressed as
(13)δWint=∫LN(x)δεxx(x)dx+∫LDs(x)δΔs(x)dx,δWext=-∫Lpx(x)δux(x)dx-δUTP,
where px(x) is the applied distributed load; the vector U={U1U2}T contains displacements at the bar ends; and the vector P={P1P2}T contains the conjugate-work forces acting at the bar ends.Imposing the equilibrium condition of (7), compatibility condition of (8), and constitutive relation of (9) and (11), (12) can be rewritten as
(14)δW=∫L((EA)*+ks(e0a)2)dux(x)dxdδux(x)dxdx-∫L(e0a)2dpx(x)dxdδux(x)dxdx+∫Lσxxs0Γdδux(x)dxdx+∫Lksux(x)δux(x)dx-∫Lpx(x)δux(x)dx-δUTP=0.In order to move all differential operators to the axial displacementux(x), integration by parts is applied once to the first three terms of (14), resulting in the following expression:
(15)∫Lδux(x)[((EA)*+ks(e0a)2)d2ux(x)dx2000000000-ksux(x)+px(x)-(e0a)2d2px(x)dx2]dx+[δux(x)(((EA)*+ks(e0a)2)dux(x)dx0000000000000-(e0a)2dpx(x)dx+σxxs0Γdux(x)dx)]0L-δUTP=0.Following the Cartesian sign convention, (15) can be written as
(16)∫Lδux(x)[d2px(x)dx2((EA)*+ks(e0a)2)d2ux(x)dx2000000000-ksux(x)+px(x)-(e0a)2d2px(x)dx2]dx-δU1(P1-(((EA)*+ks(e0a)2)dux(x)dx00000000000000-(e0a)2dpx(x)dx+σxxs0Γ)x=0)-δU2(P2-(((EA)*+ks(e0a)2)dux(x)dx0000000000000-(e0a)2dpx(x)dx+σxxs0Γ)x=L)=0.Due to the arbitrariness ofδux(x), the governing differential equilibrium equation of the system described in terms of the axial displacement ux(x) is obtained:
(17)((EA)*+ks(e0a)2)d2ux(x)dx2-ksux(x)=(e0a)2d2px(x)dx2-px(x),forx∈(0,L).Equation (17) is also known as the Navier-Cauchy equation and is used to obtain the analytically derived displacement shape functions. It is noteworthy to mention that for the solution to (17), both nonlocal and surface effects affect the homogeneous part while only nonlocal effect modifies the particular part. When both nonlocal and surface effects are neglected, (17) becomes the governing differential equilibrium equation for a local bar embedded in an elastic medium widely used in the study of axially loaded pile problems.The natural boundary conditions are obtained by accounting for the arbitrariness ofδU in (16) as
(18)P1=(((EA)*+ks(e0a)2)dux(x)dx0000-(e0a)2dpx(x)dx+σxxs0Γdux(x)dx)x=0,P2=(((EA)*+ks(e0a)2)dux(x)dx0000-(e0a)2dpx(x)dx+σxxs0Γ)x=L.Unlike in classical problem of bar-foundation system, (18) indicates that the nonlocal parameter (e0a) renders the substrate medium stiffness ks as well as the applied distributed load px(x), presented in the natural boundary conditions. The residual surface stress σxxs0 also modifies the end-force boundaries.


## 4. Finite Element Formulation of Nanowires Embedded in Elastic Substrate Media

### 4.1. Displacement-Based Formulation

Configuration of the displacement-based nanowire element embedded in elastic substrate medium is shown in Figure4. In this type of finite element formulation, the axial displacement ux(x) serves as a primary variable and is related to the element nodal displacements U through the displacement shape function matrix NB(x):
(19)ux(x)=NB(x)U.Figure 4
Nanowire-substrate element.The displacement shape functions inNB(x) are obtained by solving analytically the governing differential equilibrium equation of (17), as will be discussed in the subsequent section. The bar and elastic substrate compatibility conditions are both enforced in the strong sense. The bar-section strain εxx(x) and substrate deformation Δs(x) are related to the element nodal displacements U through the following equations:
(20)εxx(x)=dNB(x)dxU=BB(x)U,Δs(x)=NB(x)U=Bs(x)U,
where BB(x) and Bs(x) are, respectively, the bar and substrate deformation-displacement matrices.An alternative way to express the system equilibrium equation is that the virtual displacement principle forms the core of the formulation in the displacement-based model. Applying the virtual displacement principle of (12), substituting the compatibility conditions of (20), imposing the constitutive relation of (9) and (11), and subsequently imposing the arbitrariness of the virtual nodal displacements δU result in the following element stiffness equation:
(21)(KBB+Kss)U=P+Ppx+PNL-Ps0,
where KBB=∫L((EA)*+ks(e0a)2)BBTBBdx is the bar element stiffness matrix, Kss=∫LksBsTBsdx is the substrate element stiffness matrix, Ppx=∫LNBTpxdx is the equivalent load vector due to the distributed load px(x), PNL=∫L(e0a)2(dpx(x)/dx)BBTdx is the equivalent load vector due to the nonlocal effect, and Ps0=∫Lσxxs0ΓBBTdx is the equivalent load vector due to the residual surface stress σxxs0.Analytical expressions of these element matrices and equivalent load vectors are given in AppendicesA and B, respectively.


### 4.2. “Exact” Displacement Shape Functions

In this study, the analytical solution to the governing differential equation of (17) is central to obtain the exact displacement shape functions, resulting in the exact element stiffness matrix and equivalent load vector. The homogeneous solution of (17) for px(x)=0 is given [40] as
(22)ux(x)=γ1c1+γ2c2,
where c1 and c2 are generalized coordinates to be determined from the geometric boundary conditions and γ1 and γ2 are exponential functions, having
(23)γ1=e-λx,γ2=eλx,
where λ=ks/((EA)*+ks(e0a)2).In matrix form, (22) can be written as
(24)ux(x)=ΓTC,
where Γ and C are column vectors containing γ1 and γ2 and c1 and c2, respectively.The two geometric boundary conditions are related to element nodal displacements as(25)ux|x=0=U1,ux|x=L=U2.
Substituting ux(x) from (24) into (25) yields the following algebraic relation:
(26)U=ΤC,
where T is the mapping matrix between the generalized coordinates and the element nodal displacements. Symbolically solving (26) and subsequently substituting back into (24), we have
(27)ux(x)=ΓTT-1U=NB(x)U,
where NB(x)=⌊NB1(x)NB2(x)⌋ is an array containing the exact displacement shape functions. The expression of each displacement shape function is given in Appendix C.All symbolic calculations throughout this paper are performed using the computer software Mathematica [41].


## 4.1. Displacement-Based Formulation

Configuration of the displacement-based nanowire element embedded in elastic substrate medium is shown in Figure4. In this type of finite element formulation, the axial displacement ux(x) serves as a primary variable and is related to the element nodal displacements U through the displacement shape function matrix NB(x):
(19)ux(x)=NB(x)U.Figure 4
Nanowire-substrate element.The displacement shape functions inNB(x) are obtained by solving analytically the governing differential equilibrium equation of (17), as will be discussed in the subsequent section. The bar and elastic substrate compatibility conditions are both enforced in the strong sense. The bar-section strain εxx(x) and substrate deformation Δs(x) are related to the element nodal displacements U through the following equations:
(20)εxx(x)=dNB(x)dxU=BB(x)U,Δs(x)=NB(x)U=Bs(x)U,
where BB(x) and Bs(x) are, respectively, the bar and substrate deformation-displacement matrices.An alternative way to express the system equilibrium equation is that the virtual displacement principle forms the core of the formulation in the displacement-based model. Applying the virtual displacement principle of (12), substituting the compatibility conditions of (20), imposing the constitutive relation of (9) and (11), and subsequently imposing the arbitrariness of the virtual nodal displacements δU result in the following element stiffness equation:
(21)(KBB+Kss)U=P+Ppx+PNL-Ps0,
where KBB=∫L((EA)*+ks(e0a)2)BBTBBdx is the bar element stiffness matrix, Kss=∫LksBsTBsdx is the substrate element stiffness matrix, Ppx=∫LNBTpxdx is the equivalent load vector due to the distributed load px(x), PNL=∫L(e0a)2(dpx(x)/dx)BBTdx is the equivalent load vector due to the nonlocal effect, and Ps0=∫Lσxxs0ΓBBTdx is the equivalent load vector due to the residual surface stress σxxs0.Analytical expressions of these element matrices and equivalent load vectors are given in AppendicesA and B, respectively.


## 4.2. “Exact” Displacement Shape Functions

In this study, the analytical solution to the governing differential equation of (17) is central to obtain the exact displacement shape functions, resulting in the exact element stiffness matrix and equivalent load vector. The homogeneous solution of (17) for px(x)=0 is given [40] as
(22)ux(x)=γ1c1+γ2c2,
where c1 and c2 are generalized coordinates to be determined from the geometric boundary conditions and γ1 and γ2 are exponential functions, having
(23)γ1=e-λx,γ2=eλx,
where λ=ks/((EA)*+ks(e0a)2).In matrix form, (22) can be written as
(24)ux(x)=ΓTC,
where Γ and C are column vectors containing γ1 and γ2 and c1 and c2, respectively.The two geometric boundary conditions are related to element nodal displacements as(25)ux|x=0=U1,ux|x=L=U2.
Substituting ux(x) from (24) into (25) yields the following algebraic relation:
(26)U=ΤC,
where T is the mapping matrix between the generalized coordinates and the element nodal displacements. Symbolically solving (26) and subsequently substituting back into (24), we have
(27)ux(x)=ΓTT-1U=NB(x)U,
where NB(x)=⌊NB1(x)NB2(x)⌋ is an array containing the exact displacement shape functions. The expression of each displacement shape function is given in Appendix C.All symbolic calculations throughout this paper are performed using the computer software Mathematica [41].


## 5. Results and Discussions

Two numerical simulations employing the proposed model are performed to study the characteristics and behaviors of a nanowire-substrate system. The first simulation involves investigation of the response of the nanowire embedded in an elastic substrate. The second simulation examines the influences of several system parameters on contact stiffness and shows the size-dependent effect on the effective Young’s modulus of the system.


### 5.1. Simulation I: Response of a Nanowire Embedded in an Elastic Substrate

A circular silver nanowire embedded in a substrate medium is subjected to a tensile forceP of 2400 nN at its right end as shown in Figure 5. Geometric properties of the silver nanowire follow those used by Juntarasaid et al. [15] and are taken as L=1000 nm and D=50 nm. Material and surface properties of the silver nanowire come from those used by He and Lilley [22]. The bulk modulus Exx of the silver nanowire is 76 GPa while its residual surface stress σxxs0 and elastic surface modulus Exxs are 0.89 and 1.22 nN/nm, respectively. These surface properties correspond to the crystallographic direction of [001] as reported by Shenoy [42]. The nonlocal scale parameter, taken as (e0a)=200 nm, corresponds to the one used by Juntarasaid et al. [15] and Yang and Lim [16]. For the substrate medium, a stiffness coefficient Ks of 95×10-3 nN/nm3 is assumed, resulting in an elastic substrate stiffness ks of 14.92 nN/nm2. These values for the substrate are meant to represent the polymer as the surrounding substrate medium [43]. Four analytical cases are performed in this example. In the first two cases, surface effect on the nonlocal nanowire-substrate responses is investigated while in the two remaining cases, surface effect on the local nanowire-substrate responses is studied.Figure 5
Schematic and values used in numerical simulation I.Figure6 compares axial-displacement distributions along the nanowire obtained from the four cases. It can be observed that for these particular values of model parameters, influences of the nonlocal effect are more pronounced than those of the surface effect. The system becomes drastically softer when the nonlocality is neglected. It is interesting to point out that the elastic substrate stiffness is nullified with the disappearance of the nonlocal scale parameter as shown in (17), thus partially resulting in a weaker nanowire-substrate system. A larger portion of the nanowire is mobilized when the nonlocal effect is included. The axial-displacement distribution obtained from the nonlocal model with surface effect can hardly be distinguished from that obtained from the nonlocal model without surface effect. However, the surface effect is slightly magnified when the nonlocal effect is excluded. The most distinctive feature of the surface effect on the axial-displacement response is the nonzero slope of the axial-displacement distribution curve at the free end. This nonzero slope is induced by the residual surface stress and will be discussed later.Figure 6
Nanowire axial displacement versus distance along the wire.Figures7(a) and 7(b) show the nanowire axial-strain and axial-force distributions obtained from the four analysis cases. Similar to the observation on Figure 6, the influences of the nonlocal effect are more noticeable than those of the surface effect. It is interesting to observe that in Figure 7(a), the nonzero axial strain is noticed at the free end when the surface effect is included. This nonzero axial strain corresponds to the nonzero slope of the axial-displacement distribution at the free end and is caused by the nonzero residual surface stress. In Figure 7(b), the axial-force distribution obtained with the nonlocal model tends to be spreading out along the larger portion of the nanowire than that obtained with the local model. Unlike the axial-displacement and axial-strain distributions, the surface effect on the axial-force distribution is clearly observed, particularly for the nonlocal model.Nanowire axial strain (a) and nanowire axial force (b) versus distance along the wire.
(a)
(b)Figure8 shows the substrate interactive-force diagrams obtained from the four cases. As expected, the shapes of the substrate interactive-force distributions resemble those of the axial-displacement distributions following the Winkler-foundation model. Similar to the observation made earlier, the nonlocality plays a crucial role in dictating the substrate interactive-force diagram for these particular values of model parameters. The essence of the surface effect can be slightly observed when the nonlocal effect is excludedFigure 8
Substrate interactive force versus distance along the wire.


### 5.2. Simulation II: Parametric Studies of Nanowire-Substrate Systems

Parametric studies of the nanowire-substrate system in Figure5 are performed to illustrate the size-dependent effect on the effective Young’s modulus of the system and to investigate sensitivity of the model parameters on contact stiffness. As earlier described in Section 5.1., the residual surface stress σxxs0 and elastic surface modulus Exxs are 0.89 and 1.22 nN/nm, respectively. Model parameters investigated herein include the nanowire diameter, the nonlocal parameter, and the substrate stiffness. The slenderness ratio L/D is used to define the nanowire-diameter parameter and varies from 10 to 120. Therefore, the corresponding nanowire diameter varies from 100 to 8.3 nm. The nonlocal parameter (e0a) ranges from zero to 100 nm. The following nondimensional parameter K-s varying from 1 to 10 is used to define the substrate-stiffness parameter:
(28)K-s=KsΓL2ExxA.The size-dependent effect on the effective Young’s modulus of the system is now under investigation. Employing a similar approach used by He and Lilley [22] and Jiang and Yan [28], the effective Young’s modulus EBeff is obtained in the following manner The end displacement uend of the nanowire-substrate system is first computed using the proposed model, and then EBeff is obtained by solving the following nonlinear equation:
(29)uend=Pcoth(ks/(EBeffA)L)ksEBeffA,
where the right-hand side of (29) is the end displacement obtained from the proposed model without the nonlocal and surface effects.Figure9 shows variation of the effective Young’s modulus EBeff with the diameter D and nonlocal scale parameter (e0a) for nanowires embedded in substrate media with different substrate-stiffness parameters K-s. In general, effective Young’s modulus increases with decreasing nanowire diameter and increasing nonlocal scale parameter, especially for higher value of substrate-stiffness parameters. Thus, nonlocality and nanowire-substrate interactions are deemed essential to characterize the size-dependent effect on the effective Young’s modulus of the system. It is also observed that variation of the effective Young’s modulus EBeff with diameter D is not dependent on the substrate-stiffness parameter K-s when nonlocality is neglected. This is due to the nullification of the substrate stiffness induced by the disappearance of the nonlocal scale parameter as indicated in (17).Variation of effective young’s modulus with nanowire diameter and nonlocal scale parameter for various elastic substrate stiffness.
(a)
(b)
(c)
(d)Sensitivity analysis of model parameters on the contact stiffness is performed to measure essence of the nonlocal and surface effects on the system response. Following the definition by Jiang and Yan [28] and Khajeansari et al. [30], the contact stiffness of an axially loaded nanowire-substrate system is simply defined as
(30)Kend=Penduend,
where Pend and uend are the imposed force and induced displacement at an end point, respectively.In this study, two types of normalized contact stiffness are defined and used to assess the essence of the nonlocal and surface effects on the system contact stiffness. The first normalized contact stiffness is used to represent the attribution of the nonlocal effect and is defined as(31)K-non=KnsendKsend,
where Knsend is the contact stiffness accounting for both the nonlocal and surface effect; and Ksend is the contact stiffness accounting for only the surface effect. The second normalized contact stiffness is employed to represent the ascription of the surface effect and is defined as:
(32)K-sur=KnsendKnend,
where Ksend is the contact stiffness accounting for only the nonlocal effect.Figure10 shows influences of the nanowire diameter D and nonlocal scale parameter (e0a) on the normalized nonlocal contact stiffness K-non for nanowires embedded in substrate media with different substrate-stiffness parameter K-s. As anticipated, the normalized nonlocal contact stiffness K-non  is invariant with the nanowire diameter Dwhen the nonlocal effect is neglected ((e0a)=0 nm). With a larger value of nonlocal scale parameter (e0a), the nanowire diameter D shows a more significant effect on the normalized nonlocal contact stiffness K-non, especially for higher values of substrate-stiffness parameters. With increasing slenderness ratio (L/D), the nonlocal effect becomes more pronounced, especially for higher values of substrate-stiffness parameter K-s and nonlocal scale parameter (e0a).Variation of normalized stiffnessK-non with L/D for various elastic substrate stiffness and nonlocal scale parameter.
(a)
(b)
(c)
(d)Figure11 shows influences of the nanowire diameter D and the nonlocal scale parameter (e0a) on the normalized surface contact stiffness K-sur for nanowires embedded in substrate media with different substrate-stiffness parameter K-s. It is interesting to observe that the normalized surface contact stiffness K-sur is independent of K-s when nonlocality is not considered ((e0a)=0nm).  This becomes clear with the consideration of (17) where the elastic substrate stiffness ks is nullified with the disappearance of the nonlocal scale parameter (e0a). With increasing slenderness ratio (L/D), the surface effect becomes more pronounced, especially for the lower values of substrate-stiffness parameter K-s and nonlocal scale parameter (e0a). This observation is in opposition to the one drawn from Figure 10.Variation of normalized stiffnessK-sur with L/D for various elastic substrate stiffness and nonlocal scale parameter.
(a)
(b)
(c)
(d)Based on the observations made from Figures10 and 11, it can be concluded that nonlocal effect is relatively more influential than surface effect for the range of model parameters investigated herein.


## 5.1. Simulation I: Response of a Nanowire Embedded in an Elastic Substrate

A circular silver nanowire embedded in a substrate medium is subjected to a tensile forceP of 2400 nN at its right end as shown in Figure 5. Geometric properties of the silver nanowire follow those used by Juntarasaid et al. [15] and are taken as L=1000 nm and D=50 nm. Material and surface properties of the silver nanowire come from those used by He and Lilley [22]. The bulk modulus Exx of the silver nanowire is 76 GPa while its residual surface stress σxxs0 and elastic surface modulus Exxs are 0.89 and 1.22 nN/nm, respectively. These surface properties correspond to the crystallographic direction of [001] as reported by Shenoy [42]. The nonlocal scale parameter, taken as (e0a)=200 nm, corresponds to the one used by Juntarasaid et al. [15] and Yang and Lim [16]. For the substrate medium, a stiffness coefficient Ks of 95×10-3 nN/nm3 is assumed, resulting in an elastic substrate stiffness ks of 14.92 nN/nm2. These values for the substrate are meant to represent the polymer as the surrounding substrate medium [43]. Four analytical cases are performed in this example. In the first two cases, surface effect on the nonlocal nanowire-substrate responses is investigated while in the two remaining cases, surface effect on the local nanowire-substrate responses is studied.Figure 5
Schematic and values used in numerical simulation I.Figure6 compares axial-displacement distributions along the nanowire obtained from the four cases. It can be observed that for these particular values of model parameters, influences of the nonlocal effect are more pronounced than those of the surface effect. The system becomes drastically softer when the nonlocality is neglected. It is interesting to point out that the elastic substrate stiffness is nullified with the disappearance of the nonlocal scale parameter as shown in (17), thus partially resulting in a weaker nanowire-substrate system. A larger portion of the nanowire is mobilized when the nonlocal effect is included. The axial-displacement distribution obtained from the nonlocal model with surface effect can hardly be distinguished from that obtained from the nonlocal model without surface effect. However, the surface effect is slightly magnified when the nonlocal effect is excluded. The most distinctive feature of the surface effect on the axial-displacement response is the nonzero slope of the axial-displacement distribution curve at the free end. This nonzero slope is induced by the residual surface stress and will be discussed later.Figure 6
Nanowire axial displacement versus distance along the wire.Figures7(a) and 7(b) show the nanowire axial-strain and axial-force distributions obtained from the four analysis cases. Similar to the observation on Figure 6, the influences of the nonlocal effect are more noticeable than those of the surface effect. It is interesting to observe that in Figure 7(a), the nonzero axial strain is noticed at the free end when the surface effect is included. This nonzero axial strain corresponds to the nonzero slope of the axial-displacement distribution at the free end and is caused by the nonzero residual surface stress. In Figure 7(b), the axial-force distribution obtained with the nonlocal model tends to be spreading out along the larger portion of the nanowire than that obtained with the local model. Unlike the axial-displacement and axial-strain distributions, the surface effect on the axial-force distribution is clearly observed, particularly for the nonlocal model.Nanowire axial strain (a) and nanowire axial force (b) versus distance along the wire.
(a)
(b)Figure8 shows the substrate interactive-force diagrams obtained from the four cases. As expected, the shapes of the substrate interactive-force distributions resemble those of the axial-displacement distributions following the Winkler-foundation model. Similar to the observation made earlier, the nonlocality plays a crucial role in dictating the substrate interactive-force diagram for these particular values of model parameters. The essence of the surface effect can be slightly observed when the nonlocal effect is excludedFigure 8
Substrate interactive force versus distance along the wire.


## 5.2. Simulation II: Parametric Studies of Nanowire-Substrate Systems

Parametric studies of the nanowire-substrate system in Figure5 are performed to illustrate the size-dependent effect on the effective Young’s modulus of the system and to investigate sensitivity of the model parameters on contact stiffness. As earlier described in Section 5.1., the residual surface stress σxxs0 and elastic surface modulus Exxs are 0.89 and 1.22 nN/nm, respectively. Model parameters investigated herein include the nanowire diameter, the nonlocal parameter, and the substrate stiffness. The slenderness ratio L/D is used to define the nanowire-diameter parameter and varies from 10 to 120. Therefore, the corresponding nanowire diameter varies from 100 to 8.3 nm. The nonlocal parameter (e0a) ranges from zero to 100 nm. The following nondimensional parameter K-s varying from 1 to 10 is used to define the substrate-stiffness parameter:
(28)K-s=KsΓL2ExxA.The size-dependent effect on the effective Young’s modulus of the system is now under investigation. Employing a similar approach used by He and Lilley [22] and Jiang and Yan [28], the effective Young’s modulus EBeff is obtained in the following manner The end displacement uend of the nanowire-substrate system is first computed using the proposed model, and then EBeff is obtained by solving the following nonlinear equation:
(29)uend=Pcoth(ks/(EBeffA)L)ksEBeffA,
where the right-hand side of (29) is the end displacement obtained from the proposed model without the nonlocal and surface effects.Figure9 shows variation of the effective Young’s modulus EBeff with the diameter D and nonlocal scale parameter (e0a) for nanowires embedded in substrate media with different substrate-stiffness parameters K-s. In general, effective Young’s modulus increases with decreasing nanowire diameter and increasing nonlocal scale parameter, especially for higher value of substrate-stiffness parameters. Thus, nonlocality and nanowire-substrate interactions are deemed essential to characterize the size-dependent effect on the effective Young’s modulus of the system. It is also observed that variation of the effective Young’s modulus EBeff with diameter D is not dependent on the substrate-stiffness parameter K-s when nonlocality is neglected. This is due to the nullification of the substrate stiffness induced by the disappearance of the nonlocal scale parameter as indicated in (17).Variation of effective young’s modulus with nanowire diameter and nonlocal scale parameter for various elastic substrate stiffness.
(a)
(b)
(c)
(d)Sensitivity analysis of model parameters on the contact stiffness is performed to measure essence of the nonlocal and surface effects on the system response. Following the definition by Jiang and Yan [28] and Khajeansari et al. [30], the contact stiffness of an axially loaded nanowire-substrate system is simply defined as
(30)Kend=Penduend,
where Pend and uend are the imposed force and induced displacement at an end point, respectively.In this study, two types of normalized contact stiffness are defined and used to assess the essence of the nonlocal and surface effects on the system contact stiffness. The first normalized contact stiffness is used to represent the attribution of the nonlocal effect and is defined as(31)K-non=KnsendKsend,
where Knsend is the contact stiffness accounting for both the nonlocal and surface effect; and Ksend is the contact stiffness accounting for only the surface effect. The second normalized contact stiffness is employed to represent the ascription of the surface effect and is defined as:
(32)K-sur=KnsendKnend,
where Ksend is the contact stiffness accounting for only the nonlocal effect.Figure10 shows influences of the nanowire diameter D and nonlocal scale parameter (e0a) on the normalized nonlocal contact stiffness K-non for nanowires embedded in substrate media with different substrate-stiffness parameter K-s. As anticipated, the normalized nonlocal contact stiffness K-non  is invariant with the nanowire diameter Dwhen the nonlocal effect is neglected ((e0a)=0 nm). With a larger value of nonlocal scale parameter (e0a), the nanowire diameter D shows a more significant effect on the normalized nonlocal contact stiffness K-non, especially for higher values of substrate-stiffness parameters. With increasing slenderness ratio (L/D), the nonlocal effect becomes more pronounced, especially for higher values of substrate-stiffness parameter K-s and nonlocal scale parameter (e0a).Variation of normalized stiffnessK-non with L/D for various elastic substrate stiffness and nonlocal scale parameter.
(a)
(b)
(c)
(d)Figure11 shows influences of the nanowire diameter D and the nonlocal scale parameter (e0a) on the normalized surface contact stiffness K-sur for nanowires embedded in substrate media with different substrate-stiffness parameter K-s. It is interesting to observe that the normalized surface contact stiffness K-sur is independent of K-s when nonlocality is not considered ((e0a)=0nm).  This becomes clear with the consideration of (17) where the elastic substrate stiffness ks is nullified with the disappearance of the nonlocal scale parameter (e0a). With increasing slenderness ratio (L/D), the surface effect becomes more pronounced, especially for the lower values of substrate-stiffness parameter K-s and nonlocal scale parameter (e0a). This observation is in opposition to the one drawn from Figure 10.Variation of normalized stiffnessK-sur with L/D for various elastic substrate stiffness and nonlocal scale parameter.
(a)
(b)
(c)
(d)Based on the observations made from Figures10 and 11, it can be concluded that nonlocal effect is relatively more influential than surface effect for the range of model parameters investigated herein.


## 6. Summary and Conclusions

In this paper, the “exact” element stiffness matrix and the equivalent load vector for an axially loaded nanowire-substrate system including both nonlocal and surface effects are presented. The exact element stiffness matrix is derived based on the matrix virtual displacement principle using the “exact” displacement shape functions. The exact displacement shape functions are obtained by solving analytically the governing differential equilibrium equation of the problem. Two numerical simulations are performed to study characteristics and behaviors of the nanowire-substrate system.The first simulation indicates that both nonlocal and surface effects lead to a stiffer nanowire-substrate system in the same way as increasing the nanowire axial rigidity and affect the distributions of local responses along the nanowire.The second simulation points out that both nonlocal scale parameter and surrounding substrate stiffness magnify the size-dependent effect on the effective Young’s modulus of the system. Furthermore, the parametric studies performed in this second numerical simulation show that nonlocal effect is relatively more influential than surface effect for the range of model parameters investigated herein and that the influence of elastic substrate stiffness is nullified with the disappearance of the nonlocal scale parameter.One next step in this research direction is to include nonlinearities into both the nanowire and the substrate medium. It is hoped that the nanowire-substrate medium element developed herein will be useful to scientists and engineers working in the area of nanoscience and nanoengineering.



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*Source: 635428-2013-09-08.xml*