# An Exact Analytical Solution to Exponentially Tapered Piezoelectric Energy Harvester

Authors: H. Salmani; G. H. Rahimi; S. A. Hosseini Kordkheili
Journal: Shock and Vibration
 (2015)

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## Abstract

It has been proven that tapering the piezoelectric beam through its length optimizes the power extracted from vibration based energy harvesting. This phenomenon has been investigated by some researchers using semianalytical, finite element and experimental methods. In this paper, an exact analytical solution is presented to calculate the power generated from vibration of exponentially tapered unimorph and bimorph with series and parallel connections. The mass normalized mode shapes of the exponentially tapered piezoelectric beam with tip mass are implemented to transfer the proposed electromechanical coupled equations into modal coordinates. The steady states harmonic solution results are verified both numerically and experimentally. Results show that there exist values for tapering parameter and electric resistance in a way that the output power per mass of the energy harvester will be maximized. Moreover it is concluded that the electric resistance must be higher than a specified value for gaining more power by tapering the beam.


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## Body

## 1. Introduction

The dream of making sensor network nodes to monitor mechanical systems’ behavior is being achieved by applying low power, light weight, and self-sustained wireless sensors, which are capable of gaining required energy from environment. Converting light, thermal, and mechanical energies into electrical energy has been the most common methods to supply sensors’ power. Electromagnetic, electrostatic, and piezoelectric transducers are three usual conversion methods of mechanical energy into electrical energy [1]. Electromagnetic convertors have been widely used in order to generate electricity out of mechanical energy since the early 1930s [2]. During the last decade, implementing piezoelectric materials in energy harvesting devices has been extensively investigated by researchers, because of their light weight, direct implementation, and wide range of frequencies applications. Piezoelectric energy harvester is usually constructed of piezoelectric layers attached to a substrate, and its fundamental frequency is adjusted by employing tuning mass, while it is mounted on a vibrating system.As the highest performance of the piezoelectric energy harvesters occurs at their fundamental frequencies, at the early stage of the development of these devices, an equivalent single degree of freedom (SDOF) model is employed to estimate generated power [3, 4]. Later on, Erturk and Inman [5] improved SDOF model by adding separately treated strain rate and air damping terms and introducing a correction factor for varying tip mass to beam mass ratio. Although SDOF model gives a simple expression to study the energy harvester’s behavior, it lacks several important aspects of the device such as dynamic mode shapes and accurate strain distribution. These lacks have been managed through introducing a correction factor for an improved lumped parameter model by Wang and Lu [6]. Knowing that SDOF model is a simple method to assess the harvester at a limited frequency range around the fundamental frequency of the beam, Sodano et al. [7] proposed a Rayleigh-Ritz method to calculate the power harvested from piezoelectric material including damping effect in higher modes. Erturk and Inman [8, 9] also employed eigenfunction expansion method using mass normalized mode shapes of unimorph and bimorph beams with tip mass to solve the coupled electromechanical formulation of energy harvesting devices.The need for more efficient devices has encouraged researchers to present electrical and mechanical solutions in order to increase the power generation of piezoelectric vibration based energy harvesters. The most common approach used to increase the performance of energy harvesters is their geometry modification, which creates uniform strain distribution through the beam’s length. In this situation the electric charge is distributed uniformly and average power is higher than varying charge piezoelectric layer [10]. Baker et al. [11] observed that a triangular beam can harvest 50% more energy than the rectangular one, while the local overstrain occurrence is vanished by uniform strain distribution. Accepting the effects of uniform strain distribution on the harvested energy from the beam, researchers have started to examine the effects of different parameters on the harvester’s performance either numerically [12–18] or analytically [19–23]. Although numerical methods are valuable for easy implementation as well as doing parameters study, such as geometry [13–17] and tip mass [12, 18], they are time consuming and do not lead to an exact solution for the problem. On the other hand, deriving analytical solution is an intricate or almost impossible task if the governing differential equation does not belong to those familiar ones with closed form solution.Due to the existence of exact solution for eigenmodes of a uniform beam problem, a closed form expression can be obtained to present the harvester’s behavior [8, 9]. However, solving trapezoidal beams dictates taking into account assumed modes as space dependent variables. Goldschmidtboeing and Woias [19] used rectangular beam eigenmodes to form mass, stiffness, coupling, and capacitance matrices of a triangular beam which were derived by Rayleigh-Ritz method. Dietl and Garcia [20] also applied admissible mode shapes of slender prismatic beam with tip mass to study the performance of a rectangular, linear taper and reverse taper energy harvester. Rosa and de Marqui Jr. [21] implemented Rayleigh-Ritz method and Euler-Bernoulli assumptions to investigate the behavior of linear and reverse tapered energy harvesters. The Differential Quadrature Method (DQM) is another way that was used to extract mode shapes of a beam with variable width in order to form the reduced order model of electromechanical equations [23]. In addition to tapering with just varying width, the piezoelectric energy harvesters can be also modified by changing the beam thickness [22].According to this literature survey the approximated mode shapes have been employed to solve the nonuniform cross section piezoelectric energy harvesters’ governing equations. In this paper, exact normalized mode shapes of exponential beam with tip mass [24] are utilized to convert the governing electromechanical equations into modal space to calculate the power generated from piezoelectric energy harvesters. The strain rate and air damping terms are also considered to define the damping effect more accurately. After verifying the proposed formulations numerically and experimentally, parametric study is performed on beam’s length, tapering parameter, and electric resistance to investigate their effects on the energy harvesting device’s performance. In this study, we have considered unimorph and bimorph with series connection as well as bimorph with parallel connection for all the cases.


## 2. Analytical Solution

### 2.1. Electromechanical Formulation

Piezoelectric energy harvester, as shown in Figure1, is composed of a beam embedded by piezoelectric layers and is excited at its base. It is assumed that the piezoelectric layer is perfectly bonded to the substrate layer, while the integrated beam’s width is varying exponentially through the length by bx=b0e-cx, where c is tapering parameter. A proof mass is also attached on the tapered beam’s tip to regulate the fundamental frequency.Figure 1
Piezoelectric energy harvester.Because of the low thickness of the beam, the Euler-Bernoulli assumptions are employed to develop the displacement field. The governing Equation of Motion (EoM) of a beam embedded by piezoelectric layer using Euler-Bernoulli assumptions is given as [8](1)∂2Mx,t∂x2+∂2∂x2CsIx∂3wx,t∂x2∂t+Ca∂wx,t∂t+mx∂2wx,t∂t2=-mx+Mtδx-L∂2wbx,t∂t2in which Cs and Ca are equivalent strain rate and viscous air damping coefficients, respectively. w is the beam transverse deflection and wb is the base excitation displacement along z direction, while m(x) and Mt are mass per unit length and tip point mass, respectively. Area moment of inertia of the beam’s cross section changes exponentially; that is, Ix=I0e-cx, in which I0 is the moment of inertia of the beam at x=0. The internal moment of the beam M(x,t) is calculated by integrating the stress moment through the thickness as follows: (2)Mx,t=-∫tsσsbxzdz-∫tpσpbxzdz.In (2) σs and σp are defined as the normal stress in x direction at substrate and piezoelectric layers, respectively. Using the constitutive equation of isotropic and piezoelectric material, the normal stresses are formulated as(3)σs=Esε1sx,tσp=Epε1px,t-d31E3t,where Es and Ep are the modulus of elasticity of substrate and piezoelectric materials, respectively. Mechanical strain ε1(x,t)=-z∂2w(x,t)/∂x2 is calculated by applying the Euler-Bernoulli assumption. Piezoelectric electromechanical coupling is mathematically modeled by d31, and E3t=-v(t)/hp is the electric field through the z direction, where v(t) is the generated piezoelectric voltage. Substituting (3) into (2) gives the internal bending moment as(4)Mx,t=EIx∂2wx,t∂x2+ϑxvt,where EIx is the flexural rigidity of the composite beam and is calculated as(5)EIx=bxEshs312+2Ep3hs2+hp3-hs38for a two-layered piezoelectric beam, and(6)EIx=bxEshb3-ha3+Ephc3-hb33for one-layered piezoelectric energy harvester. Geometrical parameters of (5) and (6) are shown in Figure 2.Figure 2
Piezoelectric beam cross section: (a) one-layered piezoelectric beam and (b) two-layered piezoelectric beam.
(a)
(b)In (6) ha, hb, and hc are defined as(7)ha=-hsa;hb=hpa-hp;hc=hpa,where hsa is calculated as follows: (8)hsa=hp2+2hphs+Es/Ephs22hp+Es/Ephs.Alsoϑx in (4) is an electromechanical coupling term of the bending moment, in which one-layered piezoelectric beam is calculated as(9)ϑx=-bxEpd312hphc2-hb2and for two-layered piezoelectric beam, its value depends on the types of electrical connection and is derived as follows:(10)ϑpx=2ϑsx=bxEpd31hphs24-hp+hs22,where subscripts “s” and “p” indicate series or parallel connections, respectively. These two types of electrical connections are indicated in Figure 3.Figure 3
Parallel and series electrical connections.Substituting (4) into (1) and considering the location of the piezoelectric layer along the x direction using Heaviside function Hex gives the governing EoM in terms of wx,t and vt as(11)∂2∂x2EIx∂2wx,t∂x2+∂2∂x2CsIx∂3wx,t∂x2∂t+Ca∂wx,t∂t+mx∂2wx,t∂t2+∂2∂x2ϑxvtHex-Hex-L=-mx+Mtδx-L∂2wbx,t∂t2.One more necessary equation to determine unknownswx,t and v(t) is derived out of the second constitutive equation of piezoelectric material; that is,(12)D3x,t=d31σpx,t+ε33TE3t,where D3 is the electric displacement and ε33T is the permittivity at constant stress. Rewriting (12) in terms of wx,t and v(t) gives (13)D3x,t=-d31Ephpc∂2wx,t∂x2-ε33svthp,where ε33s is the permittivity at constant strain. The electric charge generated at piezoelectric layer is calculated by applying the electric displacement as follows:(14)qt=∫SD3·ndA=-∫0Lbxd31Ephpc∂2wx,t∂x2+ε33svthpdx,where n is the unit normal vector to the piezoelectric plane. The voltage of the piezoelectric layer is calculated after multiplying electric resistance R by electric current, which is the first derivative of electric charge with respect to time as(15)vt=Rit=Rdqtdt=-R∫0Lbxd31Ephpc∂3wx,t∂x2∂tdx+ε33shp·∫0Lbxdxdvtdt.Equation (15) gives the voltage for a one-layered piezoelectric energy harvester, while the general form of the governing equation is given as(16)αvtR+βε33shp∫0Lbxdxdvtdt=-∫0Lbxd31Ephpc∂3wx,t∂x2∂tdx,where(17)for  one-layered  piezoelectric  beamα=β=1for  two-layered  piezoelectric  beam,  parallel  connectionα=12;β=1for  two-layered  piezoelectric  beam,  series  connectionα=1;β=12.Equations (11) and (16) are two coupled governing differential equations of a variable width piezoelectric beam, which can be solved by implementing eigenfunction expansion method as(18)wx,t=∑s=1∞φsxηstin which φs(x) are mass normalized mode shapes of the beam and ηs(t) are the modal coordinate.


### 2.2. Free Vibration of the Piezoelectric Exponentially Tapered Beam

As it was noted, in order to solve the coupled electromechanical equations, extracting the normalized eigenfunctions of the exponentially tapered beam is needed. The eigenfunctions are calculated by solving free vibration of the beam with clamped-free boundary conditions. The free vibration differential equation of a variable cross section beam by Euler-Bernoulli assumption is given as [24](19)∂2∂x2EIx∂2wx,t∂x2+mx∂2wx,t∂t2=0.For exponentially tapered beams, flexural rigidity and mass per unit length of the beam are exponentially varied along thex direction and are formulated as follows:(20)EIx=EI0e-cx;mx=m0e-cx,where EI0 and m0 are the flexural rigidity and mass per unit length of the beam at x=0. Using the method of separation of variables, that is, considering x,t=ψxT(t), the differential equation (19) is separated into spatial and temporal equations as follows: (21)d2dx2EIxd2ψxdx2-ω2mxψx=0,T¨t+ω2Tt=0,where solution of the spatial differential equation leads to the eigenfunctions as follows:(22)ψx=ecx/2C1cosh⁡⁡ξx+C2sinh⁡⁡ξx+C3cos⁡⁡λx+C4sin⁡λx;κ>c24,ψx=ecx/2C1cosh⁡⁡cx2+C2sinh⁡⁡cx2+C3+C4x;κ=c24,ψx=ecx/2C1cosh⁡⁡ξx+C2sinh⁡⁡ξx+C3cosh⁡⁡γx+C4sinh⁡⁡γx;κ>c24in which κ2=ω2m0/EI0 and ξ, λ, and γ are given as(23)ξ=4κ+c22,λ=4κ-c22,γ=c2-4κ2.In order to find the coefficients fromC1 to C4, following boundary conditions of a clamped-free beam with a tip mass are employed:(24)ψx=0,dψxdxx=0=0,ddxEIxd2ψxdx2+ω2Mtψxx=L=0,EIxd2ψxdx2-Itω2dψxdxx=L=0,where It is the rotatory inertia of the tip mass. Nontrivial solution of this system of equations is available when the determinant of coefficient matrix equals zero. Solving the characteristic equation derived from the determinant gives the eigenvalues of the system and as a result the mode shapes of the system are specified. Mass normalized mode shapes of the beam are calculated using the following formulations [9]:(25)ϕix=ψix∫0Lψixmxψixdx+ψiLMtψiL+dψix/dxItdψix/dxx=L.The orthogonality condition of the mass normalized modes shapes is given as follows [25]:(26)∫0Lϕrxmxϕsxdx+ϕrLMtϕsL+dϕrxdxItdϕsxdxx=L=δrs,∫0Ld2ϕrxdx2EIxd2ϕsxdx2=ωr2δrswhich can be used to transfer EoM to modal space.


### 2.3. Harmonic Base Excitation Solution

The mass normalized mode shapes of (25) are applied in eigenfunction expansion series of (18). Substituting (18) into coupled electromechanical equation (11) gives(27)∑s=1∞d2dx2EIxd2ϕsxdx2ηst+∑s=1∞d2dx2CsIxd2ϕsxdx2+Cadηstdt+mx∑s=1∞ϕsxd2ηstdt2+d2dx2ϑxHex-Hex-Lvt=-mx+Mtδx-L∂2wbx,t∂t2.Integrating (27) over the length of the beam after multiplying it by φrx gives the EoM in modal space as follows:(28)η¨rt+2ζrωrη˙rt+ωr2ηrt+χrvt=frtin which ωr and ζr are natural frequency and damping ratio of the rth mode and χr and fr(t) are given as(29)χr=∫0Lϕrxϑ′′xdx+dϕrxϑxdxx=0-dϕrxϑxdxx=L+2ϕr0ϑ′0-ϕrLϑ′L,frt=-∫0Lϕrxmxdx+MtϕrLd2gtdt2.In order to change the partial differential equation (16) into ordinary differential equation with respect to time, (18) is also substituted into (16) as follows:(30)vt+Rβαε33shp∫0Lbxdxdvtdt=-∑r=1∞Rd31Ephpcα∫0Lbxd2ϕrxdx2dxη˙rt.Simplifying (30) gives the second coupled ordinary differential equation of piezoelectric energy harvester as(31)v˙t+1τcvt=∑r=1∞φrη˙rtin which(32)τc=Rβαε33shp∫0Lbxdx,φr=-d31Ephpchpβε33s∫0Lbxϕr′′xdx∫0Lbxdx.Here to find the harmonic solution of the exponentially tapered piezoelectric energy harvester, it is assumed that the base is moving harmonically inz direction, which means that (33)gt=Y0ejωt.Due to the harmonic excitation of the beam, the unknown termsvt and ηr(t) are also expected to be harmonic as follows:(34)vt=V0ejωt,ηrt=Hrejωt.The voltage amplitudeV0 is calculated by substituting (33) and (34) into (28) and (31) as (35)V0=jω∑r=1∞φrFr/ωr2-ω2+2jζrωrω1+jωτc/τc+jω∑r=1∞φrχr/ωr2-ω2+2jζrωrω,where(36)Fr=Y0ω2∫0Lϕrxmxdx+MtϕrLand the temporal term amplitude Hr is given as(37)Hr=Fr-χrV0ωr2-ω2+2jζrωrω.


## 2.1. Electromechanical Formulation

Piezoelectric energy harvester, as shown in Figure1, is composed of a beam embedded by piezoelectric layers and is excited at its base. It is assumed that the piezoelectric layer is perfectly bonded to the substrate layer, while the integrated beam’s width is varying exponentially through the length by bx=b0e-cx, where c is tapering parameter. A proof mass is also attached on the tapered beam’s tip to regulate the fundamental frequency.Figure 1
Piezoelectric energy harvester.Because of the low thickness of the beam, the Euler-Bernoulli assumptions are employed to develop the displacement field. The governing Equation of Motion (EoM) of a beam embedded by piezoelectric layer using Euler-Bernoulli assumptions is given as [8](1)∂2Mx,t∂x2+∂2∂x2CsIx∂3wx,t∂x2∂t+Ca∂wx,t∂t+mx∂2wx,t∂t2=-mx+Mtδx-L∂2wbx,t∂t2in which Cs and Ca are equivalent strain rate and viscous air damping coefficients, respectively. w is the beam transverse deflection and wb is the base excitation displacement along z direction, while m(x) and Mt are mass per unit length and tip point mass, respectively. Area moment of inertia of the beam’s cross section changes exponentially; that is, Ix=I0e-cx, in which I0 is the moment of inertia of the beam at x=0. The internal moment of the beam M(x,t) is calculated by integrating the stress moment through the thickness as follows: (2)Mx,t=-∫tsσsbxzdz-∫tpσpbxzdz.In (2) σs and σp are defined as the normal stress in x direction at substrate and piezoelectric layers, respectively. Using the constitutive equation of isotropic and piezoelectric material, the normal stresses are formulated as(3)σs=Esε1sx,tσp=Epε1px,t-d31E3t,where Es and Ep are the modulus of elasticity of substrate and piezoelectric materials, respectively. Mechanical strain ε1(x,t)=-z∂2w(x,t)/∂x2 is calculated by applying the Euler-Bernoulli assumption. Piezoelectric electromechanical coupling is mathematically modeled by d31, and E3t=-v(t)/hp is the electric field through the z direction, where v(t) is the generated piezoelectric voltage. Substituting (3) into (2) gives the internal bending moment as(4)Mx,t=EIx∂2wx,t∂x2+ϑxvt,where EIx is the flexural rigidity of the composite beam and is calculated as(5)EIx=bxEshs312+2Ep3hs2+hp3-hs38for a two-layered piezoelectric beam, and(6)EIx=bxEshb3-ha3+Ephc3-hb33for one-layered piezoelectric energy harvester. Geometrical parameters of (5) and (6) are shown in Figure 2.Figure 2
Piezoelectric beam cross section: (a) one-layered piezoelectric beam and (b) two-layered piezoelectric beam.
(a)
(b)In (6) ha, hb, and hc are defined as(7)ha=-hsa;hb=hpa-hp;hc=hpa,where hsa is calculated as follows: (8)hsa=hp2+2hphs+Es/Ephs22hp+Es/Ephs.Alsoϑx in (4) is an electromechanical coupling term of the bending moment, in which one-layered piezoelectric beam is calculated as(9)ϑx=-bxEpd312hphc2-hb2and for two-layered piezoelectric beam, its value depends on the types of electrical connection and is derived as follows:(10)ϑpx=2ϑsx=bxEpd31hphs24-hp+hs22,where subscripts “s” and “p” indicate series or parallel connections, respectively. These two types of electrical connections are indicated in Figure 3.Figure 3
Parallel and series electrical connections.Substituting (4) into (1) and considering the location of the piezoelectric layer along the x direction using Heaviside function Hex gives the governing EoM in terms of wx,t and vt as(11)∂2∂x2EIx∂2wx,t∂x2+∂2∂x2CsIx∂3wx,t∂x2∂t+Ca∂wx,t∂t+mx∂2wx,t∂t2+∂2∂x2ϑxvtHex-Hex-L=-mx+Mtδx-L∂2wbx,t∂t2.One more necessary equation to determine unknownswx,t and v(t) is derived out of the second constitutive equation of piezoelectric material; that is,(12)D3x,t=d31σpx,t+ε33TE3t,where D3 is the electric displacement and ε33T is the permittivity at constant stress. Rewriting (12) in terms of wx,t and v(t) gives (13)D3x,t=-d31Ephpc∂2wx,t∂x2-ε33svthp,where ε33s is the permittivity at constant strain. The electric charge generated at piezoelectric layer is calculated by applying the electric displacement as follows:(14)qt=∫SD3·ndA=-∫0Lbxd31Ephpc∂2wx,t∂x2+ε33svthpdx,where n is the unit normal vector to the piezoelectric plane. The voltage of the piezoelectric layer is calculated after multiplying electric resistance R by electric current, which is the first derivative of electric charge with respect to time as(15)vt=Rit=Rdqtdt=-R∫0Lbxd31Ephpc∂3wx,t∂x2∂tdx+ε33shp·∫0Lbxdxdvtdt.Equation (15) gives the voltage for a one-layered piezoelectric energy harvester, while the general form of the governing equation is given as(16)αvtR+βε33shp∫0Lbxdxdvtdt=-∫0Lbxd31Ephpc∂3wx,t∂x2∂tdx,where(17)for  one-layered  piezoelectric  beamα=β=1for  two-layered  piezoelectric  beam,  parallel  connectionα=12;β=1for  two-layered  piezoelectric  beam,  series  connectionα=1;β=12.Equations (11) and (16) are two coupled governing differential equations of a variable width piezoelectric beam, which can be solved by implementing eigenfunction expansion method as(18)wx,t=∑s=1∞φsxηstin which φs(x) are mass normalized mode shapes of the beam and ηs(t) are the modal coordinate.


## 2.2. Free Vibration of the Piezoelectric Exponentially Tapered Beam

As it was noted, in order to solve the coupled electromechanical equations, extracting the normalized eigenfunctions of the exponentially tapered beam is needed. The eigenfunctions are calculated by solving free vibration of the beam with clamped-free boundary conditions. The free vibration differential equation of a variable cross section beam by Euler-Bernoulli assumption is given as [24](19)∂2∂x2EIx∂2wx,t∂x2+mx∂2wx,t∂t2=0.For exponentially tapered beams, flexural rigidity and mass per unit length of the beam are exponentially varied along thex direction and are formulated as follows:(20)EIx=EI0e-cx;mx=m0e-cx,where EI0 and m0 are the flexural rigidity and mass per unit length of the beam at x=0. Using the method of separation of variables, that is, considering x,t=ψxT(t), the differential equation (19) is separated into spatial and temporal equations as follows: (21)d2dx2EIxd2ψxdx2-ω2mxψx=0,T¨t+ω2Tt=0,where solution of the spatial differential equation leads to the eigenfunctions as follows:(22)ψx=ecx/2C1cosh⁡⁡ξx+C2sinh⁡⁡ξx+C3cos⁡⁡λx+C4sin⁡λx;κ>c24,ψx=ecx/2C1cosh⁡⁡cx2+C2sinh⁡⁡cx2+C3+C4x;κ=c24,ψx=ecx/2C1cosh⁡⁡ξx+C2sinh⁡⁡ξx+C3cosh⁡⁡γx+C4sinh⁡⁡γx;κ>c24in which κ2=ω2m0/EI0 and ξ, λ, and γ are given as(23)ξ=4κ+c22,λ=4κ-c22,γ=c2-4κ2.In order to find the coefficients fromC1 to C4, following boundary conditions of a clamped-free beam with a tip mass are employed:(24)ψx=0,dψxdxx=0=0,ddxEIxd2ψxdx2+ω2Mtψxx=L=0,EIxd2ψxdx2-Itω2dψxdxx=L=0,where It is the rotatory inertia of the tip mass. Nontrivial solution of this system of equations is available when the determinant of coefficient matrix equals zero. Solving the characteristic equation derived from the determinant gives the eigenvalues of the system and as a result the mode shapes of the system are specified. Mass normalized mode shapes of the beam are calculated using the following formulations [9]:(25)ϕix=ψix∫0Lψixmxψixdx+ψiLMtψiL+dψix/dxItdψix/dxx=L.The orthogonality condition of the mass normalized modes shapes is given as follows [25]:(26)∫0Lϕrxmxϕsxdx+ϕrLMtϕsL+dϕrxdxItdϕsxdxx=L=δrs,∫0Ld2ϕrxdx2EIxd2ϕsxdx2=ωr2δrswhich can be used to transfer EoM to modal space.


## 2.3. Harmonic Base Excitation Solution

The mass normalized mode shapes of (25) are applied in eigenfunction expansion series of (18). Substituting (18) into coupled electromechanical equation (11) gives(27)∑s=1∞d2dx2EIxd2ϕsxdx2ηst+∑s=1∞d2dx2CsIxd2ϕsxdx2+Cadηstdt+mx∑s=1∞ϕsxd2ηstdt2+d2dx2ϑxHex-Hex-Lvt=-mx+Mtδx-L∂2wbx,t∂t2.Integrating (27) over the length of the beam after multiplying it by φrx gives the EoM in modal space as follows:(28)η¨rt+2ζrωrη˙rt+ωr2ηrt+χrvt=frtin which ωr and ζr are natural frequency and damping ratio of the rth mode and χr and fr(t) are given as(29)χr=∫0Lϕrxϑ′′xdx+dϕrxϑxdxx=0-dϕrxϑxdxx=L+2ϕr0ϑ′0-ϕrLϑ′L,frt=-∫0Lϕrxmxdx+MtϕrLd2gtdt2.In order to change the partial differential equation (16) into ordinary differential equation with respect to time, (18) is also substituted into (16) as follows:(30)vt+Rβαε33shp∫0Lbxdxdvtdt=-∑r=1∞Rd31Ephpcα∫0Lbxd2ϕrxdx2dxη˙rt.Simplifying (30) gives the second coupled ordinary differential equation of piezoelectric energy harvester as(31)v˙t+1τcvt=∑r=1∞φrη˙rtin which(32)τc=Rβαε33shp∫0Lbxdx,φr=-d31Ephpchpβε33s∫0Lbxϕr′′xdx∫0Lbxdx.Here to find the harmonic solution of the exponentially tapered piezoelectric energy harvester, it is assumed that the base is moving harmonically inz direction, which means that (33)gt=Y0ejωt.Due to the harmonic excitation of the beam, the unknown termsvt and ηr(t) are also expected to be harmonic as follows:(34)vt=V0ejωt,ηrt=Hrejωt.The voltage amplitudeV0 is calculated by substituting (33) and (34) into (28) and (31) as (35)V0=jω∑r=1∞φrFr/ωr2-ω2+2jζrωrω1+jωτc/τc+jω∑r=1∞φrχr/ωr2-ω2+2jζrωrω,where(36)Fr=Y0ω2∫0Lϕrxmxdx+MtϕrLand the temporal term amplitude Hr is given as(37)Hr=Fr-χrV0ωr2-ω2+2jζrωrω.


## 3. Results and Discussion

Using the analytical formulation of the exponentially tapered piezoelectric energy harvester discussed in this paper, some sample problems are solved to show the performance of the solution. Regarding lack of results on exponentially tapered piezoelectric beam in the literature, to verify the analytical solution a constant cross section piezoelectric beam is firstly considered and the results are compared with those from experimental and numerical methods as well as with those available in the literature for this case.


### 3.1.  Experimental Verification of the Solution

As discussed previously, in this part a constant cross section beam (withc=0) is tested using the experimental set up of Figure 4. Experimental test is conducted on a cantilever unimorph piezoelectric beam with a PZT4 patch of length L=60 mm, width b0=10 mm, and thickness hp=0.6 mm which is bonded to a steel beam with the same dimension but thickness hs=0.7 mm (Table 1). A tip of 18 grams of mass which contains 9-gram steel mass together with 9-gram accelerometer is attached to the free end of the beam as shown in Figure 4(a). This accelerometer measures the beam’s response during experiment. The finite element model is created to be the same as the experimental model, while two steel cubes of 10 × 10 × 11.2 mm3 play the role of tip masses.Table 1
PZT and steel material properties.
Material
Property
Value
PZT 4
C
11 (GPa)
139
C
12 (GPa)
77.84
C
13 (GPa)
74.28
C
33 (GPa)
114.41
C
44 (GPa)
25.64
C
55 (GPa)
30.58
e
31 (Cm−2)
−5.2028
e
33 (Cm−2)
15.0804
e
15 (Cm−2)
12.7179
ε
0 (Fm−1)
8.854 × 10−12
ε
11/ε0
1475
ε
22/ε0
1475
ε
33/ε0
1300
ρ (Kg/m3)
7960
Steel
E (GPa)
200
υ
0.3
ρ (Kg/m3)
7800Figure 4
(a) Experiment equipment setup and (b) schematic of the experimental setup.
(a)
(b)A 440 N Tira TV51144 shaker is then used to excite the test structure. During the test execution another accelerometer is also installed on the support to measure the applying acceleration. The output of the piezoelectric layer is connected to a NI USB4431 data acquisition system through a 100 Ω electric resistance. Figure4(b) shows the schematic of the experimental setup.As the modal parameters of the complex beam are required to do further analysis, an Operational Modal Analysis (OMA) is initially performed while the piezoelectric electrodes are short circuit. After this initial experiment the first natural frequency and the associated damping ratio are measured as 47.6 Hz and 4.9%, respectively. These modeling parameters are gathered in Table2 for future citation. Then a sine sweep excitation from 10 to 100 Hz for duration of 20 seconds is applied on the piezoelectric energy harvester with 100 Ω electric resistance to examine the output voltage in the specified frequency range. Cancelling the noises is performed by averaging the results between 10 times repetition of the experiment.Table 2
Energy harvesters modelling parameters.
Parameter
Value
L (mm)
60
b
0 (mm)
10
h
s (mm)
0.7
h
p (mm)
0.6
M
t (gr)
9
z
0.049
R
l
100Figure5 depicts the voltage per the base acceleration versus frequency of the piezoelectric beam. This figure also compares the experimental results with the results from the finite element method of ANSYS, the presented analytical solution, and those from relations reported by Erturk and Inman [8, 9]. It reveals that the results from the present analytical solution are comparable with those from the experiments and the relations reported in [8, 9]. Analytically, in this situation bx equals b0, which means (10), (11), and (16) converge to those for unimorph energy harvester in [8], while the terms of tip mass are added from [9]. The simplified forms of (10), (11), and (16) for the case c=0 are derived as follows:(38)ϑx=ϑ=-b0Epd312hphc2-hb2,EI0∂4wx,t∂x4+CsI0∂5wx,t∂x4∂t+Ca∂wx,t∂t+m0∂2wx,t∂t2+ϑvtdδxdx-dδx-Ldx=-m0+Mtδx-L∂2wbx,t∂t2,vtR+ε33sb0Lhpdvtdt=-∫0Lb0d31Ephpc∂3wx,t∂x2∂tdx.Figure 5
Output voltage/input acceleration versus frequency.In accordance with Figure5, it can be also concluded that the results of present work are in a good agreement with those from finite element solution of commercial software for analyzing piezoelectric beams, while the present study has lower computational effort and complexity.


### 3.2. Case Studies

Figure6 plots geometry of the beam with different tapering parameter values (i.e., c=0, 5, 10, 15, and 20). Although, increasing tapering parameter may lead to higher voltage to weight ratio [13], it also causes increasing fundamental frequency of the beam. In view of taking full advantage of beam to harvest energy, according to Figure 5, a designer needs to keep the first natural frequency of the beam close to the exciting frequency. For this purpose the designer can either use a thinner substrate layer or mount a tip mass. Some case studies are performed in this section to show the abilities of the presented analytical solution as a design tool to investigate the output voltage per unit mass of the energy harvester device. All geometrical parameters of the case studies are similar to those listed in Table 2, unless mentioned.Figure 6
Geometry of the beam with different tapering parameter values.


#### 3.2.1. Numerical Verification of the Solution

Before going into the parameter study to refine the confidence, the results from the presented analytical solution are also verified for the beams with various tapering parameter as well as different types of electrical connections using finite element method. In this example, the electrical resistance is taken to be 1000 Ω, and the damping ratio is assumed to be 1 percent. Moreover, no tip mass is attached to the beam. For this verification procedure, the output voltage generated out of the piezoelectric beam at its fundamental frequency is tabulated in Table3 for different tapering parameter and electrical connections. According to this table the maximum difference of these two methods is 3.6%, which means that the current formulation well predicts the tapered piezoelectric energy harvester’s behavior. Also it can be noted that increasing tapering parameter may reduce the generated voltage per exciting acceleration, but at the same time it makes the structure lighter. Hence, if the total mass is an important design parameter, comparing the voltage per unit mass parameter for energy harvesters will be a real parameter during case studies. According to this statement we consider this parameter during our later studies.Table 3
Comparison of analytic and FEM results.
C
0
5
10
15
20
Unimorph
Analytic (V/g)
0.5711
0.499
0.438
0.3842
0.3377
FEM (V/g)
0.592561
0.516427
0.451596
0.395634
0.347023
Difference (%)
3.621737
3.374533
3.010656
2.890045
2.686565
Bimorph series
Analytic (V/g)
0.6252
0.5479
0.4802
0.4214
0.3704
FEM (V/g)
0.64757
0.563801
0.490386
0.430593
0.377891
Difference (%)
3.454453
2.820321
2.077139
2.134963
1.982318
Bimorph parallel
Analytic (V/g)
1.156
1.011
0.8847
0.7751
0.6805
FEM (V/g)
1.18912
1.03459
0.901908
0.788796
0.691405
Difference (%)
2.785253
2.28013
1.907955
1.736317
1.577223


#### 3.2.2. Tapering Parameter Effects on Output Voltage

(a) Tuning the Natural Frequency Using Substrate Thickness. As we mentioned earlier, in order to take full advantage of beam to harvest energy, one needs to keep the first natural frequency of the beam close to the exciting frequency while tapering parameter is improved. In this section, tuning this natural frequency is done by changing substrate thickness for different length to width ratio. All parameters of the beam are the same as those in Section 3.2.1 for case c=0. Figures 7–9 depict the voltage density (V/mT0g) different tapering parameter taken at fundamental frequency for unimorph and bimorph with series and parallel connections. In these figures mT0 is defined as the total mass of the energy harvester. Evaluating the results shows that tapering the beam with exponential distribution leads to extracting higher voltage density from the energy harvester. Moreover, tapering the beam makes a uniform strain distribution over the piezoelectric layer that causes more voltage generation [13]. For all cases, with increasing the beam’s length to base width ratio, the tapering parameter with the highest voltage density is decreased. It is also observed that increasing the beam’s length causes increasing the voltage density, because of contributing more piezoelectric bulk during power generation.Figure 7
Tapering and length effects on unimorph modified thickness.Figure 8
Tapering and length effects on bimorph with series connection, modified thickness.Figure 9
Tapering and length effects on bimorph with parallel connection, modified thickness.(b) Tuning the Natural Frequency Using Tip Mass. Another way to adjust the first natural frequency of a beam with different tapering parameter is to add a tip mass. The results of the current models are plotted in Figures 10–12 for unimorph and bimorph with series and parallel connections.Figure 10
Tapering and length effects on unimorph, with tip mass.Figure 11
Tapering and length effects on bimorph with series connection, with tip mass.Figure 12
Tapering and length effects on bimorph with parallel connection, with tip mass.According to these figures, the energy harvesting device with tip mass and varying tapering parameter behaves in a way similar to that of the beam without tip mass and varying thickness (i.e., Section3.2.2 (a)). It means that by adding a tip mass designer would be also able to improve the voltage density value for a beam. In this approach a mass is added to the system which makes the device weightier, and on the other hand tapering decreases beam’s mass. Therefore, in this method the total mass of the system decreases in a lower rate in comparison with the previous method. Referring to (35) it can be noted that, for higher tapering parameters which are associated with weightier tip mass, the output voltage value improves. Compromising these effects may be the reason for achieving the maximum voltage density at the lower c in comparison with the previous method. In addition, comparing both tuning methods reveals that adding the tip mass decreases the value of voltage density of the beams with the same value of tapering parameter. Therefore, if the designed beam is strong enough to tolerate the stresses during its estimated life time, it is more appropriate to thin the substrate layer in order to tune its fundamental frequency otherwise adding the tip mass will be carried out, alternatively.


#### 3.2.3. Tapering Parameter and Electric Resistance Effects on Output Power

Electric resistance is a critical parameter for extracting the maximum power density (P/mg2) from the device [8]. In this section the same beam with L=80 mm is considered and the substrate layer’s thickness is changed to obtain a constant natural frequency for different c values. The power density versus electric resistance is depicted in Figures 13–15 for unimorph and bimorph with series and parallel connections. From these figures it is observed that there exists an optimum value of electric resistance which results in maximum power density for an energy harvesting device. This optimum value depends on tapering parameter. Increasing tapering parameter value leads to an increase in the optimum electric resistance. In addition, when electric resistance is smaller than a specified value, tapering would decrease the power density of the device, which is not desired. But for higher electric resistances, tapering parameter plays a key role for gaining maximum power with minimum weight. This value of the electric resistance and the amount of improvement in power density by tapering depends on the type of electric connection. In this example, for the highest value of the electric resistance, that is, 1 MΩ, exponential tapering will grow the power per mass of the device about 29 percent for unimorph and 14 and 52 percent for bimorph with series and parallel connections, respectively.Figure 13
Tapering and electric resistance effects on unimorph.Figure 14
Tapering and electric resistance effects on bimorph with series connection.Figure 15
Tapering and electric resistance effects on bimorph with parallel connection.


### 3.3. Exponentially Tapered versus Trapezoidal Energy Harvesters

Figure16 depicts the considered geometries for exponentially and linearly tapered energy harvesters with the parameters in Table 4 which are the same as those employed by Rosa and de Marqui Jr. [21]. In presence of 1 KΩ and 1 MΩ electric resistances, both problems are solved and the results are compared with those reported by Rosa and de Marqui Jr. [21] in Figure 17. From this figure one can observe that because of its lower piezoelectric volume the voltage generated from exponentially tapered beam is lower than those from linearly tapered beam. However, the linearly tapered beam may produce lower voltage density. Therefore, a trade-off between voltage, weight, electric resistance, and ease of construction should be always carried out to lead to a better harvester.Table 4
Energy harvesters modelling parameters.
Parameter
Value
L (mm)
50.8
b
0 (mm)
31.5
b
T (mm)
7.25
h
s (mm)
0.14
h
p (mm)
0.26
M
t (gr)
0.0164
z
0.0073Figure 16
Exponentially (c=28.92) and linearly tapered energy harvesters with the same base and tip (bT) widths.Figure 17
Comparison ofV/g values between exponentially and linearly tapered energy harvesters.


## 3.1.  Experimental Verification of the Solution

As discussed previously, in this part a constant cross section beam (withc=0) is tested using the experimental set up of Figure 4. Experimental test is conducted on a cantilever unimorph piezoelectric beam with a PZT4 patch of length L=60 mm, width b0=10 mm, and thickness hp=0.6 mm which is bonded to a steel beam with the same dimension but thickness hs=0.7 mm (Table 1). A tip of 18 grams of mass which contains 9-gram steel mass together with 9-gram accelerometer is attached to the free end of the beam as shown in Figure 4(a). This accelerometer measures the beam’s response during experiment. The finite element model is created to be the same as the experimental model, while two steel cubes of 10 × 10 × 11.2 mm3 play the role of tip masses.Table 1
PZT and steel material properties.
Material
Property
Value
PZT 4
C
11 (GPa)
139
C
12 (GPa)
77.84
C
13 (GPa)
74.28
C
33 (GPa)
114.41
C
44 (GPa)
25.64
C
55 (GPa)
30.58
e
31 (Cm−2)
−5.2028
e
33 (Cm−2)
15.0804
e
15 (Cm−2)
12.7179
ε
0 (Fm−1)
8.854 × 10−12
ε
11/ε0
1475
ε
22/ε0
1475
ε
33/ε0
1300
ρ (Kg/m3)
7960
Steel
E (GPa)
200
υ
0.3
ρ (Kg/m3)
7800Figure 4
(a) Experiment equipment setup and (b) schematic of the experimental setup.
(a)
(b)A 440 N Tira TV51144 shaker is then used to excite the test structure. During the test execution another accelerometer is also installed on the support to measure the applying acceleration. The output of the piezoelectric layer is connected to a NI USB4431 data acquisition system through a 100 Ω electric resistance. Figure4(b) shows the schematic of the experimental setup.As the modal parameters of the complex beam are required to do further analysis, an Operational Modal Analysis (OMA) is initially performed while the piezoelectric electrodes are short circuit. After this initial experiment the first natural frequency and the associated damping ratio are measured as 47.6 Hz and 4.9%, respectively. These modeling parameters are gathered in Table2 for future citation. Then a sine sweep excitation from 10 to 100 Hz for duration of 20 seconds is applied on the piezoelectric energy harvester with 100 Ω electric resistance to examine the output voltage in the specified frequency range. Cancelling the noises is performed by averaging the results between 10 times repetition of the experiment.Table 2
Energy harvesters modelling parameters.
Parameter
Value
L (mm)
60
b
0 (mm)
10
h
s (mm)
0.7
h
p (mm)
0.6
M
t (gr)
9
z
0.049
R
l
100Figure5 depicts the voltage per the base acceleration versus frequency of the piezoelectric beam. This figure also compares the experimental results with the results from the finite element method of ANSYS, the presented analytical solution, and those from relations reported by Erturk and Inman [8, 9]. It reveals that the results from the present analytical solution are comparable with those from the experiments and the relations reported in [8, 9]. Analytically, in this situation bx equals b0, which means (10), (11), and (16) converge to those for unimorph energy harvester in [8], while the terms of tip mass are added from [9]. The simplified forms of (10), (11), and (16) for the case c=0 are derived as follows:(38)ϑx=ϑ=-b0Epd312hphc2-hb2,EI0∂4wx,t∂x4+CsI0∂5wx,t∂x4∂t+Ca∂wx,t∂t+m0∂2wx,t∂t2+ϑvtdδxdx-dδx-Ldx=-m0+Mtδx-L∂2wbx,t∂t2,vtR+ε33sb0Lhpdvtdt=-∫0Lb0d31Ephpc∂3wx,t∂x2∂tdx.Figure 5
Output voltage/input acceleration versus frequency.In accordance with Figure5, it can be also concluded that the results of present work are in a good agreement with those from finite element solution of commercial software for analyzing piezoelectric beams, while the present study has lower computational effort and complexity.


## 3.2. Case Studies

Figure6 plots geometry of the beam with different tapering parameter values (i.e., c=0, 5, 10, 15, and 20). Although, increasing tapering parameter may lead to higher voltage to weight ratio [13], it also causes increasing fundamental frequency of the beam. In view of taking full advantage of beam to harvest energy, according to Figure 5, a designer needs to keep the first natural frequency of the beam close to the exciting frequency. For this purpose the designer can either use a thinner substrate layer or mount a tip mass. Some case studies are performed in this section to show the abilities of the presented analytical solution as a design tool to investigate the output voltage per unit mass of the energy harvester device. All geometrical parameters of the case studies are similar to those listed in Table 2, unless mentioned.Figure 6
Geometry of the beam with different tapering parameter values.


### 3.2.1. Numerical Verification of the Solution

Before going into the parameter study to refine the confidence, the results from the presented analytical solution are also verified for the beams with various tapering parameter as well as different types of electrical connections using finite element method. In this example, the electrical resistance is taken to be 1000 Ω, and the damping ratio is assumed to be 1 percent. Moreover, no tip mass is attached to the beam. For this verification procedure, the output voltage generated out of the piezoelectric beam at its fundamental frequency is tabulated in Table3 for different tapering parameter and electrical connections. According to this table the maximum difference of these two methods is 3.6%, which means that the current formulation well predicts the tapered piezoelectric energy harvester’s behavior. Also it can be noted that increasing tapering parameter may reduce the generated voltage per exciting acceleration, but at the same time it makes the structure lighter. Hence, if the total mass is an important design parameter, comparing the voltage per unit mass parameter for energy harvesters will be a real parameter during case studies. According to this statement we consider this parameter during our later studies.Table 3
Comparison of analytic and FEM results.
C
0
5
10
15
20
Unimorph
Analytic (V/g)
0.5711
0.499
0.438
0.3842
0.3377
FEM (V/g)
0.592561
0.516427
0.451596
0.395634
0.347023
Difference (%)
3.621737
3.374533
3.010656
2.890045
2.686565
Bimorph series
Analytic (V/g)
0.6252
0.5479
0.4802
0.4214
0.3704
FEM (V/g)
0.64757
0.563801
0.490386
0.430593
0.377891
Difference (%)
3.454453
2.820321
2.077139
2.134963
1.982318
Bimorph parallel
Analytic (V/g)
1.156
1.011
0.8847
0.7751
0.6805
FEM (V/g)
1.18912
1.03459
0.901908
0.788796
0.691405
Difference (%)
2.785253
2.28013
1.907955
1.736317
1.577223


### 3.2.2. Tapering Parameter Effects on Output Voltage

(a) Tuning the Natural Frequency Using Substrate Thickness. As we mentioned earlier, in order to take full advantage of beam to harvest energy, one needs to keep the first natural frequency of the beam close to the exciting frequency while tapering parameter is improved. In this section, tuning this natural frequency is done by changing substrate thickness for different length to width ratio. All parameters of the beam are the same as those in Section 3.2.1 for case c=0. Figures 7–9 depict the voltage density (V/mT0g) different tapering parameter taken at fundamental frequency for unimorph and bimorph with series and parallel connections. In these figures mT0 is defined as the total mass of the energy harvester. Evaluating the results shows that tapering the beam with exponential distribution leads to extracting higher voltage density from the energy harvester. Moreover, tapering the beam makes a uniform strain distribution over the piezoelectric layer that causes more voltage generation [13]. For all cases, with increasing the beam’s length to base width ratio, the tapering parameter with the highest voltage density is decreased. It is also observed that increasing the beam’s length causes increasing the voltage density, because of contributing more piezoelectric bulk during power generation.Figure 7
Tapering and length effects on unimorph modified thickness.Figure 8
Tapering and length effects on bimorph with series connection, modified thickness.Figure 9
Tapering and length effects on bimorph with parallel connection, modified thickness.(b) Tuning the Natural Frequency Using Tip Mass. Another way to adjust the first natural frequency of a beam with different tapering parameter is to add a tip mass. The results of the current models are plotted in Figures 10–12 for unimorph and bimorph with series and parallel connections.Figure 10
Tapering and length effects on unimorph, with tip mass.Figure 11
Tapering and length effects on bimorph with series connection, with tip mass.Figure 12
Tapering and length effects on bimorph with parallel connection, with tip mass.According to these figures, the energy harvesting device with tip mass and varying tapering parameter behaves in a way similar to that of the beam without tip mass and varying thickness (i.e., Section3.2.2 (a)). It means that by adding a tip mass designer would be also able to improve the voltage density value for a beam. In this approach a mass is added to the system which makes the device weightier, and on the other hand tapering decreases beam’s mass. Therefore, in this method the total mass of the system decreases in a lower rate in comparison with the previous method. Referring to (35) it can be noted that, for higher tapering parameters which are associated with weightier tip mass, the output voltage value improves. Compromising these effects may be the reason for achieving the maximum voltage density at the lower c in comparison with the previous method. In addition, comparing both tuning methods reveals that adding the tip mass decreases the value of voltage density of the beams with the same value of tapering parameter. Therefore, if the designed beam is strong enough to tolerate the stresses during its estimated life time, it is more appropriate to thin the substrate layer in order to tune its fundamental frequency otherwise adding the tip mass will be carried out, alternatively.


### 3.2.3. Tapering Parameter and Electric Resistance Effects on Output Power

Electric resistance is a critical parameter for extracting the maximum power density (P/mg2) from the device [8]. In this section the same beam with L=80 mm is considered and the substrate layer’s thickness is changed to obtain a constant natural frequency for different c values. The power density versus electric resistance is depicted in Figures 13–15 for unimorph and bimorph with series and parallel connections. From these figures it is observed that there exists an optimum value of electric resistance which results in maximum power density for an energy harvesting device. This optimum value depends on tapering parameter. Increasing tapering parameter value leads to an increase in the optimum electric resistance. In addition, when electric resistance is smaller than a specified value, tapering would decrease the power density of the device, which is not desired. But for higher electric resistances, tapering parameter plays a key role for gaining maximum power with minimum weight. This value of the electric resistance and the amount of improvement in power density by tapering depends on the type of electric connection. In this example, for the highest value of the electric resistance, that is, 1 MΩ, exponential tapering will grow the power per mass of the device about 29 percent for unimorph and 14 and 52 percent for bimorph with series and parallel connections, respectively.Figure 13
Tapering and electric resistance effects on unimorph.Figure 14
Tapering and electric resistance effects on bimorph with series connection.Figure 15
Tapering and electric resistance effects on bimorph with parallel connection.


## 3.2.1. Numerical Verification of the Solution

Before going into the parameter study to refine the confidence, the results from the presented analytical solution are also verified for the beams with various tapering parameter as well as different types of electrical connections using finite element method. In this example, the electrical resistance is taken to be 1000 Ω, and the damping ratio is assumed to be 1 percent. Moreover, no tip mass is attached to the beam. For this verification procedure, the output voltage generated out of the piezoelectric beam at its fundamental frequency is tabulated in Table3 for different tapering parameter and electrical connections. According to this table the maximum difference of these two methods is 3.6%, which means that the current formulation well predicts the tapered piezoelectric energy harvester’s behavior. Also it can be noted that increasing tapering parameter may reduce the generated voltage per exciting acceleration, but at the same time it makes the structure lighter. Hence, if the total mass is an important design parameter, comparing the voltage per unit mass parameter for energy harvesters will be a real parameter during case studies. According to this statement we consider this parameter during our later studies.Table 3
Comparison of analytic and FEM results.
C
0
5
10
15
20
Unimorph
Analytic (V/g)
0.5711
0.499
0.438
0.3842
0.3377
FEM (V/g)
0.592561
0.516427
0.451596
0.395634
0.347023
Difference (%)
3.621737
3.374533
3.010656
2.890045
2.686565
Bimorph series
Analytic (V/g)
0.6252
0.5479
0.4802
0.4214
0.3704
FEM (V/g)
0.64757
0.563801
0.490386
0.430593
0.377891
Difference (%)
3.454453
2.820321
2.077139
2.134963
1.982318
Bimorph parallel
Analytic (V/g)
1.156
1.011
0.8847
0.7751
0.6805
FEM (V/g)
1.18912
1.03459
0.901908
0.788796
0.691405
Difference (%)
2.785253
2.28013
1.907955
1.736317
1.577223


## 3.2.2. Tapering Parameter Effects on Output Voltage

(a) Tuning the Natural Frequency Using Substrate Thickness. As we mentioned earlier, in order to take full advantage of beam to harvest energy, one needs to keep the first natural frequency of the beam close to the exciting frequency while tapering parameter is improved. In this section, tuning this natural frequency is done by changing substrate thickness for different length to width ratio. All parameters of the beam are the same as those in Section 3.2.1 for case c=0. Figures 7–9 depict the voltage density (V/mT0g) different tapering parameter taken at fundamental frequency for unimorph and bimorph with series and parallel connections. In these figures mT0 is defined as the total mass of the energy harvester. Evaluating the results shows that tapering the beam with exponential distribution leads to extracting higher voltage density from the energy harvester. Moreover, tapering the beam makes a uniform strain distribution over the piezoelectric layer that causes more voltage generation [13]. For all cases, with increasing the beam’s length to base width ratio, the tapering parameter with the highest voltage density is decreased. It is also observed that increasing the beam’s length causes increasing the voltage density, because of contributing more piezoelectric bulk during power generation.Figure 7
Tapering and length effects on unimorph modified thickness.Figure 8
Tapering and length effects on bimorph with series connection, modified thickness.Figure 9
Tapering and length effects on bimorph with parallel connection, modified thickness.(b) Tuning the Natural Frequency Using Tip Mass. Another way to adjust the first natural frequency of a beam with different tapering parameter is to add a tip mass. The results of the current models are plotted in Figures 10–12 for unimorph and bimorph with series and parallel connections.Figure 10
Tapering and length effects on unimorph, with tip mass.Figure 11
Tapering and length effects on bimorph with series connection, with tip mass.Figure 12
Tapering and length effects on bimorph with parallel connection, with tip mass.According to these figures, the energy harvesting device with tip mass and varying tapering parameter behaves in a way similar to that of the beam without tip mass and varying thickness (i.e., Section3.2.2 (a)). It means that by adding a tip mass designer would be also able to improve the voltage density value for a beam. In this approach a mass is added to the system which makes the device weightier, and on the other hand tapering decreases beam’s mass. Therefore, in this method the total mass of the system decreases in a lower rate in comparison with the previous method. Referring to (35) it can be noted that, for higher tapering parameters which are associated with weightier tip mass, the output voltage value improves. Compromising these effects may be the reason for achieving the maximum voltage density at the lower c in comparison with the previous method. In addition, comparing both tuning methods reveals that adding the tip mass decreases the value of voltage density of the beams with the same value of tapering parameter. Therefore, if the designed beam is strong enough to tolerate the stresses during its estimated life time, it is more appropriate to thin the substrate layer in order to tune its fundamental frequency otherwise adding the tip mass will be carried out, alternatively.


## 3.2.3. Tapering Parameter and Electric Resistance Effects on Output Power

Electric resistance is a critical parameter for extracting the maximum power density (P/mg2) from the device [8]. In this section the same beam with L=80 mm is considered and the substrate layer’s thickness is changed to obtain a constant natural frequency for different c values. The power density versus electric resistance is depicted in Figures 13–15 for unimorph and bimorph with series and parallel connections. From these figures it is observed that there exists an optimum value of electric resistance which results in maximum power density for an energy harvesting device. This optimum value depends on tapering parameter. Increasing tapering parameter value leads to an increase in the optimum electric resistance. In addition, when electric resistance is smaller than a specified value, tapering would decrease the power density of the device, which is not desired. But for higher electric resistances, tapering parameter plays a key role for gaining maximum power with minimum weight. This value of the electric resistance and the amount of improvement in power density by tapering depends on the type of electric connection. In this example, for the highest value of the electric resistance, that is, 1 MΩ, exponential tapering will grow the power per mass of the device about 29 percent for unimorph and 14 and 52 percent for bimorph with series and parallel connections, respectively.Figure 13
Tapering and electric resistance effects on unimorph.Figure 14
Tapering and electric resistance effects on bimorph with series connection.Figure 15
Tapering and electric resistance effects on bimorph with parallel connection.


## 3.3. Exponentially Tapered versus Trapezoidal Energy Harvesters

Figure16 depicts the considered geometries for exponentially and linearly tapered energy harvesters with the parameters in Table 4 which are the same as those employed by Rosa and de Marqui Jr. [21]. In presence of 1 KΩ and 1 MΩ electric resistances, both problems are solved and the results are compared with those reported by Rosa and de Marqui Jr. [21] in Figure 17. From this figure one can observe that because of its lower piezoelectric volume the voltage generated from exponentially tapered beam is lower than those from linearly tapered beam. However, the linearly tapered beam may produce lower voltage density. Therefore, a trade-off between voltage, weight, electric resistance, and ease of construction should be always carried out to lead to a better harvester.Table 4
Energy harvesters modelling parameters.
Parameter
Value
L (mm)
50.8
b
0 (mm)
31.5
b
T (mm)
7.25
h
s (mm)
0.14
h
p (mm)
0.26
M
t (gr)
0.0164
z
0.0073Figure 16
Exponentially (c=28.92) and linearly tapered energy harvesters with the same base and tip (bT) widths.Figure 17
Comparison ofV/g values between exponentially and linearly tapered energy harvesters.


## 4. Conclusions

In this paper, an analytical solution for exponentially tapered energy harvesting device has been presented. The proposed formulations can calculate the output voltage of unimorph and bimorph with series and bimorph with parallel connections, while the tip mass is also considered. Comparing the results of the given analytical solution with experimental and numerical method results proves the analytical formulation validity to calculate the generated voltage. After verifying the formulations, parametric study is performed on tapering parameter, beam’s length, and electric resistance. While tapering the beam, its first natural frequency increases, therefore two approaches, that is, using a thinner substrate layer or mounting a tip mass, have been implemented to adjust its natural frequency. In both methods, tapering leads to a maximum value for the voltage density for different lengths of the beam. It has been also noted that electric resistance is an effective parameter on the output power of the piezoelectric beam. Our study has shown that the efficacy of tapering depends on the electric resistance, where in lower values of electric resistance than a specified one the tapering reduces the electric power density. Consequently, not only does the electric power generated in energy harvesting device depend on tapering, but also it is dependent on all parameters such as beam’s length, thickness, tip mass, and electric resistance. Therefore, it is feasible to improve the power density of the piezoelectric beam by tapering it exponentially provided that all parameters are considered in designing procedure.



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*Source: 426876-2015-07-15.xml*