# A Three-Dimensional Model of the Effective Electromechanical Impedance for an Embedded PZT Transducer

Authors: Chunyuan Zuo; Xin Feng; Jing Zhou
Journal: Mathematical Problems in Engineering
 (2013)

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## Abstract

A three-dimensional model of the effective electromechanical impedance for an embedded PZT transducer is proposed by considering the interaction between a PZT patch and a host structure. By introducing an effective mechanical impedance, the coupled electromechanical admittance formulations are derived using the piezoelectric constitutive equations. Then, a modified methodology for monitoring structure changes using an electromechanical impedance (EMI) technique is proposed. In the proposed method, the changes in the host structure are monitored by using the “active” part associated with the structural mechanical impedance, which is extracted from the measured raw admittance signatures. The strength gain of a concrete beam with embedded PZT transducers during the curing age was monitored with the proposed methodology. The experimental results demonstrate that the use of the “active” part is more sensitive as opposed to the raw admittance signatures for structural health monitoring (SHM).


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## Body

## 1. Introduction

In general, a typical structural health monitoring (SHM) system includes three major components: a sensor system, a data processing system (including data acquisition, transmission, and storage), and a health evaluation system. The sensor system is the key component in the SHM system [1, 2]. The advent of commercially available smart piezoelectric materials has provided new opportunities for SHM. The key characteristic of PZT materials is the utilization of the converse piezoelectric effect to actuate the structure in addition to the direct piezoelectric effect to sense structural deformation [3, 4]. By the direct and converse piezoelectric effects of PZT materials, the electromechanical impedance (EMI) technique simultaneously employs piezoelectric ceramic (PZT) patches as both sensors and actuators.In recent years, the EMI technique has gained wide attention and emerged as a favorable tool for structural damage detection. This technique can diagnose several types of structures, including bolted connections [5, 6], cable-stayed bridges [7], aerospace structures [8], reinforced concrete structures [9, 10], and pipeline structures [11]. The basic concept of this approach is to use high-frequency excitations to monitor the local area of the host structure for changes in the structural mechanical impedance caused by damage [12]. In the EMI technique, a small-size PZT patch is bonded to or embedded into the monitored structure and excited by an alternating voltage sweep signal. The PZT patch transfers the vibrations to the host structure, which is deformed and produces a local dynamic response. Simultaneously, the response of the host structure is transferred back to the PZT patch. Because of the electromechanical coupling property of PZT materials, the structural mechanical impedance of the host structure can be determined by the electrical impedance of the PZT patch. By monitoring the variations of the measured electrical impedance, the change in the structural mechanical impedance induced by structural damage can be detected. The advantages of EMI-based approaches include but are not limited to a lightweight and inexpensive sensor, high sensitivity to incipient damage for high-frequency actuating, and immunity to ambient or far-field loads.The interaction between the PZT patch and the host structure is the key issue for sensor design and data interpretation in EMI-based methods. During the last two decades, several modeling approaches have been proposed for describing the PZT-structure interaction. Among them, two well-known approaches are the static approach and the impedance approach. The former one developed by Crawley and de Luis [16] uses a statically determined equivalent force and moment as the amplitude of the forcing function. It is assumed that the mechanical interaction between the bonded actuator and the host structure occurs at the ends of the actuator in the form of concentrated forces. This approach is simple and easy to use but it often leads to misleading results. More importantly, the static approach does not correctly capture the physical essence of the PZT-structure interaction. In order to improve the accuracy, Liang et al. [13] presented the impedance approach instead of the static approach. This approach modeled the PZT patch connected to the host structure represented by the mechanical impedance Zs, as shown in Figure 1. The multidimensional effects associated with PZT vibrations are ignored in Liang’s model. Zhou et al. [14] extended the one-dimensional (1D) model to a generic two-dimensional (2D) PZT-structure model by considering the coupled vibration in the plane. This model replaced the structural impedance with a matrix consisting of the direct impedances Zxx and Zyy and the cross-impedances Zxy and Zyx, as shown in Figure 2. Experimental difficulties prevent the direct application of Zhou’s model for extraction of the structural mechanical impedance. To overcome this shortcoming, a new concept of “effective impedance” was introduced in the effective impedance model of Bhalla and Soh [15]. In this model, the PZT-structure mechanical interaction extends all over the finite-sized PZT patch, as shown in Figure 3. This model condenses the two-directional physical coupling between the PZT patch and the host structure into a single impedance term, which can be determined from the measured admittance signatures. Hence, the model bridges the gap between Liang’s 1D model and Zhou’s 2D model.Figure 1
Liang’s 1D impedance model [13].Figure 2
Zhou’s 2D impedance model [14].Figure 3
2D effective impedance model of Bhalla and Soh [15].Conventionally, the impedance models are usually considered as 1D or 2D, and the coupling between the extensional and longitudinal vibrations is neglected. To satisfy the requirements of the 1D model, the thickness of the PZT patch must be much smaller than its radius (length and width). However, the PZT patch has finite dimensions of thickness and radius (length and width) in practical applications, and both the extensional and longitudinal vibrations are important [17]. Hence, there is a need for the development of a three-dimensional (3D) PZT-structure interaction model, which considers the coupling between the extensional and longitudinal vibrations. The study presented here aims to model the PZT-structure interaction considering the 3D coupled vibration effect. In this paper, a 3D effective electromechanical impedance model for an embedded PZT plate is proposed by adopting the “effective impedance” concept. The new model describes the extensional actuations along the radial direction and longitudinal actuation along the thickness direction of the PZT patch. The advantage of the 3D effective impedance model is that it can only capture the “active part” associated with the structural mechanical impedance by filtering the PZT contribution. Then, the inherent properties of the monitored structure can be detected with a higher accuracy than with the raw admittance signal only. To validate the effectiveness of the proposed method, a concrete beam with embedded PZT transducers during the curing age was measured to monitor the strength gain.


## 2. Theoretical Background

In a linear vibration system, the steady-state responsex(t), that is, displacement, velocity, or acceleration, is caused by the harmonic force F(t). x(t) and F(t) have the same frequency, and x(t) lags behind F(t) by a phase angle ϕ. The structural mechanical impedance Z is defined as the ratio of the harmonic excitation to its steady-state response. Conventionally, the velocity impedance is regarded as the mechanical impedance. Therefore, the structural mechanical impedance is expressed as
(1)Z=Fu˙=Foejωtu˙oej(ωt-ϕ)=Fou˙oejϕ,
where Fo is the amplitude of the excitation force, ω is the circular frequency of the excitation force, u˙o is the amplitude of the velocity, and ϕ is the phase angle of the velocity response.The existing models are based on the definition that the structural mechanical impedance refers to a particular point, and the point considered is the PZT end point. However, the PZT-structure interaction is not restricted at the PZT end point, and it extends all over the PZT patch. The force transmission between the PZT patch and the host structure occurs along the entire boundary of the PZT patch [15]. Ignoring the effect of the PZT vibrations in the thickness direction and assuming the frequency range of interest to be much lower than the dominant modes of thickness vibration, a new concept of “effective mechanical impedance” was defined by Bhalla and Soh [15]. However, the embedded PZT patch has both the extensional and longitudinal vibrations in practical applications. Hence, the formulations of the “effective mechanical impedance” of 3D model need to be established.We consider a circular PZT patch embedded into an unknown host structure, as shown in Figure4, subjected to an electric field. The interaction of the PZT patch with the host structure is represented in the form of the boundary traction f, and the PZT-structure interaction force is assumed along the entire boundary of the PZT patch. Further, the PZT patch is assumed to be extremely small as compared to the host structure, and it has negligible mass and stiffness. Hence, the PZT patch can be regarded as an effective drive point. In addition, the impedance of the effective drive point is defined as the effective mechanical impedance.Figure 4
3D effective impedance model.The “effective mechanical impedance” of the PZT patch is defined as(2)Za,eff=∮Sf·n^dSu˙eff=Feffu˙eff,
where Feff is the effective force; n^ is the unit vector normal to the boundary; ueff=δV/Ao is defined as effective displacement of the PZT patch, where δV is the change in volume of the PZT patch; and Ao is the surface area of the PZT patch. Differentiation of the effective displacement with respect to time yields the effective velocity u˙eff. The “effective mechanical impedance” of the host structure can be defined based on applying the force on the surface of the host structure, along the boundary of the location of the embedded PZT patch.


## 3. Three-Dimensional Electromechanical Impedance Models

The existing impedance models are usually considered to be 1D or 2D models, and they neglect the longitudinal vibration of the PZT patch. Hence, there is a need for the development of a 3D PZT-structure interaction model that considers both the extensional and longitudinal vibrations of the PZT patch. By applying the concept of “effective mechanical impedance,” a 3D effective impedance model is proposed. The features of the proposed impedance model are that there are no restrictions of the PZT dimensions, and the model more accurately represents the actual situation.


### 3.1. 3D Electromechanical Admittance Formulation by the Effective Impedance

A circular PZT patch of radiusR and thickness 2h is shown in Figure 5. The polarization direction is along the Z axis, and the external exciting electric field EZ is also applied along the Z-direction and parallel to the polarization direction. Then, the vibration of the PZT patch can be regarded as a symmetrical vibration, and the shearing effect can be ignored. Owing to the symmetrical vibration, it is sufficient to use 1/8 of the PZT patch and host structure. Because of the mechanical and piezoelectric anisotropy of the PZT patch, the formulations S11E=1/YE¯, S12E=-ν12S11E=-ν12/YE¯, S13E=-ν13S11E=-ν13/YE¯, and S33E=ν33S11E=ν33/YE¯ are obtained. In cylindrical coordinates, the constitutive relations of the PZT patch are expressed as [18]
(3)Dz=ε33T¯Ez+d31(Trr+Tθθ)+d33Tzz,Srr=TrrYE¯-ν12TθθYE¯-ν13TzzYE¯+d31Ez,Sθθ=-ν12TrrYE¯+TθθYE¯-ν13TzzYE¯+d31Ez,Szz=-ν13TrrYE¯-ν13TθθYE¯+ν33TzzYE¯+d33Ez,
where Trr, Tθθ, and Tzz are, respectively, the radial, tangential, and axial stress; Srr, Sθθ, and Szz are, respectively, the radial, tangential, and axial strain; SijE is the elastic compliance constant in the short-circuited condition; YE¯ is the complex Young’s modulus of elasticity at a constant electric field; ν12, ν13, and ν33 are Poisson’s ratios; d31 and d33 are the piezoelectric strain coefficients; Ez is the electric field; Dz is the electric displacement; and ε33T¯ is the complex electric permittivity at a constant stress.(a) Geometry of the circular PZT patch and (b) stresses and displacements on the PZT patch.
(a)
(b)We letn=Tzz/(Trr+Tθθ). n is defined as the mechanical coupling coefficient between different vibrational modes [17]. By algebraic manipulation, we obtain
(4)Trr+Tθθ=YE¯λ[Srr+Sθθ+Szz-(2d31+d33)Ez],Tzz=nYE¯λ[Srr+Sθθ+Szz-(2d31+d33)Ez],
where λ=1-ν12-ν13+n(ν33-2ν13). Then, the effective force of the PZT-structure interaction is given by
(5)F=∮Sf·n^dS=(Trr+Tθθ)·2πRh4+TZZ·πR24=πR(2h+nR)4λ[Srr+Sθθ+Szz-(2d31+d33)EZ].
In the short-circuited condition, the effective force is expressed as
(6)Fshort-circuited=πR(2h+nR)YE¯4λ(Srr+Sθθ+Szz).As derived in [18, 19], the displacements of the PZT patch in cylindrical coordinates are provided by
(7)ur=A1J1(κ1r)ejωt,uθ=0,uz=A2sin(κ2z)ejωt,
where the wave number of the radial direction κ1=ω(2ρλ(1+ν12))/((1+ν12+λ)YE¯) and the wave number of the longitudinal direction κ2=ωρλ/nYE¯. A1 and A2 are constants determined by the boundary conditions. J1(x) is the Bessel function of the first kind and first order, and J1′(x)=J0(x)-(1/x)J1(x). By differentiating (7) with respect to time, the velocities are obtained as follows:
(8)u˙r=∂ur∂t=A1jωJ1(κ1x)ejωt,u˙θ=∂uθ∂t=0,u˙z=∂uz∂t=A2jωsin(κ2z)ejωt.
The strains are obtained by differentiating (7) with respect to the coordinate axes:
(9)Srr=∂ur∂r=A1[κ1J0(κ1r)-1rJ1(κ1r)]ejωt,Sθθ=urr=A1rJ1(κ1r)ejωt,Szz=∂uz∂z=A2κ2cos(κ2z)ejωt.Under the multimode vibration and free boundary conditions, the frequency equations for the PZT patch in a coupled vibration are obtained as follows:(10)cotκ2·2h=0κ1RJ0(κ1R)=(1-ν12)J1(κ1R).
Then, the following relations are obtained by solving (8) and (9):
(11)κ2·2h=(2m-1)π2,(m=1,2,3,…),κ1R=R(n),(n=1,2,3,…),
where R(n) is the root for (9), and it is a function of v12. By substituting κ1=ω(2ρλ(1+ν12))/((1+ν12+λ)YE¯), κ2=ωρλ/nYE¯, and λ=1-ν12-ν13+n(ν33-2ν13) and solving, n is obtained as follows:
(12)n=2-ν13(1+ν12)C′-(ν33-2ν13),
where C′=((2i-1)2π2)/(8R2(j))·(R2/h2).Based on the definition of the effective displacement in (1), the displacement at the boundaries of 1/8 of the PZT patch is expressed as
(13)ueff=δVAo≈2huro-Ruzo2h+R.
Differentiating with respect to time, the effective velocity is obtained:
(14)u˙eff≈2hu˙ro-Ru˙zo2h+R.To simplify the calculation, we assume that(15)uzoh=-ν13·uroR.
Substituting (7), the following formulations are derived:
(16)A1A2=-Rsin(κ2h)ν13hJ1(κ1R),A2A1=-ν13hJ1(κ1R)Rsin(κ2h).
Substituting (6), (8), (9), and (14) into (2), the effective impedance of the PZT patch is expressed as
(17)Za,eff=π(2h+R)(2h+nR)YE¯4λ(2+ν13)hjω·[κ1RJ0(κ1R)J1(κ1R)-ν13κ2htan(κ2h)].
The effective force F is related to the effective impedance of the host structure by
(18)F=∮Sf·n^dS=-Zs,eff·u˙eff.
By substituting (8), (9), and (18) into (2), with Ez=(Vo/2h)ejωt, the constants A1 and A2 are obtained:
(19)A1=(αRV0Za,eff)×(2h·J1(κ1R)[κ1RJ0(κ1R)J1(κ1R)-ν132h·J1(κ1R)×….·κ2htan(κ2h)](Zs,eff+Za,eff))-1,A2=(-ν13αV0Za,eff)×(2sin(κ2h)[κ1RJ0(κ1R)J1(κ1R)-ν13×.2sin.(κ2h.).·κ2htan(κ2h)](Zs,eff+Za,eff))-1.The instantaneous electric current is expressed as(20)I-=dQ(t)dt=∬AD˙ZdA=jω∬ADZ(Z=h)dA.
Substituting (4), (9), and (19) into (3), the electromechanical admittance of the 3D effective electromechanical impedance model is derived as
(21)Y¯=I¯V¯=G+Bj=πR2jω2h=×[×(Zs,eff+Za,eff)αβYE¯λ)-1αβYE¯λ)ε33T¯-αβYE¯λ==+(×(Zs,eff+Za,eff)[κ1RJ0(κ1R)J1(κ1R)-ν13·κ2htan(κ2h)]))-1(αβYE¯λ·(2-ν13·κ2htan(κ2h))·Za,eff)……..×([κ1RJ0(κ1R)J1(κ1R)-ν13·κ2htan(κ2h)]…..……×(Zs,eff+Za,eff)[κ1RJ0(κ1R)J1(κ1R)-ν13·κ2htan(κ2h)])-1)],
where α=2d31+d33 and β=d31+nd33; V¯=Voejωt is the instantaneous voltage across the PZT patch.This formulation containsZa,eff and the effective structural mechanical impedance Zs,eff. Za,eff  is constant for certain material parameters. The variations in Zs,eff caused by a change in the inherent properties of the host structure directly influence the electromechanical impedance. Hence, the variations in the inherent properties can be monitored by the measured electromechanical impedance.


### 3.2. Decomposition of the Coupled Electromechanical Admittance Signatures

In Section3.1, the complex electromechanical admittance of the proposed impedance model has been derived. By rearranging the various terms in (21), it can be separated into two parts as
(22)Y¯=πR2jω2h·[ε33T¯-αβYE¯λ]︸Part I+πR2jω2h·αβYE¯λ·(Za,effZs,eff+Za,eff)·T-︸Part II,
where T-=(2-ν13·(C2κ2h/tan(C2κ2h)))/[(C1κ1RJ0(C1κ1R)/J1(C1κ1R))-ν13·(C2κ2h/tan(C2κ2h))]. Part I only relates to the parameters of the PZT patch and is independent of the host structure. Part II represents the coupling between the PZT patch and the host structure. Hence, (22) is written as
(23)Y¯=YP¯+YA¯,
where YP¯ describes the PZT contribution that is insensitive to any structural changes; it is the “passive” part; YA¯ represents the contribution of the PZT-structure interaction and is sensitive to any structural changes near the PZT patch; it is the “active” part [20]. By substituting  YE¯=YE(1+ηj) and ε33T¯=ε33T(1-δj), YP¯ is expressed as
(24)YP¯=GP+BPj,
where
(25)GP=(πR)2fh(δε33T+αβYEλ·η),BP=(πR)2fh(ε33T-αβYEλ).The measured electrical admittance signals contain the “passive” and “active” parts. The existence of the “passive” part influences the sensitivity of the raw electrical admittance signals for SHM. Hence, if the PZT parameters are predicted, the “passive” part can be filtered out, and the “active” part can be derived from the raw electrical admittance signals:(26)Ga=G-GP,Ba=B-BP.
Substituting (25) and (26) into  (22), the complex form of the “active” part is expressed as
(27)YA¯=Ga+Baj=πR2jω2h·αβYE¯λ·Za,eff(Zs,eff+Za,eff)·T-.


## 3.1. 3D Electromechanical Admittance Formulation by the Effective Impedance

A circular PZT patch of radiusR and thickness 2h is shown in Figure 5. The polarization direction is along the Z axis, and the external exciting electric field EZ is also applied along the Z-direction and parallel to the polarization direction. Then, the vibration of the PZT patch can be regarded as a symmetrical vibration, and the shearing effect can be ignored. Owing to the symmetrical vibration, it is sufficient to use 1/8 of the PZT patch and host structure. Because of the mechanical and piezoelectric anisotropy of the PZT patch, the formulations S11E=1/YE¯, S12E=-ν12S11E=-ν12/YE¯, S13E=-ν13S11E=-ν13/YE¯, and S33E=ν33S11E=ν33/YE¯ are obtained. In cylindrical coordinates, the constitutive relations of the PZT patch are expressed as [18]
(3)Dz=ε33T¯Ez+d31(Trr+Tθθ)+d33Tzz,Srr=TrrYE¯-ν12TθθYE¯-ν13TzzYE¯+d31Ez,Sθθ=-ν12TrrYE¯+TθθYE¯-ν13TzzYE¯+d31Ez,Szz=-ν13TrrYE¯-ν13TθθYE¯+ν33TzzYE¯+d33Ez,
where Trr, Tθθ, and Tzz are, respectively, the radial, tangential, and axial stress; Srr, Sθθ, and Szz are, respectively, the radial, tangential, and axial strain; SijE is the elastic compliance constant in the short-circuited condition; YE¯ is the complex Young’s modulus of elasticity at a constant electric field; ν12, ν13, and ν33 are Poisson’s ratios; d31 and d33 are the piezoelectric strain coefficients; Ez is the electric field; Dz is the electric displacement; and ε33T¯ is the complex electric permittivity at a constant stress.(a) Geometry of the circular PZT patch and (b) stresses and displacements on the PZT patch.
(a)
(b)We letn=Tzz/(Trr+Tθθ). n is defined as the mechanical coupling coefficient between different vibrational modes [17]. By algebraic manipulation, we obtain
(4)Trr+Tθθ=YE¯λ[Srr+Sθθ+Szz-(2d31+d33)Ez],Tzz=nYE¯λ[Srr+Sθθ+Szz-(2d31+d33)Ez],
where λ=1-ν12-ν13+n(ν33-2ν13). Then, the effective force of the PZT-structure interaction is given by
(5)F=∮Sf·n^dS=(Trr+Tθθ)·2πRh4+TZZ·πR24=πR(2h+nR)4λ[Srr+Sθθ+Szz-(2d31+d33)EZ].
In the short-circuited condition, the effective force is expressed as
(6)Fshort-circuited=πR(2h+nR)YE¯4λ(Srr+Sθθ+Szz).As derived in [18, 19], the displacements of the PZT patch in cylindrical coordinates are provided by
(7)ur=A1J1(κ1r)ejωt,uθ=0,uz=A2sin(κ2z)ejωt,
where the wave number of the radial direction κ1=ω(2ρλ(1+ν12))/((1+ν12+λ)YE¯) and the wave number of the longitudinal direction κ2=ωρλ/nYE¯. A1 and A2 are constants determined by the boundary conditions. J1(x) is the Bessel function of the first kind and first order, and J1′(x)=J0(x)-(1/x)J1(x). By differentiating (7) with respect to time, the velocities are obtained as follows:
(8)u˙r=∂ur∂t=A1jωJ1(κ1x)ejωt,u˙θ=∂uθ∂t=0,u˙z=∂uz∂t=A2jωsin(κ2z)ejωt.
The strains are obtained by differentiating (7) with respect to the coordinate axes:
(9)Srr=∂ur∂r=A1[κ1J0(κ1r)-1rJ1(κ1r)]ejωt,Sθθ=urr=A1rJ1(κ1r)ejωt,Szz=∂uz∂z=A2κ2cos(κ2z)ejωt.Under the multimode vibration and free boundary conditions, the frequency equations for the PZT patch in a coupled vibration are obtained as follows:(10)cotκ2·2h=0κ1RJ0(κ1R)=(1-ν12)J1(κ1R).
Then, the following relations are obtained by solving (8) and (9):
(11)κ2·2h=(2m-1)π2,(m=1,2,3,…),κ1R=R(n),(n=1,2,3,…),
where R(n) is the root for (9), and it is a function of v12. By substituting κ1=ω(2ρλ(1+ν12))/((1+ν12+λ)YE¯), κ2=ωρλ/nYE¯, and λ=1-ν12-ν13+n(ν33-2ν13) and solving, n is obtained as follows:
(12)n=2-ν13(1+ν12)C′-(ν33-2ν13),
where C′=((2i-1)2π2)/(8R2(j))·(R2/h2).Based on the definition of the effective displacement in (1), the displacement at the boundaries of 1/8 of the PZT patch is expressed as
(13)ueff=δVAo≈2huro-Ruzo2h+R.
Differentiating with respect to time, the effective velocity is obtained:
(14)u˙eff≈2hu˙ro-Ru˙zo2h+R.To simplify the calculation, we assume that(15)uzoh=-ν13·uroR.
Substituting (7), the following formulations are derived:
(16)A1A2=-Rsin(κ2h)ν13hJ1(κ1R),A2A1=-ν13hJ1(κ1R)Rsin(κ2h).
Substituting (6), (8), (9), and (14) into (2), the effective impedance of the PZT patch is expressed as
(17)Za,eff=π(2h+R)(2h+nR)YE¯4λ(2+ν13)hjω·[κ1RJ0(κ1R)J1(κ1R)-ν13κ2htan(κ2h)].
The effective force F is related to the effective impedance of the host structure by
(18)F=∮Sf·n^dS=-Zs,eff·u˙eff.
By substituting (8), (9), and (18) into (2), with Ez=(Vo/2h)ejωt, the constants A1 and A2 are obtained:
(19)A1=(αRV0Za,eff)×(2h·J1(κ1R)[κ1RJ0(κ1R)J1(κ1R)-ν132h·J1(κ1R)×….·κ2htan(κ2h)](Zs,eff+Za,eff))-1,A2=(-ν13αV0Za,eff)×(2sin(κ2h)[κ1RJ0(κ1R)J1(κ1R)-ν13×.2sin.(κ2h.).·κ2htan(κ2h)](Zs,eff+Za,eff))-1.The instantaneous electric current is expressed as(20)I-=dQ(t)dt=∬AD˙ZdA=jω∬ADZ(Z=h)dA.
Substituting (4), (9), and (19) into (3), the electromechanical admittance of the 3D effective electromechanical impedance model is derived as
(21)Y¯=I¯V¯=G+Bj=πR2jω2h=×[×(Zs,eff+Za,eff)αβYE¯λ)-1αβYE¯λ)ε33T¯-αβYE¯λ==+(×(Zs,eff+Za,eff)[κ1RJ0(κ1R)J1(κ1R)-ν13·κ2htan(κ2h)]))-1(αβYE¯λ·(2-ν13·κ2htan(κ2h))·Za,eff)……..×([κ1RJ0(κ1R)J1(κ1R)-ν13·κ2htan(κ2h)]…..……×(Zs,eff+Za,eff)[κ1RJ0(κ1R)J1(κ1R)-ν13·κ2htan(κ2h)])-1)],
where α=2d31+d33 and β=d31+nd33; V¯=Voejωt is the instantaneous voltage across the PZT patch.This formulation containsZa,eff and the effective structural mechanical impedance Zs,eff. Za,eff  is constant for certain material parameters. The variations in Zs,eff caused by a change in the inherent properties of the host structure directly influence the electromechanical impedance. Hence, the variations in the inherent properties can be monitored by the measured electromechanical impedance.


## 3.2. Decomposition of the Coupled Electromechanical Admittance Signatures

In Section3.1, the complex electromechanical admittance of the proposed impedance model has been derived. By rearranging the various terms in (21), it can be separated into two parts as
(22)Y¯=πR2jω2h·[ε33T¯-αβYE¯λ]︸Part I+πR2jω2h·αβYE¯λ·(Za,effZs,eff+Za,eff)·T-︸Part II,
where T-=(2-ν13·(C2κ2h/tan(C2κ2h)))/[(C1κ1RJ0(C1κ1R)/J1(C1κ1R))-ν13·(C2κ2h/tan(C2κ2h))]. Part I only relates to the parameters of the PZT patch and is independent of the host structure. Part II represents the coupling between the PZT patch and the host structure. Hence, (22) is written as
(23)Y¯=YP¯+YA¯,
where YP¯ describes the PZT contribution that is insensitive to any structural changes; it is the “passive” part; YA¯ represents the contribution of the PZT-structure interaction and is sensitive to any structural changes near the PZT patch; it is the “active” part [20]. By substituting  YE¯=YE(1+ηj) and ε33T¯=ε33T(1-δj), YP¯ is expressed as
(24)YP¯=GP+BPj,
where
(25)GP=(πR)2fh(δε33T+αβYEλ·η),BP=(πR)2fh(ε33T-αβYEλ).The measured electrical admittance signals contain the “passive” and “active” parts. The existence of the “passive” part influences the sensitivity of the raw electrical admittance signals for SHM. Hence, if the PZT parameters are predicted, the “passive” part can be filtered out, and the “active” part can be derived from the raw electrical admittance signals:(26)Ga=G-GP,Ba=B-BP.
Substituting (25) and (26) into  (22), the complex form of the “active” part is expressed as
(27)YA¯=Ga+Baj=πR2jω2h·αβYE¯λ·Za,eff(Zs,eff+Za,eff)·T-.


## 4. Experimental Investigations

In this study, a concrete beam with an embedded PZT patch during the curing age was monitored to measure the strength gain. First, an Agilent4294A precision impedance analyzer was used for collecting the electric admittance signals. By a series of computational procedures, the “active” part associated with the mechanical impedance was derived from the raw electrical admittance signal. Finally, the “active” part was utilized to monitor the strength gain of the concrete beam during the curing age. The objective of this experiment was to demonstrate the feasibility and sensitivity of utilizing the “active” part by filtering out the PZT contribution for SHM.


### 4.1. Experimental Setup

In the experiment, a concrete beam with dimensions of10mm×10mm×50mm was used for the strength gain monitoring of concrete in the early age by the proposed approach. To measure the EMI signatures during the curing age, a PZT patch having a thin epoxy adhesive that can be regarded as a waterproof layer was embedded into the concrete structure. The diameter of the PZT patch was 20 mm, and the thickness was approximately 2 mm. The properties of the PZT patch are listed in Table 1. The experimental setup for collecting the electrical admittance signals is shown in Figure 6. The patch was wired to the Agilent4294A precision impedance analyzer. Then, the Agilent4294A precision impedance analyzer was connected to a computer via a GPIB interface.Table 1
Properties of the PZT patch.
Physical parameter
Value
Density,ρ (kg/m3)
7600
Young’s modulus,YE (N/m2)
7.75
×
10
10
Piezoelectric strain coefficient,d31 (m/V)
120
×
10
-
12
Piezoelectric strain coefficient,d33 (m/V)
280
×
10
-
12Figure 6
Experimental setup.By applying a high-frequency excitation voltage to the PZT patch with the Agilent4294A analyzer, the electromechanical admittance signature produced by the coupling vibration between the PZT patch and the host structure was measured in the frequency range of 20–200 kHz, including the real part (conductanceG) and the imaginary part (susceptance B). In the monitored frequency range, 801 data points were taken with a 1-V sweeping sine wave for the excitation. However, the measured signals are often contaminated by noise originating from the measurement system [21, 22]. To minimize the influence of noise, eight averages of the signatures were calculated per frequency point. The impedance signature at the age of 1 day was measured and defined as the baseline, and then subsequent tests were taken at the ages of 2, 3, 4, and 7 days. By analyzing the measured electrical admittance signatures, the strength gain of the concrete beam during the curing age can be monitored by the proposed approach.


### 4.2. Determination of the PZT Parameters

Owing to the influence of the production process and the high temperature in the welding process between the PZT and the wires, the properties of the PZT patches provided by the manufacturer are unreliable. In the EMI technique, the “active” part of the electrical admittance signals is predicted based on the PZT parameters. Hence, more accurate PZT parameters need to be derived before extracting the “active” part from the measured raw admittance signatures.For a PZT patch in the free-free condition prior to its embedding into the host structure, the complex electromechanical admittance is derived as (Zs,eff=0)
(28)Yfree¯=Gf+Bfj=πR2jω2h[ε33T¯+αβYE¯λ·(T-1)].
By substituting YE¯=YE(1+ηj),   ε33T¯=ε33T(1-δj),  T=M+N·j, [κ1R·J0(κ1R)]/J1(κ1R)=r+t·j, (κ2h)/tan(κ2h)=r′+t′·j, and ω=2πf, we obtain
(29)Gf=(πR)2fh[δε33T-αβYEλ{η(M-1)+N}],Bf=(πR)2fh[ε33T+αβYEλ{(M-1)-ηN}],
where
(30)M=(2-ν13r′)(r-ν13r′)-ν13t′(t-ν13t′)(r-ν13r′)2+(t-ν13t′)2,N=-(2-ν13r′)(t-ν13t′)+ν13t′(r-ν13r′)(r-ν13r′)2+(t-ν13t′)2.
Further, for low frequencies (typically <1/5 of the first resonance frequency of the PZT), [κ1R·J0(κ1R)]/J1(κ1R)=r+t·j→2 and (κ2h)/tan(κ2h)=r′+t′j→1 (i.e., r→2, t→0, r′→1, and t′→0); therefore, M→1, N→0 [13], and the quasistatic sensor approximation is expressed as [23]
(31)Gf,qs=(πR)2fh·δε33T,Bf,qs=(πR)2fh·ε33T.
Hence, the electrical constants ε33T and δ can be determined by the measured electric admittance signals Gf,qs and Bf,qs for low frequencies (typically <10 kHz). From this analysis, ε33T and δ were determined to be 1.4×10-8F/m and 0.0096, respectively.By using (29) with these PZT parameters, the electrical admittance signals of the PZT patch in the free-free condition in the frequency range of 20–220 kHz were obtained and compared with the measured free PZT signals (G,B) in Figure 7. Although the experimental and analytical free PZT signals have the good agreement in the figures, there are fundamental differences that warrant closer examination. For instance, the analytical resonance frequency is slightly higher than the experimental frequency.Comparison between the experimental and theoretical signals of the PZT patch in the free condition.
(a)
Conductance
(b)
SusceptanceIn order to achieve much better agreement between the analytical and experimental signatures, the correction factorsC1 and C2 are introduced in the terms [κ1R·J0(κ1R)]/J1(κ1R) and (κ2h)/tan(κ2h), and these terms may be replaced by [C1κ1R·J0(C1κ1R)]/J1(C1κ1R) and (C2κ2h)/tan(C2κ2h), respectively. By trial and error, the values of the correction factor were C1=1.023 and C2=0.98. Hence, very good agreement is observed between the analytical and experimental signatures. Using curve-fitting techniques, it was found that η=0.021 and K=(αβYE)/λ=7.63×10-9NV-2. From these PZT parameters, the “active” part associated with the structural mechanical impedance by filtering the PZT contribution can be extracted from the measured raw admittance signatures.


### 4.3. Results and Analysis

As mentioned above, the PZT parameters can be accurately predicted by the measured admittance signatures of the PZT patches in the “free-free” condition. Hence, the “passive” part (PZT contribution) is filtered out, and the “active” part associated with the structural mechanical impedance can be extracted from the measured raw admittance signatures. The spectra are shown in Figure7. With an increase in the curing time for the concrete specimen, the amplitudes of the Ga and Ba curves gradually diminished, and the curves shifted to the right. This indicates that the “active” part is sensitive to changes in the inherent properties of a concrete beam with embedded PZT transducers during the curing age.Figure8 depicts the variations of the “active” part curve, but the extent of the changes in the inherent properties cannot be directly determined. In other words, the spectra of the “active” part only qualitatively represent the strength gain of the concrete beam during the curing age. Although the spectra are qualitatively useful, they lack any quantitative accuracy. Traditionally, statistical pattern recognition techniques have been employed to quantify the changes in the admittance signatures, such as relative deviation, root-mean-square deviation, and mean-absolute-percentage deviation [24]. In order to quantitatively analyze the strength gain for the concrete beam during the curing age, two statistical indices are defined as follows.“Active” part extracted from the measured raw admittance signatures.
(a)
Conductance
(b)
Susceptance(
1
) Root-mean-square deviation (RMSD)
(32)RMSD(%)=∑i=1N(yi-yi¯)2∑i=1Nyi¯2×100.(
2
) Correlation coefficient (CC)
(33)CC=(yiT·yi¯)2|yiT·yi|·|y¯iT·y¯i|,
where yi and yiT separately denote the vector and its transpose for the “active” part of the electrical admittance (Ga and Ba) for curing times of 2, 3, 4, 5, and 7 days; and yi¯ and yi¯T separately denote the vector and its transpose for the “active” part of the electrical admittance for a curing time of 1 day.Figure9 shows the plots of the RMSD and CC indices for the “active” part and the measured raw admittance signatures, which are calculated at various stages during the curing age with respect to the baseline signature. From Figure 8, we find that the RMSD index increased and the CC index decreased during the curing age for the concrete beam. These indexes qualitatively represent the variations in the inherent properties of the interior of the concrete beam.Comparison between the “active” part and the measured raw admittance signatures.
(a)
G
a and G
(b)
B
a and BThe existing EMI techniques only depend on the real part of the measured electrical signatures, but the information in the imaginary part is lost. By eliminating the “passive” part, the admittance signatures are more sensitive to any structural changes than the raw signatures. By comparing the “active” part and the measured raw admittance signatures, the indices of the real part are similar, whereas the indices of the imaginary part have a large difference. Further, the indices of the imaginary component are similar to the indices of the real component in the “active” admittance signatures. This indicates that utilization of the imaginary component for damage identification is feasible. The experimental results demonstrate that the “active” part of the admittance signatures is more sensitive than the raw admittance signatures for SHM. Furthermore, the imaginary component can also be used for SHM.


## 4.1. Experimental Setup

In the experiment, a concrete beam with dimensions of10mm×10mm×50mm was used for the strength gain monitoring of concrete in the early age by the proposed approach. To measure the EMI signatures during the curing age, a PZT patch having a thin epoxy adhesive that can be regarded as a waterproof layer was embedded into the concrete structure. The diameter of the PZT patch was 20 mm, and the thickness was approximately 2 mm. The properties of the PZT patch are listed in Table 1. The experimental setup for collecting the electrical admittance signals is shown in Figure 6. The patch was wired to the Agilent4294A precision impedance analyzer. Then, the Agilent4294A precision impedance analyzer was connected to a computer via a GPIB interface.Table 1
Properties of the PZT patch.
Physical parameter
Value
Density,ρ (kg/m3)
7600
Young’s modulus,YE (N/m2)
7.75
×
10
10
Piezoelectric strain coefficient,d31 (m/V)
120
×
10
-
12
Piezoelectric strain coefficient,d33 (m/V)
280
×
10
-
12Figure 6
Experimental setup.By applying a high-frequency excitation voltage to the PZT patch with the Agilent4294A analyzer, the electromechanical admittance signature produced by the coupling vibration between the PZT patch and the host structure was measured in the frequency range of 20–200 kHz, including the real part (conductanceG) and the imaginary part (susceptance B). In the monitored frequency range, 801 data points were taken with a 1-V sweeping sine wave for the excitation. However, the measured signals are often contaminated by noise originating from the measurement system [21, 22]. To minimize the influence of noise, eight averages of the signatures were calculated per frequency point. The impedance signature at the age of 1 day was measured and defined as the baseline, and then subsequent tests were taken at the ages of 2, 3, 4, and 7 days. By analyzing the measured electrical admittance signatures, the strength gain of the concrete beam during the curing age can be monitored by the proposed approach.


## 4.2. Determination of the PZT Parameters

Owing to the influence of the production process and the high temperature in the welding process between the PZT and the wires, the properties of the PZT patches provided by the manufacturer are unreliable. In the EMI technique, the “active” part of the electrical admittance signals is predicted based on the PZT parameters. Hence, more accurate PZT parameters need to be derived before extracting the “active” part from the measured raw admittance signatures.For a PZT patch in the free-free condition prior to its embedding into the host structure, the complex electromechanical admittance is derived as (Zs,eff=0)
(28)Yfree¯=Gf+Bfj=πR2jω2h[ε33T¯+αβYE¯λ·(T-1)].
By substituting YE¯=YE(1+ηj),   ε33T¯=ε33T(1-δj),  T=M+N·j, [κ1R·J0(κ1R)]/J1(κ1R)=r+t·j, (κ2h)/tan(κ2h)=r′+t′·j, and ω=2πf, we obtain
(29)Gf=(πR)2fh[δε33T-αβYEλ{η(M-1)+N}],Bf=(πR)2fh[ε33T+αβYEλ{(M-1)-ηN}],
where
(30)M=(2-ν13r′)(r-ν13r′)-ν13t′(t-ν13t′)(r-ν13r′)2+(t-ν13t′)2,N=-(2-ν13r′)(t-ν13t′)+ν13t′(r-ν13r′)(r-ν13r′)2+(t-ν13t′)2.
Further, for low frequencies (typically <1/5 of the first resonance frequency of the PZT), [κ1R·J0(κ1R)]/J1(κ1R)=r+t·j→2 and (κ2h)/tan(κ2h)=r′+t′j→1 (i.e., r→2, t→0, r′→1, and t′→0); therefore, M→1, N→0 [13], and the quasistatic sensor approximation is expressed as [23]
(31)Gf,qs=(πR)2fh·δε33T,Bf,qs=(πR)2fh·ε33T.
Hence, the electrical constants ε33T and δ can be determined by the measured electric admittance signals Gf,qs and Bf,qs for low frequencies (typically <10 kHz). From this analysis, ε33T and δ were determined to be 1.4×10-8F/m and 0.0096, respectively.By using (29) with these PZT parameters, the electrical admittance signals of the PZT patch in the free-free condition in the frequency range of 20–220 kHz were obtained and compared with the measured free PZT signals (G,B) in Figure 7. Although the experimental and analytical free PZT signals have the good agreement in the figures, there are fundamental differences that warrant closer examination. For instance, the analytical resonance frequency is slightly higher than the experimental frequency.Comparison between the experimental and theoretical signals of the PZT patch in the free condition.
(a)
Conductance
(b)
SusceptanceIn order to achieve much better agreement between the analytical and experimental signatures, the correction factorsC1 and C2 are introduced in the terms [κ1R·J0(κ1R)]/J1(κ1R) and (κ2h)/tan(κ2h), and these terms may be replaced by [C1κ1R·J0(C1κ1R)]/J1(C1κ1R) and (C2κ2h)/tan(C2κ2h), respectively. By trial and error, the values of the correction factor were C1=1.023 and C2=0.98. Hence, very good agreement is observed between the analytical and experimental signatures. Using curve-fitting techniques, it was found that η=0.021 and K=(αβYE)/λ=7.63×10-9NV-2. From these PZT parameters, the “active” part associated with the structural mechanical impedance by filtering the PZT contribution can be extracted from the measured raw admittance signatures.


## 4.3. Results and Analysis

As mentioned above, the PZT parameters can be accurately predicted by the measured admittance signatures of the PZT patches in the “free-free” condition. Hence, the “passive” part (PZT contribution) is filtered out, and the “active” part associated with the structural mechanical impedance can be extracted from the measured raw admittance signatures. The spectra are shown in Figure7. With an increase in the curing time for the concrete specimen, the amplitudes of the Ga and Ba curves gradually diminished, and the curves shifted to the right. This indicates that the “active” part is sensitive to changes in the inherent properties of a concrete beam with embedded PZT transducers during the curing age.Figure8 depicts the variations of the “active” part curve, but the extent of the changes in the inherent properties cannot be directly determined. In other words, the spectra of the “active” part only qualitatively represent the strength gain of the concrete beam during the curing age. Although the spectra are qualitatively useful, they lack any quantitative accuracy. Traditionally, statistical pattern recognition techniques have been employed to quantify the changes in the admittance signatures, such as relative deviation, root-mean-square deviation, and mean-absolute-percentage deviation [24]. In order to quantitatively analyze the strength gain for the concrete beam during the curing age, two statistical indices are defined as follows.“Active” part extracted from the measured raw admittance signatures.
(a)
Conductance
(b)
Susceptance(
1
) Root-mean-square deviation (RMSD)
(32)RMSD(%)=∑i=1N(yi-yi¯)2∑i=1Nyi¯2×100.(
2
) Correlation coefficient (CC)
(33)CC=(yiT·yi¯)2|yiT·yi|·|y¯iT·y¯i|,
where yi and yiT separately denote the vector and its transpose for the “active” part of the electrical admittance (Ga and Ba) for curing times of 2, 3, 4, 5, and 7 days; and yi¯ and yi¯T separately denote the vector and its transpose for the “active” part of the electrical admittance for a curing time of 1 day.Figure9 shows the plots of the RMSD and CC indices for the “active” part and the measured raw admittance signatures, which are calculated at various stages during the curing age with respect to the baseline signature. From Figure 8, we find that the RMSD index increased and the CC index decreased during the curing age for the concrete beam. These indexes qualitatively represent the variations in the inherent properties of the interior of the concrete beam.Comparison between the “active” part and the measured raw admittance signatures.
(a)
G
a and G
(b)
B
a and BThe existing EMI techniques only depend on the real part of the measured electrical signatures, but the information in the imaginary part is lost. By eliminating the “passive” part, the admittance signatures are more sensitive to any structural changes than the raw signatures. By comparing the “active” part and the measured raw admittance signatures, the indices of the real part are similar, whereas the indices of the imaginary part have a large difference. Further, the indices of the imaginary component are similar to the indices of the real component in the “active” admittance signatures. This indicates that utilization of the imaginary component for damage identification is feasible. The experimental results demonstrate that the “active” part of the admittance signatures is more sensitive than the raw admittance signatures for SHM. Furthermore, the imaginary component can also be used for SHM.


## 5. Conclusions

In this paper, a three-dimensional effective electromechanical impedance model for an embedded PZT transducer is proposed. Based on the concept of effective impedance, the 3D coupled electromechanical admittance equation is derived. By rearranging the various terms, the admittance equation is separated into an “active” part and a “passive” part. Because the “active” part is sensitive to any structural changes near the PZT patch, it is feasible to use the “active” part for SHM. Then, the proposed method is used to monitor the strength gain of a concrete beam with embedded PZT transducers during the curing age. The results show that the “active” part of the admittance signatures is more sensitive to any structural damage than the raw admittance signatures, which demonstrates the validity of the proposed method.



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*Source: 218026-2013-12-31.xml*