Effects of Elevated Temperature on Guided-Wave
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StructuresJournal of Intelligent Material Systems and
http://jim.sagepub.com/content/19/12/1383The online version of this article can be found at:
DOI: 10.1177/1045389X07086691
2008 19: 1383 originally published online 20 May 2008Journal of Intelligent Material Systems and StructuresAjay Raghavan and Carlos E.S. Cesnik
Effects of Elevated Temperature on Guided-wave Structural Health Monitoring
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Effects of Elevated Temperature on Guided-waveStructural Health Monitoring
AJAY RAGHAVAN AND CARLOS E. S. CESNIK*
Department of Aerospace Engineering, The University of Michigan, 1320 Beal AvenueAnn Arbor, Michigan 48109, USA
ABSTRACT: Elevated temperatures can cause significant changes in guided-wave (GW)propagation and transduction for structural health monitoring (SHM). This work focuses onGW SHM using surface-bonded piezoelectric wafer transducers in metallic plates for thetemperature range encountered in internal spacecraft structures (201508C). First, studiesdone to determine a suitable bonding agent are documented. This is then used in controlledexperiments to examine changes in GW propagation and transduction using PZT-5Apiezoelectric wafers under quasi-statically varying temperature (also from 20 to 1508C).Modeling efforts to explain the experimentally observed increase in time-of-flight and changein sensor response peak-to-peak magnitude with increasing temperature are detailed.Finally, these results are used in detection and location of mild and moderate damage usingthe pulse-echo GW testing approach within the temperature range.
Key Words: structural health monitoring, damage prognosis, guided waves, Lamb waves,
thermal variation, temperature compensation, spacecraft structures, integrated systems health
management, bonding agent.
INTRODUCTION
Motivation
IN 2005, a new vision was defined for NASA, and it
has already set in motion plans for returning
astronauts to the Moon, and eventually, longer-term
missions to Mars. In this endeavor, integrated systemshealth management (ISHM) will play a key role in
fulfilling the mission objectives. ISHM will help in
transitioning from low-earth orbit missions with con-
tinuous ground support to more autonomous long-term
missions (Carlos et al., 2005). The ISHM system will
manage all the critical spacecraft functions and systems.
It will include monitoring capability composed of
sensors and actuators plus a reasoning system that can
evaluate the hardwares functionality. The structural
health monitoring (SHM) subsystem will be a crucial
component of the ISHM system. It will apprize
astronauts on changes in vehicle structural integrity
requiring action as well as providing the crew with thecapability to forecast potential problems and schedule
repairs based on the rate of loss of system function and
condition of hardware.
Fundamentals of Guided-wave Approaches
Among various technologies under investigation for
SHM, there are guided-wave (GW)-based approaches
These essentially involve exciting the structure with
high frequency GWs and processing the difference in
structural response with respect to a baseline signal for
the pristine condition using a tested algorithm to detectdamage and characterize it, if present. Guided waves can
be defined as stress waves forced to follow a path
defined by the material boundaries of the structure
For example, when a beam is excited at high frequency
stress waves travel in the beam along its axis away from
the excitation source, i.e., the beam guides the waves
along its axis. While several transducers have been
tested, piezoelectric wafer transducers (hereafter referred
to as piezos) seem to be the most commonly used
option. This is largely because of the low mass and space
penalty associated with incorporating them (crucial in
aerospace structures) and their high energy density for
high frequency applications. There are two mainapproaches commonly used in GW SHM, pulse-echo
and pitch-catch. In the former, typically after exciting
the structure with a pulse, a sensor (usually immediately
adjacent to the actuator) is used to detect scattered
echoes of the pulse coming from discontinuities. Since
the boundaries and the wavespeed for a given cente
actuation frequency of the toneburst are known*Author to whom correspondence should be addressed.E-mail: [email protected] 16 and 823 appear in color online: http://jim.sagepub.com
JOURNAL OF INTELLIGENT MATERIAL SYSTEMS AND STRUCTURES, Vol. 19December 2008 1383
1045-389X/08/12 138316 $10.00/0 DOI: 10.1177/1045389X07086691 SAGE Publications 2008
Los Angeles, London, New Delhi and Singapore
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the signals from the boundaries can be filtered out
(assuming a narrow enough time-span excitation pulse is
used; alternatively one could subtract the test signal
from the baseline signal). One is then left with signals
generated from the damage sites (if present). From these
signals, damage sites can be located using the known
wavespeed. One potential caveat of this approach isthat there are small areas in the immediate vicinity of
the actuator and structural features (e.g., stiffeners) with
decreased sensitivity for the actuatorsensor pair. The
actual size of these areas decreases with decreasing
time-span of the excitation pulse. This results from the
difficulty in distinguishing between minor differences in
the actuation signal/reflections from structural features
(e.g., caused by small temperature changes) and reflec-
tions caused by structural damage.
In the pitch-catch approach, a pulse signal is usually
sent across the specimen under interrogation and a
sensor at the other end of the specimen receives the
signal (in plate-like structures this is often implementedusing a network of such paths to cover the structure).
From various characteristics of the received signal, such
as delay in time-of-flight, amplitude, frequency content,
etc., information about the damage (if present) can be
obtained. Thus, the pitch-catch approach cannot be
used to locate the defect unless a dense network of
transducers is used. Issues with both approaches in the
face of changing temperature will be discussed later in
this study. A detailed survey of GW SHM, including
fundamentals and early history, is presented in a review
paper by the authors (Raghavan and Cesnik, 2007c). As
pointed out there, while GW SHM has shown a good
deal of promise in various laboratory demonstrations,several issues remain to be resolved before they see
widespread field deployment in structures. Among these,
compensation for environmental and service conditions
is a crucial one.
Spacecraft Structures and Their Environment
Typical spacecraft structures are composed of different
substructures, each of which can act as waveguides,
thereby making them attractive application areas for GW
SHM. This is also true of the planned NASAs crew
exploration vehicle (CEV). The CEV is expected to have
an aluminum alloy internal structure in the shape ofa blunt body capsule protected by bulk insulation,
composite skin panels, and a thermal protection system
(TPS), see Stanley et al. (2005). Spacecraft structures
in particular present a challenging application due to
the harsh environment of outer space as well as the
tremendous heat flux and high temperatures attained
during re-entry into a planets atmosphere. While fiber
optic sensors can be designed to withstand these harsh
re-entry temperatures, they are passive and cannot be
used to excite GWs. Some authors have examined SHM
in spacecraft structures using fiber optic sensor networks
by passive strain/loads monitoring (e.g., Friebele et al.,
1999; Ecke et al., 2001). However, such passive
approaches require a much denser network of sensors
than GW approaches. The internal spacecraft structures,
however, are somewhat insulated by the TPS. The TPS is
typically designed to keep temperatures below 1508C ininternal structures, particularly in manned missions
(Myers et al., 2000). Apart from the re-entry phase,
even in the course of the flight, the temperature of
spacecraft structures varies significantly, with tempera-
tures up to 708C (Larson and Wertz, 1995) depending on
whether they face towards or away from the Sun. For
solar arrays, this fluctuation is even greater (up to 1008C,
see Larson and Wertz, 1995). Another source of
temperature variation in internal spacecraft structures is
the heat radiated by cabin electronics, which is difficult to
reject into space, and is therefore controlled by active
cooling. Commercial piezos are functional without loss in
properties up to half their Curie temperature. For leadzirconium titanate, or PZT 5A (a.k.a. DoD Type II), one
of the more commonly used piezoceramics, half the Curie
limit is about 1758C. Thus, internal spacecraft structures
become a potential application area for GW SHM using
PZT-5A piezos. Some studies have examined GW SHM
for cryogenic tanks (Blaise and Chang, 2001; Lin et al.,
2003) and thermal protection systems (Yang et al., 2003;
Derriso et al., 2004; Huang et al., 2005) in spacecraft
structures. However, the experiments/simulations in
these studies were restricted to room temperature
(except in Blaise and Chang, 2001). The GW SHM
algorithm must account for temperature changes to
minimize false damage indications and reduce errors indamage characterization during the course of space
missions. The present study explores this very issue.
Previous Efforts on Effects of Temperature for GW SHM
There have been some efforts to address the issue of
varying temperature for GW SHM in the literature.
Blaise and Chang (2001) investigated the performance
of piezoelectric transducers (in GW pitch-catch config-
uration) embedded into sandwich structures for cryo-
genic fuel tanks at low temperatures (up to 908C).
An empirical model (linear) was fitted to experimentally
obtained data points for changing signal peak-to-peakmagnitude and time-of-flight. Reasonable agreement
between the interpolated signals from the empirical
model and experimental data for intermediate tempera-
ture values was obtained. However, no damage detec-
tion studies were reported by them. Lee et al. (2003)
studied the effect of temperature variation on the Lamb-
wave response of a piezoceramic sensor in a pitch-catch
configuration on a metallic plate from room tempera-
ture up to 708C. They observed that the effect of
temperature variation over this range (analyzed using
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principal component analysis) was much more
pronounced than the effect of damage (drilled 1-mm
diameter hole). Lu and Michaels (2005) and
Konstantinidis et al. (2006) examined GW SHM under
mild thermal variations from 20 to 408C. Both addressed
modeling the varying time-of-flight in this temperature
range due to changing substrate elastic modulus andthermal expansion, and good agreement with experi-
ments in this temperature range was observed. Lu and
Michaels (2005) also suggested using a bank of baseline
signals for various temperatures and picking a baseline
signal which minimizes difference relative to the test
signal for that particular temperature. Chambers et al.
(2006) suggested test procedures for environmental
robustness certification of GW SHM transducers in
aircraft structures. Schulz et al. (2003) studied the
performance of PZT-5A patches as free vibration
sensors bonded using various adhesives on aluminum
beams up to 2408C. A drop of 74% in strain response
amplitude (relative to room temperature value) wasobserved at 1508C, and the response dropped to zero at
2408C. They also explored alternative materials for high
temperature applications, and identified lithium niobate
and nanotubes as potential transducer materials for
future high temperature applications (up to 10008C).
However, these have much weaker piezoelectric proper-
ties at room temperatures compared to PZT. Results
from preliminary thermal experiments were also
reported by the authors (Raghavan and Cesnik,
2005a). These tests examined sensor response variation
in pitch-catch tests done using PZT-5A piezos bonded
on a 1-mm thick aluminum plate up to 1508C. It was
observed that the sensor response decreased continu-ously with increasing temperature and went to the noise
floor beyond 1108C. It was suspected that this decrease
was due to bonding agent degradation.
Objectives of this Study
It is evident from the literature reviewed that the
issues of compensation for and damage characterization
under thermal variations expected in GW SHM for
spacecraft structures (above room temperature) have
not received much attention. This study aims to
contribute in these aspects. First, studies done to find
a suitable bonding agent (for GW SHM using piezo-ceramics on aluminum plates) that does not degrade
under thermal variations from 20 to 1508C are reported.
With a suitable bonding agent chosen, controlled
experiments are done to examine changes in GW
propagation and transduction using PZT-5A piezos
under quasi-statically varying temperature (also from
20 to 1508C). All parameters changing with temperature
are identified and quantified based on data from
the literature. Modeling efforts exploiting these data
to explain the experimental results are outlined.
Finally, these results are used to explore detection
and location of damage (indentations/holes) using the
pulse-echo GW testing approach in the same tempera
ture range.
BONDING AGENT SELECTION
Bonding Agents Tested and Specimen Preparation
After an initial pre-screening, three different two-par
epoxies were evaluated for the temperature range o
interest. These were 10-3004 (Epoxies, Etc., 2006), and
Epotek 301 and 353ND (Epoxy Technology, 2006)
Epotek 301 and 353ND, both low-viscosity agents, are
rated for continuous operation up to 200 and 2508C
respectively. 10-3004 is relatively viscous, and is rated
for continuous operation up to 1258C, although the
manufacturer clarified that it should work up to 1508C
for short-term use (hours). In addition, it was confirmedfrom the manufacturers that each epoxy would be
suitable for surface-bonding piezoceramics (with metal-
lic electrodes) on aluminum plates. While 10-3004 and
301 can be cured overnight at room temperature
353ND needs to be cured in an oven at 808C fo
25 min. Standard surface preparation procedures were
followed with each, i.e., the plate surface was made
rough by light sanding, and both the plate and piezos
were cleaned thoroughly using acetone to get rid of
grease and dust. After uniformly applying a thin-layer
film of epoxy to both surfaces and cleaning the excess
light pressure was applied using small weights (2 lb.) to
the interface to help the bond set.
Experimental Tests with Epotek 301 and
Epoxies, Etc. 10-3004
The first aluminum alloy (5005) plate specimen
(40350.32cm3) tested had four PZT-5A piezo
that were surface-bonded using Epotek 301 (Figure 1)
Two piezos were used as actuators (dimensions
2.51.50.03 cm3, at the center, on either surface)
and two as sensors (dimensions 1 10.03 cm3). One o
the sensors (Sensor 1) was immediately adjacent to the
actuator, and the other (Sensor 2) was 10 cm away from
the plate center. This specimen was thermally cycledfrom 20 to 1508C in an industrial oven and then cooled
back to room temperature over three cycles. A Labview
based automated thermal test setup was developed for
these experiments. After turning the oven on, at every
108C intervals (read by a type-K thermocouple with
18C accuracy attached to one side of the plate
specimen), the Labview program triggered an Agilen
33220A function generator to send a 3.5-cycle Hanning-
windowed toneburst, with center frequency 210 kHz to
the actuators (excited symmetrically), 16 times each
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at 1-s intervals. A Hewlett Packard 54831B Infiniium
oscilloscope recorded the sensor response signals, which
were sampled at 10 MHz and averaged over the 16
readings at each temperature. In these tests, it was
observed that the sensor response signal of Sensor 2decreased monotonically in peak-to-peak magnitude
with increasing temperature (Figure 2). The error bars
shown are based on the standard deviation over the 16
readings at each temperature. Furthermore, Sensor 2s
response signal peak-to-peak magnitude at room tem-
perature decreased at the end of each cycle, and the
shape of the signal also changed significantly, as shown
in Figure 3. It should be noted that the sensor response
was compensated for varying actuation signal magni-
tude (which dropped due to the increasing capacitance
of the actuators with temperature). While some amountof irrecoverable loss in response strength is expected
after the first few cycles, due to thermal pre-stabilization
of piezos (Berlincourt et al., 2007), the signal shape is
not expected to change. Despite the actuators being
excited symmetrically, and thereby only supposedly
exciting the S0 mode, experimental imperfections cause
weak A0 mode excitation. To counter this, the sensor
was originally designed (Raghavan and Cesnik, 2005b)
to be very weakly sensitive to the A0 mode (the sensor
size equaled the A0 mode wavelength at 210 kHz).
However, after each cycle, the strength of the slower A0mode contribution at 208C in the Sensor 2 signal
increased. This suggested that the sensors effectivearea kept decreasing after each cycle. Based on these
factors, it was concluded that the Epotek 301 bond line
was indeed degrading as a result of the thermal cycling.
An analogous test was done with PZT-5A transducers
bonded using 10-3004 on an aluminum alloy (5005)
plate. In this case, the results were even more drastic and
the sensor response dropped gradually to the noise floor
at 1008C while heating in the very first cycle, and never
recovered.
Experimental Tests with Epotek 353ND
Finally, tests were done with Epotek 353ND.The specimen tested (also an aluminum 5005 specimen
of size 4035 0.32 cm3) was similar to the ones tested
above. The schematic of this is shown in Figure 4. It had
two 2 10.03 cm3 piezos surface-bonded on either face
of the plate at the center which were used as actuators.
Three surface-bonded 1 10.03cm3 piezos were used
as sensors, of which one was immediately adjacent to one
of the actuators and two were at a distance of 10.2 cm
from the plate center. The specimen was thermally cycled
in the same temperature range seven times in the oven,
35cm PZT-5A actuators2.5cm x 1.5cm
10 cm
3.2 mm
PZT-5ASensor 2
PZT-5ASensor 1
1 cm x 1 cm1 cm x 1 cm
Aluminum 5005 plate
Type K thermocouple
0.3 mm
40 cm
Supportblocks
Figure 1. Schematic of specimen for tests with Epotek 301.
2 4 6 8 10
x105
0.12
0.1
0.08
0.06
0.04
0.02
0
0.02
0.04
0.06
Time (s)
Sensor
2signal(V)
Before thermal expts.
After thermal cycle 1
After thermal cycle 2
After thermal cycle 3
EMI
S0mode A0mode
Boundaryreflections
Figure 3. Sensor 2 signal at room temperature before and aftereach of the three thermal cycles for tests with Epotek 301 (thesignals are offset by a small DC voltage for clarity; EMI electromag-netic interference from the actuation).
0
0.05
0.1
0.15
0.2
0 20 40 60 80 100 120 140
Sensor
2peak-to-peakmagnitude(V) 1st cycle heating 1st cycle cooling
2nd cycle heating 2nd cycle cooling
3rd cycle heating 3rd cycle cooling
Temperature (deg C)
Noise floor
Figure 2. Variation of Sensor 2 response magnitude (peak-to-peak) and associated error bars with temperature over three thermalcycles (for tests with Epotek 301).
1386 A. RAGHAVAN AND C. E. S. CESNIK
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using the same experimental setup and settings described
above. In this case, the sensor response peak-to-peak
magnitude and shapes did not change (within negligible
error margins, see Figure 5) when the signals before and
after each thermal cycle are compared. The very firstcycle was an exception, being the thermal pre-stabiliza-
tion cycle discussed before, which caused a 17% drop in
Sensors 2 and 3 response peak-to-peak magnitude (but
the signal shape did not change after the cycle). Thus, this
epoxy proved to be suitable for the purposes of this study.
Thereafter, more controlled tests were conducted with
this same specimen to study signal changes for pristine
specimens and to explore damage characterization
at different temperatures, which is discussed in the
following sections.
EFFECTS OF ELEVATED TEMPERATURE
FOR PRISTINE SPECIMEN: EXPERIMENTS
AND MODELING
Experimental Setup and Results
In designing the specimen for tests with Epotek
353ND, Sensor 1 was collocated with the actuator
with the intention of using it for damage detection using
pulse-echo tests. Sensors 2 and 3 were for tracking
changes in the GW transmitted signal with temperature
(in undamaged state). In addition, Sensors 2 and 3
also act as mild GW scatterers, due to the increased
local stiffness and mass caused by their presence
This simulates the effect of some structural feature
(e.g., rivets) which could act as GW scatterers in morecomplex structures. While the specimen was tested in the
industrial oven initially to check for bond degradation
the ovens heating/cooling rate could not be tightly
controlled, and was very rapid (up to 108C/min) a
times. This fast heating rate led to non-repeatable
signals for Sensor 1, which could potentially be
interpreted as false positives. This is discussed in the
next section. More controlled tests were subsequently
done in a computer-controlled autoclave (Figure 6)
where both the heating and cooling rates were set to
18C/min. A 5-min dwell period at 1508C was also
included in the thermal cycle between the heating and
cooling phases (Figure 7). The data at 90 and 1008Cwhile cooling was not used, since in this temperature
range, the autoclave switches from exclusively air
cooling to a combination of air and water cooling
leading to oscillations in the cooling rate over this range
For these tests, the center frequency was reduced to
120 kHz. This was to minimize actuation signal distor
tion effects at higher frequencies caused by increasing
actuator capacitance at higher temperatures. While
a Krohn-Hite 7500 wideband amplifier was tried for a
couple of thermal cycles in the oven, it was unable to
35cm
Piezo actuators2 cm x 1 cm10.2
cm
3.2 mm
Aluminum 5005 plate
Sensor 31 cm x 1 cm
Thermocouple
Damage location
8 cm
0.3 mm
Sensor 2
1 cm x 1 cm
40 cm Supportblocks
1 cm x 1 cmSensor1
Figure 4. Schematic of specimen for tests with Epotek 353ND.(Damage introduced and discussed later.).
0 1
x104
0.05
0.04
0.03
0.02
0.01
0
0.01
0.02
0.03
0.04
0.05
Sensor2response(V)
Before thermal cycleAfter thermal cycle
S0 mode
Boundary reflections
Mild A0mode
Electromagneticinterference
Time (s)
0.2 0.4 0.6 0.8
Figure 5. GW signal sensed by Sensor 2 (bonded using Epotek3 53 ND ) bef or e a nd a fte r a th er m al c yc l e: th e dif f ic ul ty in distinguishing between the two signals is indicative of therepeatability of signals after the thermal cycle.
Autoclave
Plate specimenand cable stand
TC
Oscilloscope
Labview system
Function generator
Data acquisition for TC
Figure 6. Labeled photograph of setup and autoclave for controlledthermal experiments (TC thermocouple).
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amplify without significant signal distortion and ripple
at higher temperatures. Therefore, no amplifier was usedfor the controlled tests in the autoclave. The actuation
signal was still a 3.5-cycle Hanning windowed toneburst
of 18 V peak-to-peak magnitude at 208C, with the two
actuators on either surface excited symmetrically. At
every 108C intervals, the LABVIEW setup triggered the
function generator to send this actuation signal to the
function generator 30 times with 1-s gaps between each
trigger. The 1-s gap between each excitation ensures that
the GWs from the previous excitation have died out and
do not interfere with the GWs from the next excitation
burst. The oscilloscope in turn is triggered by a square
wave pulse from the function generator through a
separate synchronization channel coinciding with thebeginning of each excitation burst. This ensures that
the start of the actuation pulse is set as time zero for
the signal in the oscilloscope. The oscilloscope stores the
signals from the piezos, averaged over the 30 signals
from the multiple excitation bursts to reduce signal noise
levels, along with the standard deviation in peak-to-peak
magnitude. During this 30-s period over which signal
averaging is done, the autoclave continues heating/
cooling at 18C/min, meaning the specimen temperature
varies by up to 0.58C. However, this temperature
variation is within the accuracy of the thermocouple
(18C). It is also representative of situations encoun-
tered in practical applications: one can seldom expectthe structure to remain at perfect thermal equilibrium
for on-the-field applications. Data were collected over
two thermal cycles for the pristine, undamaged condi-
tion. As mentioned before, as temperature increases, due
to increasing actuator capacitance, there is an increase in
the electrical load seen by the function generator.
Therefore, due to the lack of an amplifier, there was a
drop in actuation peak-to-peak magnitude from 18 V at
208C to %13V at 1508C (but negligible shape distor-
tion). All signals presented for higher temperatures in
this study have been scaled for 18-V peak-to-peakactuation level (by multiplying the sensor signals with
the ratio of 18V to the actuation peak-to-peak
magnitude at the corresponding temperature).
Figure 8 shows the GW signal read by Sensor 2 at
various temperatures while heating. Evidently, there is a
decrease in GW speed of the first transmitted GW pulse
as temperature increases. In addition, the signal peak-
to-peak magnitude increases with increasing tempera-
ture up to a certain point (around 908C) and then
decreases with increasing temperature. Hysteresis effects
were found to be negligible (unlike in the oven tests,
where significant hysteresis was observed between the
heating and cooling phases due to very differenttemperature change rates in the two phases).
Identification and Quantification of Thermally
Sensitive Parameters
In order to explain these effects, an effort was made to
identify all parameters in the experiment that change
with temperature. The following list was compiled and
data for their thermal variation were found from various
sources in the literature:
1. Youngs moduli of structural substrate and PZT-5A:
The substrate elastic modulus is probably the mostimportant parameter for thermal variations. There is
a significant decrease in the elastic modulus of
aluminum with increasing temperature. This causes
a reduction in GW speeds, as reflected in the change
in dispersion curves. Furthermore, in quantifying
thermal variations of elastic modulus, two different
data sets were found: one for the variation in static
elastic modulus (U.S. Munitions Board Aircraft
Committee, 1955), and the other for dynamic elastic
modulus (Lord and Orkney, 2000). These data are
0 2 4 6 8 10
x 105
0.06
0.04
0.02
0
0.02
0.04
Sensor2response(V)
20C90C (heating)150C
Time (s)
Figure 8. GW signals recorded by Sensor 2 (averaged over30 signals for each temperature) at various temperatures whileheating (offset by a small DC voltage for clarity).
0 1 2 3 4 50
50
100
150
Tempera
ture(C)
Time (h)
Figure 7. Typical timetemperature curve for experiments done inthe computer-controlled autoclave.
1388 A. RAGHAVAN AND C. E. S. CESNIK
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shown in Figure 9. The former was obtained from
standard stressstrain tests conducted under varying
temperature for aluminum alloy 7075, while the latter
was found from measuring changes in natural
frequency of aluminum beam (alloy 5052) flexural
vibrations with temperature. No data were found foraluminum 5005, the material used in the tests here.
However, it is similar in composition to the two
alloys for which data were found. The variation in
elastic modulus of PZT-5A is relatively small
(Williams et al., 2004). No data were obtained for
dynamic elastic modulus variation of PZT-5A.
2. Piezoelectric properties of PZT-5A: It is well-known
that the piezoelectric constants (d31 and g31) vary
significantly with temperature (Berlincourt et al.,
2007). For GW SHM, the variation in the product
d31 g31 is of relevance (the d31 constant is associated
with actuation shear stress induced, while the g31
constant is associated with the piezo-sensor sensitiv-ity), and this can vary by as much as 7%, as shown
in Figure 10. In addition, the dielectric constant of
PZT-5A increases linearly with temperature, which
causes the load seen by the function generator to
increase. This however, does not affect sensor
response by itself.
3. Thermal expansion: This is a relatively mild effect,
and causes the plate thickness, piezo dimensions, and
distances traveled by the GWs in the plate to
increase, while material density decreases. Since the
thermal expansion coefficients of aluminum and
PZT-5A are known (average values over 20 to
1508C are 25.5mm/m-8C for aluminum obtainedfrom Matweb (2007); 1 2.5mm/m-8C for PZT-5A,
see Williams et al., 2004), these effects can be
accounted for. The effect of changing (static) elastic
modulus, plate thickness, and density were used to
compute Lamb-wave phase velocity dispersion curves
at different temperatures (Figure 11). The dispersion
curves at equally spaced temperatures are unequally
spaced, particularly at the higher temperatures. This
is because of the nonlinear change in Youngs
modulus and density with temperature.
4. Damping and pyroelectric effects (not considered)
Another parameter that changes with increasing
temperature is damping in the structural substrate
The best reference found in this regard (Hilton and
Vail, 1993) estimated an increase by a factor of 4 in
the loss modulus (representative of damping) a
100 Hz in aluminum alloy 2024. This still ensure
that the loss modulus is orders of magnitude lower
than the elastic modulus and can be neglected, as was
verified at room temperature in a previous work
(Raghavan and Cesnik, 2005b). Therefore, damping
was ignored at higher temperatures too. Finally, due
to the pyroelectric effect, temperature changes causea static voltage to appear across a piezos electrodes
Since the experimental signals were acquired with a
2 Hz high-pass filter built into the oscilloscope, thi
effect was not considered either.
Theoretical Modeling and Signal Analysis
Effects (a)(c) were incorporated into the theoretica
models developed by the authors (Raghavan and
Cesnik, 2005b). These models can capture the
1540
1560
1580
1600
1620
1640
1660
1680
0 20 40 60 80 100 120 140 160
PZT-
5Ad31xg31
(C-V/m-sqN)
Temperature (C)
Figure 10. Variation of d31g31 of PZT-5A (Berlincourt et al., 2007)
0
1000
2000
3000
4000
5000
6000
0 100 200 300 400 500
Phasevelocity(m/s
)
S0 at 20C
A0 at 150C
A0 at 80C
Frequency (kHz)
A0 at 20C
S0 at 150C
S0 at 80C
Figure 11. Combined effect of changing aluminum elastic modulus(static) and thermal expansion on phase velocity.
58
60
62
64
66
68
70
0 20 40 60 80 100 120 140 160
Youngsmodulus(GPa)
Al staticAl dynamicPZT-5A
Temperature (C)
Figure 9. Variation of Youngs moduli (ANC-5 1955; Lord andOrkney, 2000; Williams et al., 2004).
Effects of Elevated Temperature on Guided-wave SHM 1389
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three-dimensional GW field excited and sensed by
arbitrarily shaped, surface-bonded finite-dimensional
piezos in isotropic plates. The models assume uncoupled
dynamics and the piezo-actuator is modeled as causing
surface shear traction along its edge in the direction
normal to the edge on the surface of the underlying
substrate. More recently, extensions of these modelsto other structural configurations (isotropic beams,
hollow cylinders, and composite plates) have also been
proposed (Raghavan and Cesnik, 2007a,b). These
models have been validated extensively by numerical
and experimental results. The inputs for these models
are the material properties, dimensions of the structure,
the piezo dimensions, the piezo-actuators shear
traction magnitude, and piezo-sensors piezoelectric
constant and Youngs modulus, all of which are
thermally sensitive parameters as explained above.
Reduced transducer dimensions were used to generate
the theoretical plots. A 20% reduction in transducer size
over nominal values was assumed based on an earlierwork to correlate frequency response plots from
experiments with theoretical predictions for piezos of
the same thickness on similar aluminum plates
(Raghavan and Cesnik, 2005b). This is to account for
shear lag, which causes strain transfer to happen over a
small area close to the actuator edge, and not exactly
the actuator edge, as assumed in the pin-force model.
In addition, variations in the traction magnitude exerted
by the piezo due to changing elastic moduli and
dimensions were accounted for using the equation for
static actuation by piezos in Chaudhry and Rogers
(1994). These models were used to generate theoretical
predictions for the time-domain sensor response signalsat various temperatures between 20 and 1508C for the
configuration used in the experiments, incorporating
data for the thermal variation of the model inputs. With
that, it was examined whether the experimentally
observed increase in time-of-flight of the GW S0 mode
wave-packet received by Sensor 2 and the change in
sensor response peak-to-peak magnitude could be
captured. Spectrograms of these signals were generated
(for both the theoretical and experimental ones) and
the time-of-flight of the first transmitted S0 pulse was
computed from them. This also allowed examining to
see whether there was a change in the center frequency
of this pulse with temperature. The time-of-flight hereis defined as the time corresponding to the peak in the
first wave pulse (from the spectrogram) minus half
the excitation pulse span (corresponding to the peak of
the excitation), as shown in Figure 12. It was calculated
with a resolution of the experimental sampling rate, i.e.,
0.1ms. The comparison between theory and experiment
is shown in Figure 13 for time-of-flight and in Figure 14
for sensor response magnitude (peak-to-peak). To get
an estimate of the error in time-of-flight, the raw
un-averaged 30 signals were collected for two points
per thermal cycle (1008C while heating and 708C while
cooling). The data from Sensor 3 is very similar.
Discussion of Results and Implications for GW SHM
The theoretical estimates for time-of-flight are in
agreement with the experimental data (within error
(a)
(b)
(c)
10
0
10
0.05
200
150
100
0
0.05
Actuation
signal(V)
Sensor
signal(V)
Frequency
(kHz)
Time (s)
10
2
x104
x104
0.2 0.4
Time of flight
0.6 0.8
10.2 0.4 0.6 0.8
x10410.2 0.4 0.6 0.8
Figure 12. Extraction of time-of-flight at 908C while heating: (a)actuation signal; (b) Sensor 2 response signal; and (c) spectrogramof signal in (b).
0.02
0.04
0.06
0.08
0.1
0.12
0 20 40 60 80 100 120 140 160
Cycle 1 heating
Cycle 1 cooling
Cycle 2 heating
Cycle 2 cooling
Theoretical (static modulus variation)
Temperature (C)
Sensor2responsepeak-to-peakmagnitude
Figure 14. Variation in response magnitude (peak-to-peak) of firsttransmitted S0 mode received by Sensor 2.
19.5
20
20.5
21
21.5
22
0 20 40 60 80 100 120 140 160
Time-of-flight(s)
Exper imental (cycle 1 heat ing) Exper imental (cycle 1 cool ing)
Exper imental (cycle 2 heat ing) Exper imental (cycle 2 cool ing)
Theoretical (static elastic modulus) Theoretical (dynamic elastic modulus)
Temperature (C)
Figure 13. Variation in time-of-flight of first transmitted S0 modereceived by Sensor 2.
1390 A. RAGHAVAN AND C. E. S. CESNIK
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margins) and the agreement seems better for the
theoretical data set generated assuming static elastic
modulus variation. The center frequency was calculated
with a resolution of 3 kHz, which is limited by the time
span of the signal recorded. With this resolution, the
center frequency of the sensed S0 mode pulse remained
constant at 133 kHz for both the theoretical andexperimental data sets at different temperatures. For
the sensor response magnitude prediction, there is
clearly a significant gap between the theoretical estimate
and experimental data. The experimentally observed
increase of up to 33% while heating to 908C in the
response magnitude of Sensor 2 is not captured by the
theoretical model, but the decrease of 18% at 1508C is
predicted within the error margin. One possible expla-
nation for this is changing bond layer properties with
temperature (the model used here assumed perfect
bonding). Data were unavailable for variation of bond
layer elastic modulus with temperature and therefore it
could not be quantified. However, the static modulusvariation and thermal expansion data can be used to
give a good approximation to account for the slowing
down of wavespeeds with increasing temperature, and
is used in the subsequent section to generate damage
location estimates. An empirical compensation
approach is used for varying response magnitude.
From these experiments, it is clear that temperature
can cause significant changes in the magnitude and
time-of-flight for the first transmitted pulse received by
the sensor. Even with the instantaneous temperature
known, this causes greater error margins in the
magnitude and time-of-flight measurement under
slightly varying temperature. In most pitch-catchapproaches used, changes in these very features are
used to conclude whether damage is present in the
actuatorsensor path or not. It should be clarified that
in this context, pitch-catch approaches refer to those
that use a dense network of transducers and rely on
changes in the GW signal transmitted over the direct
actuatorsensor paths. Therefore, the pitch-catch
method is inherently more sensitive to false positives in
damage detection under varying temperature. On the
other hand, pulse-echo approaches typically rely on the
absence or presence of reflected or scattered echoes
between the actuation/first transmitted pulse and the
boundary reflection (although some researchers do useechoes arriving after the first boundary reflection).
If damage is present, regardless of temperature increase,
there will always be some GW reflection/scattering and
a sensor adjacent to the actuator or elsewhere should be
able to pick this up (assuming the damage is sensitive
to the mode and frequency of the incident GW).
Therefore, in principle, the only modification to make
for GW pulse-echo based damage characterization
under varying temperature would be to account for
varying GW speeds and scale the reflection magnitude
according to the changed sensor sensitivity at tha
particular temperature. However, complications arise
for pulse-echo methods in structures with features, such
as rivets in trying to detect and locate mild damage
which is roughly at the same distance (within a few cm
from the actuator as the rivet. In this context, damage is
called mild if the magnitude of the reflected GW by it iscomparable to that of the reflection from the rivet
structural discontinuity. This is explored experimentally
in the next section.
DAMAGE CHARACTERIZATION UNDER
VARYING TEMPERATURE
Baseline Signals and Threshold Values
As mentioned in the previous section, before any
damage was introduced two data sets were obtained for
the baseline, pristine condition of the specimen (whichhad transducers bonded with Epotek 353ND) from two
identical thermal cycles on different days. This was to
get a sense of the repeatability of the baseline condition
for a given temperature between the two cycles. The
baseline signal read by Sensor 1 (collocated with the
actuator) is shown in Figure 15. There is some non-zero
signal between the actuation pulse and the boundary
reflection due to mild A0 mode excitation and some
reflection from Sensors 2 and 3. At 208C, the A0 mode
reflection from Sensors 2 and 3 is discernible, while the
S0 mode reflection is negligible. However, at highe
temperatures, the S0 mode reflection from Sensors 2
and 3 becomes stronger (e.g., see Figure 15)Furthermore, there is some error in the magnitudes o
these mild reflections received at Sensor 1 when data
from the two cycles are compared. Figure 16 shows one
of the worse scenarios in this regard, while Figure 17 is
an example of better repeatability observed among
2 4 6 8 10
x 105
0.1
0.05
0
0.05
0.1
Time (s)
Sensor1respo
nse(V)
20C120C (heating)
S0mode actuation
Boundary reflections
Undesired A0
mode actuation
A0
reflectionfrom s2 and s3
S0
reflection
from s2 and s3
Figure 15. Signal read by Sensor 1 at 20 and 1108C (Cycle 1) fopristine condition.
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the readings. This error in repeatability arises from the
variation in time-of-flight and sensor response magni-tude under changing temperature. As mentioned earlier,
there is a 18C error in the temperature read by the
thermocouples and the autoclave continues heating/
cooling at 18C/min during the 30-s period of data
collection for each temperature reading. With large
temperature-change rates, this problem is further
exacerbated. This explains why poor signal repeatability
was observed in the initial experiments in the oven. The
variation between the two baseline cycles defines the
threshold values for the subsequent damage detection
experiments. In practice, it would be advisable to get
some more data for the variability in baseline condition
at various temperatures, particularly in less homoge-neous structural layouts with rivets, stiffeners, etc. In
addition, while data were collected here at 108C
intervals, it can also be used for baseline interpolation
at intermediate temperatures. This can be done by
simple weighted averaging of the two signals taken at
the multiples of 108C within which the intermediate
temperature lies (see Figure 18). Of course, this is
possible because in this case, the variation between
signals at 108C intervals is not significant enough
to cause destructive interference between them
when averaged. However, if the piezo is used to monitorlarger structures or using higher frequencies, the spacing
between reflections from structural features may
increase in the time domain and destructive interference
might become a possibility with weighted averaging. In
such cases, readings can be taken at more closely spaced
temperature intervals to overcome this issue.
Once the two sets of baseline signals were recorded,
threshold energy levels were obtained from them.
The threshold energy in this context is defined as the
peak signal energy obtained from the spectrogram of the
difference signal between the two baselines (scaled for
18V actuation as well as to match the peak-to-peak
magnitude of the first S0 actuation pulse between thetwo) at the same temperature. The threshold energy is
chosen to be the peak value from the spectrogram in the
time window between the end of the S0 mode actuation
signal seen at Sensor 1 and the beginning of the
boundary reflections (illustrated in Figure 16 and
Figure 17). As explained in the authors previous work
(Raghavan and Cesnik, 2007d), some kind of time
frequency analysis is essential for GW signals because
they allow for distinguishing among the different GW
modes possible and also enable tracking the change in
the center frequency of the scattered GW pulse (since
damage may be more sensitive to frequencies other than
the center frequency of the incident GW pulse). This cansignificantly affect the speed of the scattered pulse,
which can contribute to location estimate errors.
Indentation Damage
Subsequently, damage was introduced artificially in
the plate by drilling. As alluded to at the end of an
earlier section, the case of mild damage was first
explored. To ensure that the reflections were not too
strong, damage was introduced along the axis of weaker
0 2 4 6 8 10
105
0.15
0.1
0.05
0
0.05
0.1
0.15
Sensor1r
esponse(V)
90C85C (Interpolated)80C
Time (s)
Figure 18. Illustration of interpolated signal (at 858C) obtained byweighted averaging of recorded signals at 80 and 908C (slightlyoffset by a constant value for clarity) from pristine specimen whileheating during Cycle 1.
Sensor1
response(V)
Frequency
(kHz)
0.05
160
140
12010080
60
2 4 6
Time (s)
Cycle 1 (pristine)Cycle 2 (pristine)Difference
8
8 x 103
6
4
2
10
2 4 6 8 10
x 105
x 105
180
0.05
0
Thresholdenergyvalue
Time-frequencywindow forthresholdenergy
Figure 17. Sensor 1 response during Cycles 1 and 2 for pristinecondition along with the difference signal and its spectrogram at 608Cwhile cooling (signals offset by a small DC voltage for clarity).
Sensor1
response(V)
Frequency
(kHz)
0.05
0.05
0
150
50
100
2 4 6 8 10
0.15
Cycle 1 (pristine)Cycle 2 (pristine)Difference
0.05
0
0.1
x 105
2 4 6
Time (s)
8 10
x 105
Time-
frequencywindow forthresholdenergy
Thresholdenergyvalue
Figure 16. Sensor 1 response during Cycles 1 and 2 for pristinecondition along with the difference signal and its spectrogram at1208C while heating (signals offset by a small DC voltage for clarity).
1392 A. RAGHAVAN AND C. E. S. CESNIK
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actuation of the rectangular actuators. Theoretical
models developed earlier by the authors (Raghavan
and Cesnik, 2005b) predicted a 30% weaker GW strain
field along this direction. Experiments were first donefor a triangular cross-sectional indentation of maximum
diameter 5 mm and depth 1.7 mm (Figure 19(a)). The
damage center is 8 cm away from the plate center and its
location is shown in Figure 4. The signal obtained from
Sensor 1 at room temperature after introducing this
damage is shown in Figure 20, along with the pristine
condition signal and the difference between the two.
As a well-established practice in the GW SHM commu-
nity, this difference signal is used for damage detection
and characterization. There are clear reflections in the
difference signal whose peak energies from the spectro-
gram are well above the energy threshold defined for
208C. The two distinct reflections in the signal are theS0- and A0-mode reflections from the indentation.
As explained in the authors earlier work (Raghavan
and Cesnik, 2007d), even though the S0 mode is
predominantly excited, mode conversion is possible at
a defect. In this case, because of the controlled
introduction of damage in the specimen, the A0 and S0mode reflections were expected and their time-of-flight
values could be estimated. However, in field applica-
tions, one has to blindly infer all information from the
GW signals. Therefore, for practical situations, one has
to be able to identify the GW mode of each reflection as
well. This can be done from the reflections character-
istics in the timefrequency plane. For the A0 mode,since higher frequencies travel much faster than the
lower ones, the peaks at higher frequencies within the A0mode reflection arrive faster than those for the lower
ones in the timefrequency plane. On the other hand,
for the S0 mode the converse is true, but the variation in
S0 mode wavespeeds is milder over the frequency range
and structure used in these experiments. Once the mode
is identified, the group speed(s) corresponding to the
frequency at which the peak within the reflection occurs
is used with the time-of-flight for estimating the radial
location of the damage site (see Raghavan and Cesnik
2007d). As mentioned in an earlier section, the group
speeds for a particular temperature are computed by
accounting for the Youngs modulus at that temperatureand thermal expansion in the dispersion curves. In this
case, the GW packet originates from one edge of the
actuator and its echo travels back all the way to the
other edge and has to further traverse a distance equal to
half the sensor dimension before the peak of the
reflected GW is seen in the sensor response. Therefore
minor correction terms to account for the transi
times of the GW packet through the transducers are
subtracted from these estimates. At 208C, the radia
location estimates of the indentation are 7.2 and 8.2 cm
(from the plate center) based on the S0 and A0 mode
reflections, respectively. The analysis done in thi
study was done by manually tracking the reflections inthe spectrograms. In principle, the chirplet matching
pursuit algorithm used earlier by the authors (Raghavan
and Cesnik, 2007d) should allow automated tracking
and better resolution for real-time processing in
end applications. However, its implementation in
LastWave 2.0 (Bacry, 2007) makes approximations to
reduce computational complexity which do no
capture the slowing down of wavespeeds at elevated
temperatures seen in Figure 13.
The indented specimen was thermally cycled in the
autoclave to check whether the difference signa
remained above the pre-defined threshold level at each
temperature point. Some of the signals read by Sensor 1during this experiment are shown in Figure 20 and
Figure 21. The results are also summarized in Table 1
The A0 and S0 mode reflections from the indentation
had peak energy (from the spectrogram, in the excited
frequency band as shown in Figure 20 for the signal at
208C) well above the threshold up to 808C while heating
Some of the S0 mode reflections (from 50 to 808C) mixed
with the excitation difference signal, due to which the
S0 mode reflection underestimated the damage location
(shown in Figure 21). Beyond 808C, the A0 mode
(a) (b)
Figure 19. Photographs of damage introduced: (a) indentation and(b) through-hole.
Sensor1
response(V)
Frequency
(kHz)
0.05
0
2 4 6 8 10
2 4 6
Time (s)
PristineIndentation
Difference
8 10
0.2
0.1
0
x 105
x 105
0.05
180
160140
120
100
80
60
S0
modereflection
A0
modereflection
Figure 20. Sensor 1 response at 208C for pristine and indented specimens, along with the difference signal (offset by smaDC values for clarity) and its spectrogram.
Effects of Elevated Temperature on Guided-wave SHM 1393
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Table
1.
Summaryo
fresu
lts
show
ing
trends
in
thermalexperimentfordamage
cha
racterization
with
indented
specimen
(Key:
Temp.
Temperature;
(h)
heating
phase;
(c)
cooling
phase;
S0
ToF
time-o
f-flightfor
S0
mode
reflection
from
indentation;
S0
loc.
est.
radiallocatione
stimate(relativetoplatecenter)ofdamagebasedonS
0
modereflectio
n).
Temp.
(8C)
S0
ToF(ks)
S0
energy(V2)
Threshold
energy(V2)
S0
above
threshold?
S0
loc.est.
(cm)
A0
ToF(ks)
A0
energy(V2)
A0
above
threshold?
A0loc.est.(cm)
20
(h)
28.1
0
0.0
631
0.0
142
Yes
7.2
50.6
5
0.2
8825
Yes
8.2
40
(h)
28.0
0
0.1
229
0.0
025
Yes
7.2
51.2
0
0.3
695
Yes
8.6
70
(h)
18.6
0
0.0
739
0.0
154
Yes
4.7
54.6
0
0.5
895
Yes
9.1
110
(h)
31.2
0
0.1
808
0.1
850
No
7.9
56.0
0
0.1
959
Yes
9.2
130
(h)
18.6
0
0.0
66
0.0
517
Yes
4.5
34.1
0
0.0
886
Yes
4.9
150
0.0
275
25.5
0
0.0
839
Yes
4.0
120
(c)
0.0
375
28.6
0
0.1
363
Yes
4.1
80
(c)
25.5
0
0.2
688
0.0
525
Yes
6.5
56.8
0
0.1
502
Yes
9.5
50
(c)
27.5
0
0.0
681
0.0
033
Yes
7.1
55.8
2
0.2
240
Yes
9.4
20
(c)
30.3
5
0.0
483
0.0
023
Yes
7.8
53.9
5
0.4
228
Yes
8.8
1394 A. RAGHAVAN AND C. E. S. CESNIK
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reflection was still above the threshold, but had peakenergy that was comparable to the threshold. The
weaker S0 mode reflection had peak energy lower than
the threshold at some points after 908C while heating.
In addition, as illustrated in Figure 21, at some points
over 1008C, there is a reflection that arrives approxi-
mately where the S0 mode was seen at lower tempera-
tures, but can be wrongly identified as A0 mode by its
timefrequency characteristics. This results in much
larger errors for the radial location estimate.
Subsequently, while cooling below 808C, again both
reflections were well above the threshold, and gave
reasonable location estimates.
Through-hole Damage
Following this, a through hole of diameter 7.5 mm
was drilled at the same location (Figure 19(b)). The
response of Sensor 1 recorded after drilling through at
208C is shown in Figure 22. As seen in the difference
signal, the S0 mode reflection is now much stronger
while the A0 mode reflection appears much weaker
(but still well above the threshold at 208C). The radial
location estimates are 8.6 and 8.3 cm based on the S0 and
A0 mode reflections, respectively at 208C. The results
from thermally cycling the specimen with the through-
hole are shown in Figures 22 and 23 and tabulated inTable 2. In this case, the S0 mode reflection is reasonably
above the threshold at all temperatures. There is an
error of 1.9 cm in the estimate (based on the S0 mode) at
1508C, where the signal is the weakest. At a couple of
points, the radial location of the damage is over-
estimated by more than 1 cm (1008C while heating and
508C while cooling), which is possibly due to the mixing
of the S0 mode with the difference in the reflection from
Sensors 2 and 3. At other temperatures, the radial
location estimates based on the S0 mode are within 1 cm.
The A0 mode reflection, which was weak at 208C to
begin with, is discernible up to 708C while heating, bu
beyond that is indistinguishable from the difference in
boundary reflection until the specimen cools back to
room temperature.
DISCUSSION
Thus, for mild damage up to 808C, detection was no
problematic, but there was a slightly increased error in
location as temperature increased. However, beyond
that temperature, there is a definite decrease in
sensitivity, as reflected in the poorer detection
characterization capability in the indentation experi
ment. This can be attributed to the higher sensitivity
of the substrate elastic modulus to temperature
at higher temperatures (Figure 9), causing greater
variation in the mild reflections from Sensors 2 and 3
2 4 6 8 10
(a)
Pristine
Indentation
Difference
1 2 3 4 5 6 7 8 9 10 11
x 105
x 10
5
0.1
0.05
0
0.05
0.1
0.1
0.05
0
0.05
0.1
Pristine
Indentation
Difference
Sensor1
response(V)
S0
reflection mixed with excitation
A0
reflection
Sensor1
response(V)
A0
reflectionnegligible
Time (s)
(b)S0
reflection appearslike A
0mode in t-f ane
Figure 21. Sensor 1 response for pristine and indented specimens,along with the difference signal (offset by small DC values for clarity)at (a) 608C during heating and (b) 1508C.
0.1
0.05
0
0.05
2 4 6 8 10
0
(b)
PristineHoleDifference
PristineHoleDifference
0.05
0.05
0.1
x 105
2 4 6 8 10
(a) x 105
Figure 23. Sensor 1 response during heating for pristine andthrough-hole specimens, along with the difference signal (offset bysmall DC values for clarity) at: (a) 70 and (b) 1408C.
Sensor1
response(V)
Frequency
(kHz)
0.05
0.05
0
S0
modereflection
A0
modereflection
Pristine
Hole
Difference
Time (s)
280
100
120
140
160
4 6 8 100
0.05
0.1
0.15
0.2
2 4 6 8 10
x 105
x 105
Figure 22. Sensor 1 response at 208C for pristine and through-hole specimens, along with the difference signal (offset by smaDC values for clarity) and its spectrogram.
Effects of Elevated Temperature on Guided-wave SHM 1395
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Table2.
Summaryofresu
ltsshow
ingtrendsinthermalexperiment
fordamagecharacterizationusings
pecimenw
iththrough-h
ole(Key:
Te
mp.
Temperature;
(h)
heatingphase;
(c)
coolingphase;
S0
ToF
time-o
f-flightfo
rS
0
modereflectionfrom
thru-h
ole;
S0
loc.
est.
radiallocationestima
te(relativetoplate
center)ofdamagebasedonS
0
modereflection;
Bndry
A0
mode
reflectionpeakw
ithinboundaryreflection).
Temp.
(8C)
S0
ToF(ks)
S
0
energy(V2)
Threshold
energy(V2)
S0
above
threshold?
S0
loc.est.(cm)
A0
ToF
(ks)
A0
energy(V2)
A0
above
threshold?
A0
loc.est.(cm)
20
(h)
33.4
5
0.2
198
0.0
142
Y
es
8.6
49.7
5
0.0
763
Yes
8.3
40
(h)
34.3
0
0.2
972
0.0
025
Y
es
8.8
55.2
0
0.1
119
Yes
9.0
70
(h)
32.5
0
0.2
463
0.0
154
Y
es
8.3
56.7
0
0.2
128
Yes
9.0
110
(h)
40.6
0
0.2
578
0.1
850
Y
es
10.2
Bnd
ry
130
(h)
33.4
0
0.3
105
0.0
517
Y
es
8.2
Bnd
ry
150
25.6
0
0.1
073
0.0
275
Y
es
6.1
Bnd
ry
120
(c)
31.0
0
0.1
997
0.0
375
Y
es
7.6
Bnd
ry
80
(c)
28.0
0
0.2
985
0.0
525
Y
es
7.0
Bnd
ry
50
(c)
36.2
0
0.3
393
0.0
033
Y
es
9.3
Bnd
ry
20
(c)
33.8
0
0.2
018
0.0
023
Y
es
8.7
53.6
0
0.0
623
Yes
8.8
1396 A. RAGHAVAN AND C. E. S. CESNIK
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and consequently, poorer repeatability of the
baseline signals. In addition, the sensor sensitivity
(in terms of signal magnitude) drops below the value
at 208C beyond 1308C (as seen in Figure 14). For the
through-hole, which can be termed moderate damage,
detection was clearly possible at all temperatures, but
at a few points (3 of a total of 29 cases), there wasinaccuracy in the location estimate (by up to 2.2 cm for
damage located at 8 cm), partly due to interference with
the difference in reflection from Sensors 2 and 3
(simulating structural features in field applications).
One way to reduce the error in location is to use higher
center frequencies and/or fewer number of cycles (which
increases frequency bandwidth) in the actuation signal.
However, that was not feasible in the present setup
(which did not use amplifiers), since significant distor-
tion was observed for such actuation signals at higher
temperatures due to increasing actuator capacitance.
In addition, in the present experimental setup, the
scaling of the signals to compensate for changingactuation level increased the signal-to-noise ratio at
higher temperatures. This indicates the need for reliable
actuation signal amplification for actuating piezos at
elevated temperatures.
SUMMARY AND CONCLUSIONS
This study addressed the issue of GW SHM using
piezos under thermal variations as expected in spacecraft
internal structures. Experiments were done to determine
a bonding agent (for piezos on aluminum plates) that
did not degrade under thermal variations from 20 to1508C. Using this bonding agent (Epotek 353ND),
results from controlled experiments done to examine
changes in GW propagation and transduction using
PZT-5A piezos under quasi-statically varying tempera-
ture (also from 20 to 1508C) were presented. Thermally
sensitive variables in the experiments were identified and
quantified to model the experimentally observed
changes under temperature variation. The Youngs
modulus of the structure was the most critical of these
parameters. The increase in time-of-flight of GW pulses
with increasing temperature was captured by the model
(within the error margins). However, there was a
significant gap in the prediction of the large increase insensor response magnitude up to 1008C. The stronger
vulnerability of pitch-catch approaches (that detect
damage in the direct actuatorsensor path based on
changes in the first pulse transmitted over this path) to
false positives under changing temperature was then
explained. Finally, detection and location of damage
(by drilling) using the pulse-echo GW testing approach
in the presence of mild structural GW scatterers
(to simulate rivets) was explored in the same tempera-
ture range. Damage characterization of a half-plate
thickness indentation at 8 cm from the actuators was no
significantly affected up to 808C, but beyond tha
temperature, detection/characterization was difficult
The problems beyond 808C can be traced to increased
sensitivity of substrate elastic modulus to temperature
and weaker sensor sensitivity beyond 1308C. For a
through-hole, damage detection and characterizationwas possible at all temperatures and, except at a few
temperatures (3 out of 29), damage was located within
1 cm for a nominal location of 8 cm and, hole diamete
0.75cm. Suggested approaches for improving the
sensitivity at higher temperatures include testing a
higher frequencies and/or with shorter time-span
excitation pulses, with reliable, low-distortion actuation
amplifiers.
ACKNOWLEDGMENTS
The authors gratefully acknowledge Dr. W.H. Prosser
(NASA Langley) for suggesting the investigation o
b o nd in g agen t d egr ad ati on . T he ass i st ance o
Mr. Danny Lau (University of Michigan) in setting up
one of the experiments is also appreciated. This work
was supported by the Space Vehicle Technology
Institute under grant NCC3-989 jointly funded by
NASA and DoD within the NASA Constellation
University Institutes Project, with Ms. Claudia Meye
as the project manager.
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