[American Institute of Aeronautics and Astronautics 49th AIAA Aerospace Sciences Meeting including...
Transcript of [American Institute of Aeronautics and Astronautics 49th AIAA Aerospace Sciences Meeting including...
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High Resolution Micro-Optical Wall Shear Stress Sensor
Ulaş K. Ayaz§, Tindaro Ioppolo
*, Volkan Ötügen
†
Southern Methodist University, Dallas, TX 75275
We report an optical wall shear stress sensor based on the whispering gallery modes (WGM) of a
dielectric sphere. Radial deformations of such spheres, for example caused by shear stress, results in
a shift in the WGMs, thereby allowing one to monitor the effect (shear stress) causing such shifts.
The sensor is composed of a sensing element, which is a movable plate flush to the wall. The sensing
element is attached to a lever on one end, and the other end is in contact with the sphere. Thus, the
shear force felt by the sensing element is transmitted to the sphere mechanically through the rotation
of the lever. Previous experimental results with these spheres showed force resolutions as good as
~10-10
N, which for a sensing element of ~650 m2, would be equivalent to a few hundred Pa
resolution. In this paper, we experimentally investigate an WGM based shear stress sensor that is
composed of a PDMS sphere with base-to-curing-agent mixing ratio of 40:1 and a sensing element of
~650 m2. The sensor is first calibrated statically and then the performance characteristics of the
sensor (sensitivity to normal pressure, dynamic range and frequency response) are tested. The
calibration of the sensor is then validated by testing the sensor in a 2-D Poiseuille's flow.
I. Introduction The measurement of wall shear stress has been one of the challenges of fluid mechanics research. Significant
progress has been made in wall shear
stress measurement techniques, but still
further developments are needed. In
particular, reliable, low-noise, high
resolution sensors applicable to a wide
range of flows are needed 1,2
. Most of
the currently used sensors, such as hot-
wire/film-based anemometry 3, heat
flux gages 4, surface acoustic wave
sensors 5 and laser based velocity
sensors 6,7,8
, oil film interferometry 9,
are indirect approaches where the wall
shear stress is determined from the
measurement of another flow property.
Further, a new class of MEMS-based
sensors have been proposed recently
(thermal 10,11
, floating element 12
and
optical wall shear sensor 13
) to measure
the shear stress indirectly. Of these,
thermal sensors are simple to fabricate
but they are based on heat transfer
analogy, and their calibration can be
§
Graduate student, Mechanical Engineering Department * Post Doctoral Associate, Mechanical Engineering Dept.
† Professor, Mechanical & Aerospace Engineering Dept., AIAA Associate Fellow
Figure 1. Schematic of WGM sensor
49th AIAA Aerospace Sciences Meeting including the New Horizons Forum and Aerospace Exposition4 - 7 January 2011, Orlando, Florida
AIAA 2011-337
Copyright © 2011 by Volkan Ötügen. Published by the American Institute of Aeronautics and Astronautics, Inc., with permission.
2
difficult. Optical MEMS (MOEMS) sensors based on laser Doppler anemometry are promising, however
generating sufficiently small measurement volumes for high Reynolds number applications can be challenging. A
direct measurement method is the floating element sensor which is based on the measurement of the deflection of a
floating element that is flush with the flow. Capacitive 12,13,14
, piezoresistive 15,16
, differential optical shutter and
fringe moiré 17
techniques have been developed to measure the displacement of the floating element. Some of
these techniques are quite promising but they are still work in progress, as such, some of the MEMS and MOEMS
approaches described above may suffer from electromagnetic noise interference, tunnel vibration, and undesirable
flow through gaps.
The micro-optical sensor presented here is based on WGM resonators and is capable of measurements resolved
in time and space with a large dynamic range. It promises to overcome some of the drawbacks of the current skin
friction measurement techniques. The signal output is optical, which makes the sensor essentially immune to
electromagnetic interference. The mechanical principle is similar to the floating element technique in that the force
exerted by the flow on a small surface element flush with the wall is measured. However, whereas the typical
floating element sensor requires considerable movement/deflection to measure the force exerted by the flow, the
present sensor requires movements only in the order of nanometers for measurement. Thus, the present sensor
basically has no moving parts.
In the past few years, several optical sensor concepts have been proposed exploiting the WGM shifts of
microspheres. They include protein adsorption18,19
, trace gas detection20
, impurity detection in liquids 21
, structural
health monitoring of composite materials 22,
detection of electric field 23
, magnetic field 24, 25
and temperature26, 27
as
well as mechanical sensing, such as pressure 28
and force 29,30
. The technique we present here is an extension of the
WGM-based force sensor reported earlier 29,30
. The central element is the dielectric microsphere whose optical
mode (WGM) shifts are monitored to determine the force exerted on it by the surface (sensing) element. Several
individual sensors were built and tested to validate them under steady and unsteady conditions. Each sensor had a
surface element (plate) of 1mm x 1mm or smaller.
II. WGM Sensor Concept
The sensing is based on tracking the shifts in optical modes (WGM) of a dielectric sphere caused by applied
force. The optical modes of the sphere are excited by coupling light from a tunable laser into the sphere using a
tapered optical fiber as illustrated in Fig. 1. Light from a tunable laser is carried through an optical fiber with a
section that is stripped and tapered to about ~10 m diameter. A photodiode placed on the opposite end of the fiber
monitors the transmitted light intensity. The tapered section of the fiber serves as an input/output port for the
microsphere. When the laser frequency is tuned over a small range, the WGMs are observed as narrow dips in the
transmission spectrum through the fiber. The position of each WGM in the transmission spectrum depends on the
morphology (i.e. size, shape) of the sphere. The WGM linewidths, , can be extremely narrow thereby allowing
for the detection of even very small perturbations of the sphere’s morphology. Thus, any force applied to the
sphere that causes a detectable shift in WGM can be measured by monitoring the transmission spectrum through
the fiber.
WGMs of microspheres can be explained by ray optics. Laser light coupled at a grazing angle into the
microsphere will experience a total internal reflection, provided that the index of refraction of the sphere is greater
than that of the surrounding medium. The light will circumnavigate the interior surface of the sphere and a
resonance (WGM) will be observed when the round trip distance traveled is an integer multiple of the light
wavelength. Therefore, a first order approximation to the optical path inside the sphere would give the resonance
wavelengths as
lan 0
2 (1)
where no and a are the sphere’s refractive index and radius, is the vacuum wavelength of laser and l is an
integer representing the circumferential mode number. The above condition is valid for a >>. A minute change in
the size or the refractive index of the microsphere will lead to a shift in the resonance wavelength as
a
da
n
dnd
0
0
. (2)
3
By monitoring the WGM shifts, any effect that leads to a radial deformation or change in the refractive index
can be measured. For example, force applied to the sphere will lead to a change in both its radius and its refractive
index. However, previous investigations have shown that (dno/no) >> (da/a) when a uniaxial force is applied to the
sphere along the polar direction 30
. Thus, only the radial deformation needs to be considered for the measurement
of force.
One of the features that makes the WGM-based sensors attractive is the extremely large optical quality factors
(Q= /) associated with the spheres. Larger Q values lead to higher measurement resolution of the WGM shift
() and the physical parameter causing the shift. For example, Q values approaching the material loss limit of 1010
have been reported 31
with fused silica micro-spheres. These exceptionally large Q values cannot be reached by
planar interferometric systems such as Fabry-Perot instruments and brag gratings (which render Q values typically
in the order of 100). In the present, we obtain optical Q values between 106 and 10
7 with polymeric spheres of
diameters in the range between 200µm and 1 mm.
III. Sensor Details
A. Sensor Design A schematic and photographs of the wall shear stress sensor are shown in Figs. 2 and 3, respectively. The
cylindrical sensor cavity fits into a hole on test section wall with its outside surface flush to the wall. The top
surface of the cylindrical cavity is made of
~1 mm thick aluminum. The active
components of the sensor cavity are the
PDMS microsphere, a 125 µm silica beam
that acts as a lever, and a flat plate that
serves as the sensing surface. The silica
beam is connected to the 0.8 by 0.8 mm
square sensing plate on one end and to a
back plate (0.4 by 0.4 mm) on the other
with loctite epoxy. The back plate
compresses the microsphere against the
backstop with the force transmitted
through the beam. Both plates are made of
brass with a nominal thickness of ~25m.
The silica beam is attached to the bottom
corner of the cavity wall as shown in Fig. 2
with a PDMS 10:1 base-to-curing agent
mixing ratio. The attachment point also
serves as the pivot about which the
silica/plate system rotates. The sensing
plate is aligned flush with the wind tunnel wall with its outer side exposed to the flow. As the silica/plate system
pivots about the attachment point, it transmits the shear force experienced by the plate to the microsphere slightly
deforming it (dr/r) and causing a shift in the sphere WGM. A 60-µm latex membrane covers the gap of about 200
µm between the sensing element and the wall to prevent flow through the cavity.
Figure 2. Side view (left) and front view (right) of the shear stress
sensor
Figure 3. Top (left) and bottom (right) photographs of the shear
stress sensor
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B. Calibration Previous studies have shown that for a given sphere material, the sphere size determines the calibration factor
relating WGM shift to applied force 29,30
. For the shear stress sensor, however, the effect of the additional
components (the lever, the polymeric base at the pivoting point, latex membrane, etc) will each have an effect on
sensor calibration.
Figure 4 shows a schematic of the static calibration setup.
A cantilever beam mounted on a translational stage is used to
exert the force on the sensing surface. The beam is a silica fiber
with a length and diameter of 60 mm and 0.125 mm,
respectively. One end of the beam is attached to a micro-
translation stage while the other end (which is flattened to have a
larger surface area) is in contact with the microsphere. A
Michelson interferometer is used to measure the deflection of
the beam (with a resolution of ~ 65 nm). The force exerted on
the sensor by the deflected beam can be calculated as:
ukFbeam
(3)
where
3
4
64
3
L
DEkbeam
(4)
F is the force exerted on the sensor by
the beam and u, D, E and L are the tip
deflection, diameter, Young's modulus and
length of the beam, respectively. Figure 5
shows a typical calibration result for a PDMS
sphere with 40:1 base-to-curing-agent mixing
ratio. The sphere diameter for this case is
~700 m. The shear stress is obtained by
dividing the applied force by the sensing
surface area. The plot of Fig. 5 is essentially
linear in the range of calibration and the
sensitivity is simply d/d. Along with the
optical quality factor, sensitivity determines
the measurement resolution. If we assume
that the minimum measurable WGM shift is
∆λ= λ/Q, the measurement resolution is:
1
dd
Q
(5)
For a Q-factor of 107, the resolution for
the sensor of Fig. 5 is ~10-2
Pa. The measurement resolution can be increased by using PDMS spheres with larger
base-to-curing agent ratios which yield smaller Young's moduli. For example, Fig. 6 shows the calibration plot of
Figure 4. Experimental setup for
static calibration
d/d = 15.145 pm/Pa
0
2
4
6
8
10
12
14
16
18
20
0 0.5 1 1.5
WG
M S
hif
t, p
m
Shear Stress, Pa
Figure 5. Static calibration of sensor with a 40:1 mixing
ratio PDMS sphere of diameter ~ 700 µm
d/d = 230.87 pm/Pa
0
20
40
60
80
100
120
140
0 0.2 0.4 0.6 0.8
WG
M s
hif
t, p
m
Shear stress, Pa
Figure 6. Static calibration for shear stress sensor with a 60:1
mixing ratio PDMS sphere of diameter ~ 750 µm
5
a sensor with a 60:1 base-to-curing agent ratio PDMS sphere of diameter ~ 750 m. As shown, a fifteen fold
increase in sensitivity is achieved with this sphere. The corresponding shear stress resolution for this sensor is ~650
Pa.
Although we show here sensor results with only PDMS spheres of 40:1 and 60:1 mixing ratios, other dielectric
spheres with similar optical characteristics (such as silica, PMMA etc.) can also be used for this type of sensor. By
changing the sphere diameter and material, a wide range of measurement range and resolution can thus be obtained.
C. Normal Pressure Response Shear stress sensors are subject to a normal
pressure due to the pressure difference between the
test section (flow channel) and the surrounding
medium (atmospheric pressure). The sensor's
response to such a pressure could add additional
noise in the measurements. In order to test the
response of the sensor to the normal pressure, we
mounted the sensor on a test chamber where, the
sensing element was subject to the pressure in the
chamber. The microsphere used for this test had
~700 m and it was made of PDMS 40:1 base to
curing agent mixing ratio. The pressure inside the
chamber was changed and the corresponding
WGM shifts were observed. The WGM shifts with
respect to the changes in the normal pressure are shown in Fig. 7.
As it is seen in the figure, the sensor does not respond to the changes in the normal pressure. The random
scatter in the data is most likely due to the vibration of the test section as it was subject to the normal pressure.
D. Dynamic Range
The dynamic range of the sensor is defined as the ratio of maximum to minimum shear stress it can measure.
In the proposed sensor, since WGMs of the dielectric microsphere essentially defines this ratio, we setup an
experiment to measure the dynamic range
of the microsphere. Figure 8 illustrates
the setup for this experiment. Basically,
a PDMS microsphere of 60:1 base to
curing agent mixing ratio and ~900 m
diameter is placed between two infinitely
stiff metallic plates, one of which is
attached to 1-D translation stage whereas
the other remained fixed in position. A
Michelson interferometer is used to
measure the distance the translational
stage moved. The translation stage is
moved forward for ~ 200 m and then it
was moved back. The WGM shifts
during the loading and unloading process
of the sphere are given in Fig. 9. Note
that the data in Fig. 2 represents a slight
scatter (< 2%).
The dynamic range of the sphere is
calculated as:
max
(6)
Figure 8. Experimental setup for dynamic range
measurements
-0.20
-0.15
-0.10
-0.05
0.00
0.05
0.10
0.15
0.20
0 20 40 60 80
WG
M s
hif
t, p
m
Normal Pressure, Pa
Figure 7. Sensor response to applied normal Pressure
6
Where max is the
maximum applied shear
stress and is the
minimum resolvable shear
stress. Previously, we
have shown that the
WGMs are linear with
respect to the radial
deformation 29,30
,
therefore, we can rewrite
the Eq. (6) as:
L
L
max
(7)
With Q-factor given
as:
L
DQ
(8) where Lmax is the maximum distance
the translation stage has moved and L is
the minimum resolvable displacement, and
D is the diameter of the sphere. Thus, the
minimum resolvable distance is given as
Q
RL
(9)
Assuming a Q~107, the data in Fig. 9
would result in a dynamic range as high as
~5x105, >100 dB.
E. Frequency Response Dynamic calibrations have also been
carried out to determine the frequency
response of the sensors. The setup for
dynamic calibrations is a variation of
the static setup shown in Fig 4. The
long optical fiber beam is replaced by
a short, rigid beam that is connected
to a piezoelectric actuator. The
actuator is driven at a range
frequencies while the displacement
amplitude is kept constant. Several
measurements (typically, 5 to 8) are
made at each frequency, and the
corresponding WGM shifts are
plotted against frequency as shown in
Figs. 10 and 11 for PDMS spheres of
60:1 and 40:1 mixing ratios,
respectively.
0123456789
0 200 400 600 800
WG
M s
hif
t, p
m
Frequency, Hz
Figure 10. Frequency response for WGM shear stress sensor
with a PDMS sphere (60:1 mixing ratio, ~750 m diameter)
0
1
2
3
4
5
6
0 1000 2000 3000 4000
WG
M S
hif
t, p
m
Frequency, Hz
Figure 11. Results of the frequency response for WGM shear stress
sensor with a PDMS sphere (40:1 mixing ratio, ~700 m diameter)
Figure 9. The WGM shifts with respect to the displacement
of the translational stage. (Sphere diameter ~900 m)
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For the 60:1 mixing ratio sphere, the natural frequency of the sensor is around ~300 Hz. Therefore, the
sensor's performance is limited to a bandwidth < 300 Hz. The sphere with 40:1 mixing ratio, on the other hand,
possesses a fairly flat frequency response
up to ~3.5 kHz. Thus, as it is typical of a
sensor that has any mechanical
components, the present sensor presents
a tradeoff between bandwidth and
sensitivity.
IV. Experiments
A schematic of the two-dimensional
wind tunnel is shown in Fig. 12. In order
to achieve a two-dimensional flow in the
mid section, the cross-section of the
wind tunnel has a large aspect ratio; the
height and span of the channel are 4.76 ±
0.05 mm and 160 mm, respectively
yielding an aspect ratio of AR ~33. The
test section is far enough from the
entrance (800 mm) so that the flow in the
test region is fully developed for nearly
the full range of flow rates considered.
A set of six pressure taps are located inside the wind tunnel at the mid-point to measure the streamwise distribution
of the wall pressure. The pressure taps are placed on the wall opposite to the wall shear sensor, and have a diameter
of ~100m to minimize flow
perturbations and spatial
integration effects in the measured
pressure. Each tap is connected to a
Scanivalve which is attached to
pressure transducer as shown. At
the outlet of the tunnel, a fan
operates in the suction mode to
drive the air flow inside the
channel. The fan is controlled by a
dc motor and its rpm can be varied
continuously allowing for
measurements at different flow
rates. For a fully developed one-
dimensional isothermal flow, the
shear stress at the wall can be
calculated from
dx
xdPh
2
(10)
where h is the channel height and dP/dx
is the streamwise gradient of pressure in the
fully developed flow region. In these
experiments, the shear stress calculated by
Eq. (10) is compared to the shear stress
measured by the optical sensor. Figure 13,
shows the results of a typical experiment
Figure 12. Test facility for the steady flow studies
0
0.05
0.1
0.15
0.2
0.25
0.3
0.35
0.4
-0.5
0.5
1.5
2.5
3.5
4.5
5.5
0.00 5.00 10.00 15.00 20.00 25.00
She
ar S
tre
ss, P
a
WG
M s
hif
ts,
pm
Time, seconds
WGM sensor
Calculated shear stress
Fig ure 13. Steady flow test results for the WGM shear stress sensor
-0.05
0
0.05
0.1
0.15
0.2
0.25
0.3
0.35
0 0.1 0.2 0.3 0.4
Wa
ll s
hea
r st
ress
, P
a (
WG
M
sen
sor)
Wall shear stress, Pa (Calculated)
Figure 14. Comparison of WGM sensor results to those
calculated from pressure drop
8
where the flow rate is first increased and then decreased over a long period of time. The figure presents both the
shear stress calculated from Eq (10) and the WGM shifts registered from the optical sensor. Figure 14 compares the
results directly obtained by the WGM sensor and those inferred from the pressure gradients. (The WGM shifts are
converted to shear stress using the calibration curve of Fig 5). The solid line in Fig 11 represents perfect
coincidence of two data sets. Clearly, there is strong agreement between the two measurements and, further, the
sensor shows no hysteresis effects.
V. Conclusion
An optical wall shear stress sensor based on whispering gallery modes of a spherical resonator has been
demonstrated. In situ calibration as well as the frequency response of the sensor have been investigated. Shear
stress resolutions of the order of 10-2
Pa have been demonstrated when a 700 µm diameter PDMS sphere with 40:1
base-to-curing agent mixing ratio is used. This resolution is further improved to ~650 Pa if a 60:1 mixing ratio
PDMS sphere is used. However, frequency response tests show that, while using a softer material for sphere
improves the resolution of the sensor, at the same time there is a corresponding reduction in the sensor bandwidth.
The sensor is linear even when the sphere deformation is on the order of hundreds of microns promising to have
extremely high dynamic range.
Acknowledgements
We acknowledge the support from the National Science Foundation through grant CBET-0809240 with Dr.
Henning Winter as program director and the Air Force Office of Scientific Research through STTR contract FA
9550-10-C-0091 with Dr. John Schmisseur as program manager.
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