ij----------------...surface elastic waves 2.1 properties of surface elastic waves 2.2 types of...
TRANSCRIPT
.~PLICATION OF OPTICAL FIBERS TO WIDEBAND DIFFERENTIAL INTERFEROMETRY AND MEASUREMENTS OF PULSED WAVES IN LIQUIDS
by
Avinash 0. Garg
Thesis submitted to the Faculty of the
Virginia Polytechnic Institute and State University
in partial fulfillment of the requirements for the degree of
MASTER OF SCIENCE
in
ELECTRICAL ENGINEERING
A?PROVED:
. . . ----------------------------Dr. R. 0. Claus
iJ----------------Dr. L. C. Burton Dr. D. D. Chen
July, 1982 Blacksburg, Virginia
ACKNOWLEDGEMENTS
I would like to thank my advisor, Dr. R. 0. Claus, for
his time, encouragement and unceasing patience. I also wish
to thank my graduate committee, Dr. L. C. Burton and Dr. D.
D. Chen for their comments and suggestions
I am indebted to Tyson Turner and· Dan Dockery for their
help and numerous suggestions. Among those whom I owe spe-
cific gratitude are Vicki Trump and my colleagues Janet
Wade, John Gray and Sam Zerwerkh.
I must include special note of appreciation to my par-
ents for their love and endless patience and moral support.
ii
TABLE OF CONTENTS
ACKNOWLEDGEMENTS . . . . . . . . . . . . . . . . . . . . ii
Chapter page
I.
I I.
INTRODUCTION
SURFACE ELASTIC WAVES
2.1 Properties of Surface Elastic Waves 2.2 Types of Elastic Waves 2.3 Rayleigh Waves 2.4 Stoneley Waves .....
1
4
4 5 8
10
III. DETECTION OF SURFACE WAVES USING SURFACE DEVICES 12
IV.
v.
VI.
3.1 Transduction ...... . 3.2 Piezoelecetric transducers
3.2.1 Piezoelectricity 3.2.2 Piezoelectric Transducers
3.3 Electromagnetic transducers 3.4 Electrostatic transducers
OPTICAL DETECTION TECHNIQUES
4.1 Interaction of surface waves with optical waves . . . . . . .
4.2 Michelson Interferometer .. 4.3 Stabilized path interferometer 4.4.Differential Interferometer
FIBER DIFFERENTIAL INTERFEROMETER
12 . 13
13 18 22
. 23
28
28 36 42 44
56
5.1 Differential Fiber System . 56 5.2 Maximum permissible DC movement of the
surf ace 60 5.3 Measurements 66 5.4 Results 67
BULK WAVE DETECTION USING DIFFERENTIAL INTERFEROMETRIC TECHNIQUES 69
6.1 Technique for the detection of bulk waves 69 6.2 Two beam differential system for bulk wave
detection . . . . . . . . . . . . . . . 70 6.3 Four beam differential system for detection
of bulk waves 80 6.4 Results ........... 88
iii
VII. CONCLUSIONS AND FURTHER REFINEMENTS ........ 90
REFERENCES . . . . . . . . . . . . . . . . . . . . . . . 94
Appendix page
A. PREPARATION OF SINGLE MODE FIBERS FOR EXPERIMENTS . 98
B. COMPUTER PROGRAM FOR CALCULATING THE POSITIONS OF LENSES FOR VARIOUS SAW FREQUENCIES 105
C. DATA FOR THE DETECTION OF PULSED WAVE IN WATER USING TWO BEAM DIFFERENTIAL SYSTEM 118
D. DATA FOR DETECTION OF THE DIRECTION OF PULSED WAVE IN WATER USING FOUR BEAM SYSTEM 121
VITA 127
ABSTRACT
iv
LIST OF TABLES
Table page
3.1. Types of Crystals and their Constants [11] . 17
6.1. Data values for detection of compressional waves in water (refer figure 6.4) . . 79
6.2. Data values for detection of direction of bulk waves in water (refer figure 6.10) . . 89
v
LIST OF FIGURES
Figure
3.la. Quartz crystal structure
3.lb. Crystal cuts
3.2. Piezoelectric transducer
3.3. Electromagnetic transducer
3.4. Electrostatic transducer .
4.1. Flat plate Fabry-Perot interferometer
4.2. Bulk waves in water .
4.3. Diffraction of light by compressional waves in water
4.4. Michelson interferometer
4.5. Stabilized optical path interferometer
4.6. Differential interferometer .
4.7. Basic differential interferometer geometry
4.8. Narrowband differential interferometry
4.9. Sensitivity of a differential interferometer
4.10. Sensitivity of differential interferometer as a
page
14
15
20
24
25
32
35
37
38
43
4S
47
50
S4
function of spot separation . SS
S.l. Fiber differential interferometer 57
S.2. Remote detection head S9
5.3. Gaussian wavefront in far field 61
5.4. Focussed gaussian beam 62
vi
5.5. Collimated gaussian beam 65
5.6.. Result from pulse generation on mirror surface . 67
6.1. Two beam system for detection of bulk waves in water . 71
6.2. Water tank 72
6.3. Data for the scan of a standing bulk wave in the water tank . . . . . . . . . . 74
6.4. Sensitivity of system to position of beams on bulk waves in water . . 75
6.5. Data for the detection of pulse using two beam system 77
6.6. Path of ultrasonic pulse in the water tank 78
6.7. Four beam system for detection of direction of bulk waves in water . . . . . . . . 81
6.8. Diffraction patterns due to a single and crossed gratings . . . . . . 82
6.9. Modified four beam system . 85
6.10. Data from four beam system 86
7.1. Diffraction pattern due to grating and square aperture . 92
A.1. Path of ray of light through a step index optical fiber . . . . . . . . . . . . . 99
A.2. Transmission modes in an optical fiber 102
C.l. Detection of ultrasonic pulse using two beam system 118
C.2. Comparison of RF noise to signal from the two beam system . . . . . . . 119
D.l. Detection of the pulsed bulk wave in water (vertical pair of beams) 122
vii
D.2. Detection of pulsed bulk wave in water (horizontal pairs of beams) .
D.3. RF noise due to Metrotek pulser and laser noise
D.4. Detection of direction of pulsed wave in water using one set of beams
D.S. Detection of direction of pulsed wave in water using the remaining pair of beams .
viii
123
124
125
126
Chapter I
INTRODUCTION
Practical measurements of surface acoustic waves (SAW)
and bulk waves in materials evaluation applications require
the use of sensing systems with a linear response and good
sensitivity over a wide dynamic range. More importantly,
these devices should be insensitive to low frequency speci-
men translations, such as those typically caused by back-
ground vibrational noises in on-site measurement situations,
and must be adaptable to specimen surface orientation.
Several types of transducers may be used for these mea-
surements, all having their respective advantages and disad-
vantages. Piezoelectric transducers are perhaps the most
easily used but they tend to mechanically load the surface,
thereby distorting the surface particle displacement fields
to be measured. Like the non-contacting electromagnetic and
capacitive transducers, they also effectively integrate par-
ticle motion across their active surface areas, producing
output signals for which the transfer functions are not very
well characterized.
Optical techniques are thus pref erred over these trans-
ducers because they off er a wide dynamic range and because
1
2
output signals from these techniques are directly propor-
tional to surface acoustic wave amplitude. Optical techni-
ques offer sensitivity and frequency response similar to or
better than the surface contacting and non-contacting trans-
ducers, and at the same time also allow point surface prob-
ing without surface loading. Although many optical techni-
ques due to their design are sensitive to surface acoustic
wave signals and low frequency vibrational noises, differen-
tial methods having variable acoustic bandwiths which can be
tuned to eliminate the noise component from the ouput signal
are preferred. In addition to these advantages, optical
techniques are available which can be made insensitive to
surface irregularities.
Here we descibe the construction and theory of opera-
tion of one such optical technique. This system has all the
above mentioned advantages of the various optical techniques
and in addition is convenient for the inspection of surfaces
oriented in any direction. This has been achieved by the use
of optical fibers for transmitting light from input optics
to output optics, thus providing separate input and detec-
tion units which may be easily positioned.
3
The application of the same type of optical probing to
bulk waves in liquids is also described. Specifically, dif-
ferential interferometric techniques have been used for the
detection of pulsed bulk waves in water. Herein we describe
a pulsed two laser beam system and a four beam system for
determining the propagation direction of the bulk wave.
The discussion follows with Chapter 2 which introduces
elastic waves and their properties which have made them
popular in field of nondestructive testing. We then consider
in Chapter 3 the various surface contacting and non-contact-
ing devices for the detection of SAW on specimen surfaces.
Chapter 4 briefly introduces various optical techniques
including the theory behind the Michelson and differential
interferometers. With the theory behind us we now discuss
the development, construction and results of the fiber dif-
ferential system. Chapter 6 deals with the detection of com-
pressional waves in water using two and four beam diff eren-
tial interferometric techniques.
Chapter II
SURFACE ELASTIC WAVES
2.1 PROPERTIES OF SURFACE ELASTIC WAVES
Interest in elastic waves in electronics and signal
processing applications can be attributed to their various
properties, the most important one being their very low vel-
ocities as compared to those of electromagnetic waves. These
velocities range from 1.Sxl0 3 m/s to approximately 12xl0 3
m/s, with surface elastic wave velocities lying in the lower
third of this range; this is about 10 5 times smaller than
electromagnetic wave velocities [1]. The major advantage of
this low velocity is that the physical size of elastic wave
resonators is 105 · times smaller than their electromagnetic
counterparts. Thus, attractively small elastic wave tran-
smission components such as resonators, filters, and delay
lines can be made for use in electronics.
Interactions between elastic waves and other waves and
beams can also be used for modulation and detection. El as-
tic waves can be amplified by allowing them to propagate in
a medium which also contains charge carriers drifting under
the influence of an applied voltage. Nonreciprocal propaga-
tion of elastic waves occurs in certain magnetic materials
located in a steady magnetic field. Also, in some magnetic
4
5
materials there is a strong interaction between elastic
waves and magnetic waves and this property can be used for
the transduction of bulk elastic waves. Interaction of sound
and elastic waves has been used in devices like ultrasonic
beam deflectors.
Elastic waves can also propagate along the external
boundaries of solids and these surface waves can be used for
flaw detection in manufactured objects. Since the velocity
and direction of propagation of the surface acoustic wave
can be altered by surface and substrate treatment, these
observables can be used to determine surface characteris-
tics. These properties and various others have made surface
elastic waves useful in the field of nondestructive testing
and evaluation.
2.2 TYPES OF ELASTIC WAVES
Elastic waves can be categorized depending upon their
properties and modes. The two major groups are bulk waves
and surface elastic waves.
Bulk waves can propagate in any direction in a solid
irrespective of the isotropic or anisotropic elastic nature
of the solid. The phase velocities of the bulk waves are
6
independent of frequency (at least from below 20 kHz up to
the microwave frequency range) and are numerically equal to
the square root of a linear combination of the elastic
stiffness constants divided by the mass density of the sol-
ids. Three independent bulk waves can propagate in a given
direction. One of these is along the direction of propaga-
tion (longitudinal bulk waves). The other two are transverse
bulk waves having particle displacements entirely tran-
sverse to the direction of propagation.
On the other hand, as a surf ace wave propagates along
the free surface of a solid, the particles on the surf ace
move in elliptical paths. This motion of a surface wave can
be decomposed into two components, one in the direction of
propagation and one normal to the free surface. Both longi-
tudinal and transverse strain are associated with the
motion. The phase velocity is similar to that of bulk waves,
but since the particles at a free surface are subjected to
less strain than particles deep inside the bulk of the
solid, the surface wave velocity is lower than the bulk wave
velocities. Because of the low velocities the surface wave
energy thus cannot propagate into the interior and hence
tends to remain on the surface. The surface wave amplitude
decreases from its value at the surface to small values at a
7
depth of about a wavelength. As an example of the distances
involved, ~ surface wave in glass has a velocity of 3180
m/s, so that a wavelength at 2. 25 MHz is approximately 1. 4
mm.
Other important distinguishing charactersitics of sur-
face waves are the accompanying electromagnetic field in
piezoelectric and magnetic materials, and their dispersive
propagation in layered media. At high frequencies surface
waves are also quite sensitive to surface irregularities and
to contamination on the surfaces. This can be used to advan-
tage in the nondestructive testing of various materials, as
this characteristic permits easy damping of unwanted surface
waves and also accounts for loss and scattering.
Surface elastic waves can be further subclassified
according to their various modes of propagation. Elastic
waves traveling on a .free
on the surface of water)
Lord Rayleigh in 1885 and
solid surface (analogous to waves
were mathematically predicted by
hence are called Rayleigh waves
[4]. These waves are frequently used in nondestructive test-
ing and evaluation. In addition to these types of surface
waves, there are waves with characteristics similar to Ray-
leigh waves although they are not free surface phenomena;
8
these are interface waves. In 1924 Stoneley analyzed the
more generalized case of elastic waves propagating along the
surface of separation of two solids [4]. His results con-
firm that elastic waves similar to Rayleigh waves may exist
along the boundary between two solids under the more strin-
gent conditions that the shear wave velocities of the two
media be nearly equal. Hence these interface waves have been
called Stoneley waves. Other waves like Love waves in seis-
mology, consisting of transverse guided waves in bound solid
layers, and Lamb waves in thin plates or laminations, have
been classified as surface waves although their basic nature
is very much different from the Rayleigh and Stoneley waves.
Besides these, there also exist refraction arrivals. This
type of wave can be readily excited in the ultrasonic range
at the contact interface between two different media. This
type of elastic wave, although a body wave, is guided by the
interface and is usually termed an interface wave. This is
actually the refracted wave commonly used in geophysical
exploration and subsurface geological mapping [4].
2.3 RAYLEIGH WAVES
The characteristics of Rayleigh waves (waves traveling
on the surface of a homogeneous solid medium in a vacuum or
9
air) are that their amplitude decreases rapidly with dis-
tance from the surface, their propagation velocities are
less than that of bulk waves in an unbounded medium, and,
except in the plane wave case, their intensity diminishes
with propagation distance at a rate proportional to the
inverse first power of the distance rather than the usual
inverse square law relationship. This diminishing amplitude
of the Rayleigh wave exemplifies the inhomogeneous nature of
these waves and is analagous to the skin effect of electro-
magnetic waves.
A plane inhomogeneous wave can be expressed by the gen-
eralized wave expression
¢'=Aexp[-(k" x+k" y+k" z)]x x y z
exp[-i(wt-k' x-k' y-k' z)], x y z (2.3.1)
where the wave now propagates in the (k'x,k'y,k'z) direction
and its amplitude decreases in the perpendicular direction
given by (k"x,k"y,k"z). This is the inhomogeneous wave con-
dition.
Assume an inhomogeneous plane wave in rectangular coor-
dinates with the direction of propagation parallel to the
x-y plane. Let 80 be the angle of incidence with respect to
10
the x-axis; 80 is a complex quantity 80 =a+ie. Thus under
proper substituion the wave equation now becomes:
~'=Aexp{-ksinhe[ysina-xcosa]}x
exp{-i[wt-kcoshe(xsina+ycosa)]}. (2.3.2)
This function again shows the exponential decrease in ampli-
tude at right angles to the direction of propagation and
also shows the effective wave propagation vector to be
kcoshe. Using this effective wave number , the wave velocity
is noted to be
c'=w/(kcoshe)=c/(coshe),
where c is the plane wave velocity.
(2.3.3)
The velocity of the
inhomogeneous wave is thus less than the plane wave veloc-
ity. Moreover, for large values of e, low propagation veloc-
ity occurs in the x direction as well as a rapid decrease in
amplitude in the y direction.
2.4 STONELEY WAVES
Waves traveling along the bounding interface between
two solids are kn~wn as Stoneley waves. If a layer of a dif-
ferent material is attached to a surface of a semi-infinte
solid, a Stoneley wave may propagate with a phase velocity
which is frequency dependent such that the wavelength is
11
comparable with the layer thickness. This effect in layered
solids permits one to fabricate wave guiding structures with
which the wave energy can be directed about in the surface
plane; it also permits construction of delay lines in which
the delay depends on the frequency [11]. The velocity of
the Stoneley waves has been shown to be less than that of
the slowest shear waves in either medium. Also the veloci-
ties of Stoneley waves have been found to be higher than
highest value of free surface Rayleigh waves in either med-
ium. This constraint strongly limits the existence of
Stoneley waves.
Chapter III
DETECTION OF SURFACE WAVES USING SURFACE DEVICES
3.1 TRANSDUCTION
Interaction of the detection system and an acoustic
wave on a surface is termed transduction. This interaction,
however, should take place so as to create a negligible
effect on the surface wave being detected. Various types of
contacting and noncontacting transducers have been used for
the detection of elastic waves (mainly surface elastic
waves). Each of these have their inherent advantages and
disadvantages which determine their particular uses. Piezoe-
lectric transducers are very highly sensitive devices and
have a wide dynamic range but they tend to load the surf ace
under test. Noncontacting transducers like electromagnetic
and electrostatic transducers solve this loading problem to
some extent, but due to their finite size they tend to inte-
grate over the area of their surface giving transforms of
signals which cannot be easily characterized. Their finite
size also makes point probing of a surface impossible.
Optical detection techniques have
made transduction possible with
been developed which have
negligible loading on the
surface and which at the same time permit point probing of
the surface. These techniques are highly sensitive anti have
12
13
a very wide dynamic range. They also eliminate the depen-
dence of the system on the type of material surface being
tested.
3.2 PIEZOELECETRIC TRANSDUCERS
3.2.1 Piezoelectricity
Certain crystals, when mechanically strained by the
application of an external stress, generate electric charges
on certain of their crystal surfaces. The polarity of these
charges reverses when the direction of strain is reversed.
This effect is called the piezoelectric effect. Conversely,
when charges are applied by external means to faces of the
crystal, the crystal exihibits strain, i.e. dimensions of
the crystal change. Reversing the direction of the applied
field reverses the sign (direction) of this strain.
Piezoelectric axes of the crystal are defined as direc-
tions in which tension or compression develop polarization
parallel to the strain. A crystal is said to be an "X-cut"
when its plate is cut with its face perpendicular to the
X-axis of the crystal; while one cut with its faces parallel
to the lateral faces of the crystal is termed as a "Y-cut". :1
Other often used crystal cuts include the "Z-cut" and the
"AC-cut" crystals. The various cuts dictate "the various uses
of the transducers and are shown in Figure 3.1 (11]. Their
14
z z
y
Left Hand Right Hand
z
x I. R. E. Axes and angles.
FIGURE 3.la. Quartz crystal structure [ll].
15
z
X-CUT
Z-CUT
AT +35.15° BT- 49° CT+ 3 8° OT- '52° ET+ 66° FT - 57°
z
Y-CUT
y
CUT e ¢ l/J x 0 90 90 y 90 90 90 z 0 0 0
AC 90 59 90
FIGURE 3.lb. Principal crystal cuts used in piezoelectric transduction [ 1 1 ].
16
advantages and disadvantages have been discussed in the
following section.
The piezoelectric crystal, due to its piezoelectric
properties, can be used for converting mechanical signals
into electrical signals and vice-versa. This property has
been utilized to manufacture piezoelectric transducers. Dif-
ferent piezoelectric crystals used for the manufacture of
transducers are listed in Table 3.1. The strain and stress,
related by elastic constants of the crystals, can be related
to the electrical parameters like electrical charge, vol-
tage, and polarization by constants of proportionality.
These constants are the piezoelectric constants for the par-
ticular crystal. Since the crystals are not isotropic,
these constants and elastic constants are different for dif-
ferent directions in the crystal [11].
Depending on the direction of the applied field and the
orientation of the crystal, various stresses and strains in
the crystal can be produced. An electric field applied per-
pendicular to the faces of an X-cut quartz plate will pro-
duce elongation along the X-axis,
Y-axis and shear in the Y plane.
compression along the
If an alternating field
with this orientation is applied to the crystal, the crystal
17
TABLE 3.1.
MATERIAL FORMULA PIEZOELECTRIC CONSTANTS DIELECTRIC CONSTANT coulombs/newtons with respect
or to air meters/volt
x 10-12
Quartz Si02 dll -2.3 4.5
dl4 +0.7 4.5
Tourmaline Silicate of dl5 -3.7 6.3
B and Al with d22 -0.3 6.3 one or more
other metals. d31 -0.3 7.1 Variable comp-
d33 -1.9 7.1 osition.
Rochelle KNaC4H4o6 .4H20 dl4 = approx. 550 350 Salt 30° at
ADP NH4H2Po4 dl4 -1.5 56
d36 +48 16
KDP KH2Po4 dl4 +l. 3 42
d36 +21 21
Barium BaTi03 dlS +390 2900 Titanate
d31 -37 170 Crystal d33 +84 170
Barium BaTi03 dl5 +280 1450 Titanate Ceramic d31 -78 1700
d33 +190 1700
18
can be made to oscillate with a frequency dependent upon the
thickness of the crystal.
Crystal quartz is the most widely used piezoelectric
material for the construction of stable oscillators. This
can be attributed to two of its major properties: (1)
quartz can be used for its piezoelectric properties up to
573° c, and 2) the piezoelectric constants of quartz are
less temperature dependent than those of other materials.
3.2.2 Piezoelectric Transducers
Piezoelectric transduction can be accomplished by pro-
ducing an RF (radio frequency) electric field between the
end faces of a massive piezoelectric crystal or a thin pie-
zoelectric crystal mounted on a massive substrate.
The design of the mounting for the crystals is impor-
tant in many applications. Crystal mounting can affect its
freedom to oscillate, its damping, and its sensitivity as a
detector of mechanical motion. The design is also critical
because mapy times it is desired to have the crystal serve
as an interface between one fluid medium and other. Here
the seal has to be liquid tight and gas tight.
19
A much utilized piezoelectric element is a plate cut
from a piezoelectric crystal such that a voltage applied to
the two parallel surfaces of the plate produce a strain in
the direction perpendicular to these surfaces. This is some-
times called a compression plate. A widely used plate of
this type is an X-cut quartz plate; the parallel surfaces
are cut perpendicular to the X-axis of the crystal. The
applicable piezoelectric constant for this X-cut quartz is
d 22 in Table 3.1. X-cut quartz crystal is especially useful
in transducer design to generate ultrasonic longitudinal
vibrations in liquids, gases, and solids [11]. A basic
design for a pizoelectric transducer is shown in Figure 3.2
[ 23 l .
The compression plate described has the interesting
property that the displacement of one of the surfaces with
respect to the other, i.e., the change in thickness ot, is
directly proportional to the voltage difference V between
the surfaces, and is independent of the thickness t of the
plate. This can be shown as follows. The strain is directly
proportional to charge Q per unit surface area, as
ot/t = d 22 Q4TI/K. (3.3.l)
Considering the crystal plate as a parallel plate capacia-
tor,
PIEZOELECTRIC -----t-+-t-~--D IS K
WEAR PLATE
20
---CASE
BNC
CONNECTOR
FIGURE 3.2. Schematic of a typical piezoelectric transducer [30].
21
Q = KV I ( 41Tt) I ( 3 . 3 . 2 )
where K is the appropriate dielectric constant of the X-cut
quartz. Therefore,
6t/t = d2 2 ( v /t) t (3.3.3)
or ct is directly proportional to voltage V, independent of
t [ 11] .
X-cut quartz transducers are primarily used for the
generation of longitudinal or compressional waves; AC-cut or
Y-cut quartz finds uses in the generation and detection of
shear or transverse waves. The Y-cut is one of the most
coupled of the series of different cut transducers for it is
not completely free from parasitic vibrations caused by
cross coupling between modes. It also has a frequency change
in its thickness vibration as the temperature is changed.
The AC-cut vibrates in a very pure shear mode with a low
temperature coeffiecent of frequency change. The AC-cut is
also less fragile than the Y-cut for a given thickness and
may be driven at higher voltages [11].
Finally, because of the symmetrical elastic properties
of tourmaline about the Z-axis, a Z-cut tourmaline trans-,,
ducer gives a pure compressional wave in the Z-direction.
22
3.3 ELECTROMAGNETIC TRANSDUCERS
The progress of ultrasonics was hampered by the lack of
development of transducer materials. Lorentz force transduc-
tion solved this problem to a great extent. In the process
of Lorentz force transduction, an electric current flowing
through a conductor such as a coil induces eddy currents on
a separate electrically conducting substrate subjected to an
external magnetic field.
In electromagnetic transducers, a field is electromag-
netically induced across the gap between the coil and the
conducting substrate and the field decays exponentially with
distance from the surface according to the classical skin
depth effect.
Electromagnetic acoustic transducers (EMATs, EMTs, or
EATs) are devices consisting of a flat coil placed near the
surf ace of a conducting nonmagnetic specimen placed in an
external magnetic field. The energized coils induce an eddy
current in the skin depth region of the conductor which,
because of the static magnetic field, exerts a Lorentz force
per unit volume resulting in a mechanical wave. The direc-
tion of the magnetic field parallel to the specimen surface
governs the type of wave, longitudinal or shear, to ~e gen-
erated in the specimen [19].
Figure 3.3.
23
Some basic EMATs are shown in
The major advantage of these transducers over previous
transducers is the absence of a coupling layer which permits
unique measurement possibilities in severe environments,
under dynamic conditions, and on unprepared specimen sur-
faces. In addition, absolute measurements of sound fields,
in principle, are possible. This feature indicates the
reproducibility of ultrasonic measurements so such transduc-
ers can also be used for the calibration of other transduc-
ers.
3.4 ELECTROSTATIC TRANSDUCERS
Like electromagnetic transducers, electrostatic trans-
ducers (ESATs) can be used as noncontacting transmitters and
receivers of ultrasound in materials. An ESAT is essentially
a capaciator whose two electrodes are the specimen itself
and one external electrode with a gap between them. Figure
3.4 shows a typical ESAT. The electrodes are parallel to
each other and their surfaces should be resonably smooth.
Polarization charges appear on both electrodes in the pres-
ence of an applied field. This electric field may result
either from an alternating potential difference or a static
ELECT RI CAL COIL
ELECTRIC AL COIL
24
SAMARIUM COBALT --- MAGNET
s I } MEANDER
"' COIL EMAT
/ , ,
/ /
/ / / /
I / / I
/ / I /
~sv' {a)
SAMARIUM COBALT .. ,..__ MAGNET
[I ~ I ~ I ~ I : II]}~;~~~~ c
a ~
~ ) ., s Q ~
Q 8 ( ~ a> I ® ~
0 ~ l Q l3J I
~
f) ~SH ( b)
FORCES F= JxB
J t-+ F . B
WAVE
FORCES F=JxB
WAVE
FIGURE 3.3. Electromagnetic transducers with (a) meander coil to excite vertically polarized shear wave, and (b) periodic magnet to excite horizontally polarized shear wave[36].
25
ELECTRODE
OPTICAL FLAT
•
FIGURE 3.4. Schematic of an electrostatic transducer [27,35).
26
bias voltage applied across the gap (19]. The first method
limits the use of an ESAT as a source only whereas the sec-
ond method permits ESATs to be used as either a receiver or
a source of ultrasound on a surface.
The basis of an electrostatic transducer as an ultra-
sound source is the coulomb force excited on the polariza-
tion charges. For a polarization charge density o, the cou-
lomb force exerted is (19]
(3.5.l)
where Ea is the permittivity of the dielectric between the
two electrodes. The surface charge is [19]
where C = Ea/h is the capacitance per unit area across the m
gap hand Vt= Va+V(w). Va is the static de bias voltage and
V(w) is the signal voltage (19].
The system traction F2 which acts normal to the speci-
men is (28]
F (w) = (C 2 Va/Ea)V(w}. z m (3.5.3)
In the alternate excitation method, no de bias field is
used, but rather a high amplitude, time varying signal, e.g.
27
V0 sinwt, is applied [19]. As shown by Cantrell and Breazeale
[27], the surface tractions F, z acting on the specimen sur-
face in this case, are
F (w) = (SV 0 2 /(2h 2 ))(1-cos2wt), z (3.5.4)
which is twice the frequency of the applied voltage. In most
applications of the ESAT as a detector of ultrasound, a~vol-
tage proportional to capacitance charge is produced, pro-
vided that the de polarizing voltage is connected to the
ESAT with a large (~20 Megohm) resistor [19].
Chapter IV
OPTICAL DETECTION TECHNIQUES
4.1 INTERACTION OF SURFACE WAVES WITH OPTICAL WAVES
In the study of nondestructive testing and evaluation
using acoustic systems, one is frequently concerned with the
geometric distribution of acoustic fields on a free surface.
Surface acoustic waves which produce surface disturbances
can be directly measured using phase measurement techniques.
Hence, we require instruments which probe both the amplitude
and phase of the local field. Direct measurement instru-
ments include piezoelectric and electromagnetic transducers,
both of which require contact with the sample and are lim-
ited in frequency response. In addition, use of such a sur-
face probe tends to perturb the acoustic field distribution
and the extent of this perturbation is not easily assessed.
In contrast, optical probes certainly interact with the
surface but have a little effect on the acoustic field pro-
pagation. This "low coupling" implies a correspondingly low
optical power and hence loading effects are negligible. Use
of optical probes allows the easy probing at different
points on the surface. Other advantages include no compli-
cated mechanical or electrical connections (as in the case
of electromagnetic and electrostatic transducers) or p~epa-
28
29
ration of the surface other than polishing. Additionally,
optical techniques are applicable, unlike piezoelectric and
electromagnetic transducers,
which are at least partially
to virtually all materials
reflecting and over a wide
range of surface acoustic wave frequencies. Even with their
loose coupling, optical techniques have a very high sensi-
tivity. Typically, optical interferometers have been devel-
oped with capabilites of measuring vibrations of the order
of 3x10- 10 cm [2].
Different types of optical interactions have been used
to detect surface acoustic waves and bulk waves. Perhaps the
most common one is the detection of surface displacements by
the phase modulation of a laser beam by the acoustic wave.
Because photodetectors are insensitive to phase changes in
the optical beam, the output beam must be amplitude modu-
lated with a signal retaining the acoustic phase informa-
tion. This can be done by interferometric techniques which
involve some type of a phase bridge. A Michelson interferom-
eter, for example, is set up using a fixed or a moving mir-
ror to supply the reference beam and a partially reflecting
surface under test to supply the signal beam. Provided that
the laser beam diameter is smaller than the SAW wavelength,
the acoustic wave modulates the phase of the beam reflected
30
from the surface relative to the reference beam. This
modulation is detected and by using techniques described by
various authors can be converted to amplitude modulation for
detection by the photodetector [29].
Laser interferometry is capable of very high sensitiv-
ity in the detection of vibrational amplitudes. This techni-
que is ideal for detecting small piezoelectrically induced
vibrations. In the past many authors have employed two beam
interferometers such as Michelson, Fizeau, or Tyman-Green
types. The best of the Michelson interferometers has a sen-
sitivity of io-g cm. Laser interferometers of the Fizeau
type are capable of measuring vibrations of the order of
3x10- 10 cm. Unfortunately, these interferomters must be cal-
ibrated at vibrational amplitudes of the order of io- 5 cm or
larger [ 2] .
A significant improvement in the performance of a
Michelson interferometer was acheived by Sizogric and Gund-
j ian, who were able to measure vibrational amplitudes of
io- 10 cm by use of lock-in detection techniques [21]. Another
advantage of their method was the elimination of the need of
calibration at large amplitudes. However, any Michelson
interferometer design involves two serious disadvantages: it
31
is only a two beam interference device, and it is quite sus-
ceptible to environmental acoustic noises.
Another type of interferometer is the flat plate
Fabry-Perot interferometer which is a multiple beam device,
but its resulting high sensitivity requires that a high
degree of parallelism be maintained between the plates.
Hunsinger used the flat plate Fabry-Perot interferometr sys-
tern for real time analysis of signals generated due to sur-
face acoustic waves travelling on one of the two mirrors of
Fabry-Perot system [7]. A simplified version of the experi-
mental set up used by him is shown in Figure 4.1. One of
the two mirrors of the Fabry-Perot system has a surface wave
coupled to it using a transducer for its generation. The
propagation of SAW on one of the mirrors modulates the width
of the cavity between the two reflecting surfaces of the
Fabry-Perot system giving fringes whose spacings are depen-
dent on the cavity modulation. This modulation is detected
and analyzed. However, two major defects are present in a
system like this: ( 1 ) the system ~equires mirrors with . reflectivity of 95% to 98% which means that the intensity of
the output pattern is very low, and (2) as mentioned before,
the Fabry-Perot system requires a high degree of parallelism
between its two flat plate mirrors, which makes it a very
SURFACE WAVES
INCIDENT BEAM~ __ __._.....,..
INTERDIGITAL CONNECTORS 1--;.."~·
INFORMATION INPUT
FIGURE 4 .1.
32
ACOUSTICAL ABS ORR ER
FLUID COUPLING REGION
: SECOND ORDER L..--=-~-;?: FIRST ORDER
~~~==~::::~! ZERO ORDER ~""""""-~-::::::::::,,......1 FIRST ORDER
: SECOND ORDER
FQURIER PLANE
PIEZOELECTRIC SUBSTRATE
Detection of SAW using flat plate Fabry-Perot interferometer [7].
33
inconvenient device for practical applications. Bruins,
Garland and Greytak developed a spherical Fabry-Perot inter-
ferometric system which, when compared to the flat plate
Fabry-Perot system, has high sensitivity; its transmission
characteristics are changed much less by small angular dis-
placements of the mirrors and therefore it is less suscepti-
ble to acoustic noises. They have measured oscillatory dis-
placements of 4x10- 12 cm [2,6].
A Fabry-Perot interferometer is inherently more sen-
si tve to small changes in optical path than a Michelson
interferometer or other two beam interferometers. This is
due to the sharpness of the multiple beam interference
fringes as compared to those of two beam systems. With phase
sensitive detection of the interferometer output, fringe
sharpness implies a much larger relative change in the out-
put intensity for a given change in the optical path.
Surface acoustic waves have also been studied using
reflected light [20]. In this method acoustic surface waves
with straight parallel wavefronts are launched on a reflect-
ing surface which is illuminated by a laser beam incident
normally on this surface. The reflected wave is a plane wave
as is the incident light wave. Due to the acoustic surface
34
wave, the surface becomes corrugated and the reflected wave-
front parallel to the surface will exhibit a phase corruga-
tion. Amplitude corrugation of the optical wavefront as it
travels away from the surface occurs and this may be
detected and analyzed.
Bulk waves can be detected using the acoustooptical
interaction of light with bulk waves. This involves the dif-r
fraction of light from ultrasonic waves which can occur due
to several reasons. Bulk waves, like sound waves, are long-
itudinal waves. They travel by the displacement of material
along the direction of propagation (longitudinal). As an
analogous case, consider a long tube of water with a piston
transducer mounted at one end as shown in Figures 4.2. When
the transducer surface moves forward, the liquid in front of
the transducer is compressed, and the fluid pressure and
density rise above their unperturbed values, as shown in
Figure 4.2a. This compressed fluid travels forward, com-
pressing the fluid layers next to it, and a compressional
pulse travels down the tube as shown in Figure 4.2b. When
the transducer face moves back, the fluid in front of the
transducer expands, its pressure and density falling below "
the unperturbed values, and a pulse of rarefaction travels
down the tube as in Figure 4.2c. Now if we apply an ~C sig-
35
TRANSDUCER WAT JR PIPE
l~lllll I I I II I I l I I l I I I ITIU \I\ 1111111 / c0 1
I~ I 111111111111111111111111111111111 c b 1
I ~Ill I I 11111111111111111111111111111 cc 1
~ · I I 1~1111 I I 111~1111111111111111111 c d 1
-~ ~ ( e )
I COMPRESSIO N
RAREFACTION
FIGURE 4.2. Passage of ultrasonic compressional waves in water.
36
nal to the tranducer, alternating pulses of rarefaction and
compression will travel down the tube as shown in Figure
4.2d and Figure 4.2e. The refractive index of a transparent
medium is directly dependent on the density of the medium.
Thus, a bulk wave travelling through a semi-transparent med-
ium makes the medium appear like a phase grating to a beam
of light incident on it. By diffraction theory, when a beam
of light encounters a phase grating the output of the grat-
ing is a series of diffraction orders as shown in Figure
4.3. The spacing and intensity of the orders is directly
dependent on the frequency of the phase grating, which in
this case is in one-to-one correspondence with the bulk wave
frequency. Thus, interaction of the bulk wave and light wave
by this technique gives both magnitude and phase information
about the bulk wave.
4.2 MICHELSON INTERFEROMETER
Perhaps the most common and simple interferometer is
the Michelson interferometer. This device consists of a
coherent collimated beam of light which is split into a
reference beam and a signal beam at the surface of a par-
tially reflecting mirror or beam splitter as shown in Figure
4.4. These two beams are reflected from the surf aces of two
TANK
INPUT
BEAM
COM PR ESSlON
RAREFACTION
37
WATER
LENS
TRANSDUCER
FIGURE 4.3. Diffraction due to bulk waves in liquids.
SCREEN
+I
0
-1
38
INPUT BEAM
OUTPUT FRINGE i• PATTERN
REFERENCE
ARM
- -- -SAMPLE
ARM
FIGURE 4.4. Michelson interferometer. The system is very sensitive to changes in either of its arms.
39
mirrors, recollimated and superimposed to create an
interference pattern. The position of this pattern is highly
sensitive to any relative optical phase (path length)
changes between the two beams. These phase differences can
occur due to either relative movement between the mirrors or
a local change in the index of refraction of the material in
the path of one of the beams. These two potential causes of
phase modulation permit accurate measurement of both small
displacements by reflection and small changes in index of
refraction by transmission. The absolute magnitude of the
effective pathlength changes in both the cases are small
with respect to the wavelength of the light source.
Since the input beam undergoes amplitude division at
the beam splitter to produce the signal and reference beams,
these beams are of equal amplitude and the same frequency
under ideal conditions but they differ in phase depending on
the distances they travel independently. Assuming an arbi-
trary relative phase difference,
represented mathematically as:
these two beams can be
E E 0 sin(wt+k(x+6x)), and (4.2.1) s
E = E 0 sin(wt+kx), (4.2.2) r
where ox is the difference in optical path between the two
beams and k is the propagation constant.
40
If these two beams are collimated and superimposed, the
total field E at the output may be written as:
E = E +E . s r (4.2.3)
Using trignometric identities and subsequent simplification,
Equation 4.2.3 then becomes
where
E E sin[wt+kx+(kox)/2], m
Em= E 0 cos[(kox)/2].
(4.2.4)
Equation 4.2.4 clearly shows the dominance of the ox
term in the amplitude Em of the final output field E. If ox
<< \ the resultant output field E has an amplitude almost
equal to 2E 0 ; while if ox= A/2 it is zero. This gives rise
to a series of bright and dark lines due to constructive and
destructive interference.
Thus, for
kox/2 = (2n+l)TI/2, (4.2.5)
cos[(kox)/2] = 0,
where
k = 2TI/L
Equation 4.2.5 becomes
41
ox = (2n+l)A/2, (4.2.6)
where n 0,1,2,3, ... giving rise to destructive interfer-
ence.
Similarly,
cos[k6x/2] 1
when
kox/2 = nTI. (4.2.7)
Using the previous substitutions this becomes
ox = nA., (4.2.8)
where n = 0,1,2,3,
ence.
giving rise to constructive interfer-
Although the Michelson interferometer is highly sensi-
tive it has some very serious disadvantages. These include:
l. High susceptibility to low frequency vibrations
and DC movements of the signal or reference mir-
rors
2. Critical alignment of the entire interferometric
system
42
3. Inability to be tuned to any one particular
£regency for the detection of surface acoustic
waves
In addition, due to its construction and severe limitations
it has to be mounted on a relatively heavy and vibration
free optical table, making it extremely inconvenient for
pratical use in the nondestructive testing of large struc-
tures.
4.3 STABILIZED PATH INTERFEROMETER
Palmer and Green developed an interferometric technique
which uses a closed loop feedback system to stabilize a
Michelson interferometer with respect to low frequency vib-
rations and DC movements of the signal mirror [30]. Here,
the low frequency and DC signals are detected by the photo-
detector as shown in Figure 4.5 and fedback to a piezoelec-
tric crystal which has the reference mirror mounted on it.
The reference mirror moves in accordance with the signal
mirror for "noise" frequencies, resulting in the effective
neutralization of relative path changes due to DC or low
frequency movements of either of the two mirrors. Although
this system does eliminate the problem of low frequency
noise vibrations, it retains other disadvantages including
Specimen
Photodetector
43
Control Circuit
RF Amplifier AE Signal Output
FIGURE 4.5. Stabilized optical path interferometer. The stabilizing circuitry eliminates the low frequency noise vibrations (less than 1 .kHz) and also makes the system relatively insensitive to DC movements of the specimen [30].
44
critical alignment, inconvenience, and the potential for
nonlinear closed loop feedback instability.
4.4 DIFFERENTIAL INTERFEROMETER
The interferometric technique developed by Palmer,
Claus and Fick solved most of the problems encountered by
the Michelson interferometer. See Figure 4.6. The differen-
tial interferometer is insensitive to low frequency vibra-
tions and eliminates the need for critical alignment of the
specimen surface. It can also be tuned to detect surface
acoustic waves with frequencies ranging from 20 kHz to above
200 MHz. Other advantages of this technique include [23],
1. The output
optical path
signal is directly proportional to
changes so that both amplitude and
phase of an acoustic wave can be measured.
2. For the same reason, surface, dilatational, and
shear waves can be measured.
3. Absolute calibration is easily accomplished.
4. Waves can be measured on a point-to-point basis in
any plane of interest in or on a specimen.
MASK BEAM EXPANDER AND COLLIMAOTR --------...
I LASER]~' 480 Hz Ll L2 H L3
CHOPPER :J·~ REF. I
L4
M
VARIFOCAL LENS ~
R F SIGNAL OUTPUT
SPECIMEN
,,,,-: --
~ /
t MECHANICAL
DRIVE
FIGURE 4.6. Experimental setup for a two beam differential interferometer. The expanded laser beam illuminates the holographic divider H and mask M transmits the two desired beams for the interferometer. The output fringe pattern is spatially filtered by grid G [23].
+:> U1
46
5. In some cases where both dilatational and shear
waves are present,
isolated.
the two types can be easily
Using their notation, two collimated beams, incident on
a varif ocal lens system, are focused at points P and Q on
the surface of an unperturbed specimen as illustrated in
Figure 4.7 (10). The two beams make a small angle 8 with
respect to the z axis.
cally as,
These can be represented mathemati-
E 0 expi[w 0 t-k(xsin8+zcos8)+¢], and
E2 = E 0 expi[w 0 t-k(-xsin8+zcos8)+¢],
(4.4.1)
(4.4.2)
where ¢ is half the phase difference between the two beams,
w0 the optical radian frequency, k the propagation constant,
and E 0 the wave amplitude.
The two beams, reflected from the specimen surface, are
collimated by the lens and superimposed to give a total
field E, in the region of overlap, where
E = E1 +E 2 • (4.4.3)
Use of trignometric identities and additional simplification
yields,
47
z -8 +8
x VARI FOCAL LENS
F
J_ --........ ......--....... p -- ,,.- Q __ , __ _ ..--- ___ SPECIMEN
r--.A12--..: PLANE I
FIGURE 4.7. Basic two beam differential interferometer geometry with beams focussed at points P and Q which are half an acoustic wavelength apart. The reflected wavefronts emerge at an angle to the normal and superimpose to form an interference pattern [10].
48
E = 2E 0 [expi(w 0 t-kzcos8)]cos(kxsin8+¢). (4.4.4)
The total optical irradiance is given by the product of the
complex conjugates of the total ouput field:
H EE* I
H = 4E 0 2 cos 2 (kxsin8+¢). (4.4.5)
Since 8 is very small, sin s~s and
(4.4.6)
This equation represents the straight line interference pat-
tern. From this equation it can be deduced that H is a maxi-
mum when cos 2 (kx8+¢) is a maximum. The cosine term is maxi-
mum for
kx8+¢ = m1T, m O, l,2,3, • • • /
x = (m1T-¢)/k8. (4.4.7)
The values of x give the positions of intensity maxima, or
constructive interference.
Similarly, H is a minimum when the cosine term is a
minimum. This occurs when
kx8+¢ = (2n+l)1T/2, n O, l,2,3, • • • • /
49
x = (n(2n+l)/2 - ¢)/k8, (4.4.8)
giving the positions of intensity minima, or destructive
interference.
The fringe spacing ox (distance between two maxima or
two minima) is given by
ox = x -x m m-1
= (mn-¢)/k8 - ((m-l)n-¢)/k8
= 1T/k8 I (4.4.9)
or, since k = 2n/A.,
x = A./28. (4.4.10)
As seen from Figure 4.8, and derived later in this sec-
tion, maximum signal sensitivity is obtained when points P
and Q are separated by half the acoustic wavelength A/2.
For small angles 8,
tans ,,,9 (4.4.11)
Thus,
(A/2)F = 28, and (4.4.12)
F = A/48 = oxA/2A.. (4.4.13)
50
BEAM I BEAM 2
NARROWBAND DIFFERENTIAL INTERFEROMETRY
W(x,t) = 2A sin ( w0 t - Kx)
~x = (2n +I )A/2
n = {0,1,2,3, ... }
A = 27T/K
FIGURE 4.8. Positions of the beams on the specimen surface for a narrowband differential interfer9meter {24].
51
Equation 4.4.9 shows that F, the focal length of the
lens system, is proportional to the surface acoustic wavel-
ength. Thus, to have the system tunable to any desired fre-
quency we need a varifocal lens system. Letting d = 6x and
substituing the above derived values in Equation 4.4.5, we
obtain
H 4E 0 2 cos 2 [(nx/d)+¢]. (4.4.14)
Referring to Figure 4.4.4, assume a surf ace wave of
frequency f velocity v, wavelength A and amplitude E 0
traveling on a specimen surface. Two optical beams 61 and 62
separated by a distance d, probe at points P and Q on the
specimen surface. Let the surface displacements at P and Q
be denoted as,
61 = E 0 cos(2nft), and
62 = E 0 cos(2nft-2nd/A).
The total phase difference is given by 6
6 = E 0 [cos(2nft) - cos(2nft - 2nd/A)].
Differentiating the above equation results in,
d6/dt = E 0 [-sin(2nft) +
sin(2nft - 2nd/A)]2nf.
(4.4.15)
(4.4.16)
52
Equating this to zero and solving for t we get,
t = (l/2nf)arctan[(sin2nd/A)/(cos(2nft)-l)]. (4.4.17)
The above derived value for t can either be a maximum
or a minimum. To resolve this situation we differentiate
Equation 4.4.16 again
d 2 o/dt 2 = E 0 [-cos(2nft) + cos(2nft - 2nd/A)]4n 2 f 2 .
(4.4.18)
To find the maximum value of function o, Equation
4.4.14 should be less than zero. Thus,
cos(2nft) < cos(2nft - 2nd/A}, (4.4.19)
cos(2nft) < cos(2nft)cos(2nd/A) + sin(2nft)sin(2nd/A),
(4.4.20)
cos(2nft)[l - cos(2nd/A)] < sin(2nft)sin(2nd/A}, and
(4.4.21)
tan(2nft) > [l - cos(2nd/A)]/sin(2nd/A). (4.4.22)
Equation 4.4.22 is the condition on t for which o can
be a maximum. This is satisfied by Equation 4.4.17. Thus,
Equation 4.4.17 gives the value fort= t . Using this value m
oft in Equation 4.4.15 we get, m
53
6 = E 0 [cos(2nft ) - cos(2nft - 2nd/A)]. m m m (4.4.23)
Assuming, for simplicity, a value of t such that
cos(2nft) = 1, a graph of 6 as a function of d/A is plotted
as shown in Figure 4.9 [24]. From the graph it is apparent
that the maximum for 6 is obtained when d/A = 0.5 or an odd
multiple of this, i.e. ford/A= (2n+l)/2, for n=0,1,2, ..
Figure 4.10 shows the graph with 6 plotted as a func-
tion of frequncy with d/A chosen for a maximum sensitivity
for a surface acoustic wave of 1 MHz on glass. It can be
seen from plots a, b, and c that the bandwith dro~s off as
d/A increases from 1/2 to 5/2. Ideally, infinitely small
bandwith is possible and is limited only by the equipment
used [24].
-CD 'O ->-~
> ~ Cf)
z w Cf)
er w
0
- 5
~ -10 ~ 0 er w u.. a::: w -15 ~ z
54
BANDWIDTH at -3 dB
POINTS
di.A = O· 5 ()..
-3 dB -3 dB
-20!.._~~___....~~~-+--~~~~~~~-
FIGURE 4.9.
n n+Q·25 n+0·50 nf().75 n-+1·00
d/A.Q.
Interferometer sensitivity as a function of beam spacings d and acoustic wavelength, plotted using Equation 4.4.23 [24J.
dB
55
0 BW = f
d = A/2
-10
-20 f
0 BW = f/3
d = 3A/2
-10
-20 f
0 BW = f/5
d = 5A/2
-10
FIGURE 4.10. Sensitivity of a differentiai interferoweter is directly related to the spot separation d between the two beams on the specimen surface [24].
Chapter V
FIBER DIFFERENTIAL INTERFEROMETER
5.1 DIFFERENTIAL FIBER SYSTEM
Although highly sensitive, the differential interferom-
eter and other optical detection systems are not useful for
the practical nondestructive evaluation of large specimen
surfaces because the alignment and relative positioning of
the optical components is critical and requires the use of a
massive and vibration-free support table. To eliminate this
disadvantage a similar system has been developed which
effectively separates the fixed input optics from a portable
remote detection head using single mode fiber waveguide. In
this system a 2.0 mW helium-neon laser and beam shaping
optics are rigidly mounted in one enclosure as shown in Fig-
ure 5.1. The coherent light beam is amplitude divided into
two beams which are focused using lOX microscope objectives
onto the ends of two ITT-110 single mode fibers having nomi-
nal 4.5 micron diameter cores. To simplify the procedure of
focusing the beams on such small areas, the cut and modes-
tripped ends of the fibers were mounted in six-axis posi-
tioners. The two fibers, each two meters long, transmitted
the light to the remote detection head through a flexible
cable assembly.
56
LASER BE.AM +V REMOTE DETECTION
HEAD
I '•<c aV P
10 x FOCUSING EYEPIECE
~
FIBER 1 HOLDER
FlBER
AMPLIFIER
SIX AXIS POSITIONERS
SPECIMEN/ SURFACE
DIGITAL STORAGE
OSCILLOSCOPE
FIGURE 5.1. Fiber Differential interferometer. The input laser beam is split into two beams of equal amplitude and focussed onto two ends of optical fibers poitioned using six axes positioners. These fibers transmit the beams to a remote detection head.
I _/
Ul '--1
58
Inside the remote detection head, the fibers are
mounted parallel with their adjacent ends spaced 1.0 mm
apart as shown in Figure 5.2. The beams emitted from the
ends of the two optical fibers are then focused, using a
varifocal lens system constructed of four lenses, to points
P and Q on the specimen surface. Here, the lenses Ll and L4
are fixed lenses with the position of lens L4 adjusted so
the specimen surface is always in its back focal plane.
Lenses L2 and L3 are movable lenses which can be translated
by microprocessor-controlled stepping motors to change the
focal length of the entire varifocal length assembly, thus
changing the separation between spots P and Q. Spot separa-
ti on, as explained in Chapter 4, tunes the interferometer
to be highly sensitive to one particular SAW frequency. A
computer program for calculating the positions of lenses L2
and L3 which are required for various spot separations and
corresponding surface wave frequencies is given in Appendix
B.
The focused beams are reflected from the specimen sur-
face and superimpose to give an optical interference pattern
as shown. This interference pattern is spatially filtered
using a Ronchi ruling with a grid spacing equal to the spa-
tial periodicity of the pattern. The output of this filter
CABLE
FIGURE 5.2.
SPATIAL FILTER
BEAMSPLI TTER
~=r=====_J~p
L4
DETECTOR
SPECIMEN SURFACE
Remote detection head. Lenses L1 L2 , L3, and L4 form a varifocal lens system for focussing the two beams onto the specimen. Lenses L and L3 are movable lenses for tuning the interferometer. Lenses L. ana L4 are fixed lenses with specimen lying in the back focal plane of lens L4 . The reflected interference pattern is spatially filtered by the spatial filter and detected by the photodetector.
\JI \()
60
is then focused onto the optical detector which demodulates
the intensity variations and generates an electronic signal
proportional to instantaneous surface displacement. This
signal is electronically filtered and acquired by a digital
storing oscilloscope where it can be processed.
5.2 MAXIMUM PERMISSIBLE DC MOVEMENT OF THE SURFACE
The beam emmitted from a laser has a Gaussian profile
wavefront [33]. At large distances z from the waist as shown
in the Figure 5.3, this wavefront is essentially, a spheri-
cal wave radiated fromn a quasi-point source located at the
waist position. The far field angle 8 of the beam may be
defined as [ 33],
8 = w(z)/z ::: \/(nw 0 ), Z >> Zo (5.2.1)
where w0 is the half power radius of the waist of the beam
at position z 0 , w(z) is the waist at some position z,
is the wavelength of the light beam.
and \
Gaussian beams can be focused to extremely small spots
making them useful for point, probing, local heating, for
drilling holes and generally in carrying out operations in
area only a wavelength or two in diameter [33]. The waist
radius w0 of the focused spot shown in Figure 5.4 ~an be
shown to be,
Xo1'jo
..; Wo
WAIST (z =0)
61
x,y
-\ e 1~
z
FIGURE 5.3. Gaussian wavefront in the far field propagating from a waist located at z=O. The angle at which a gaussian beam diverges or converges from the waist is inversly proportional to the spot size w at the waist [33).
0
62
w'
d
1 _, ___ _
FIGURE 5.4. Gaussian beam of diameter d focussed to a spot of diameter d [33].
0
63
w0 = 2F\, (5.2.2)
where F is the f number of the lens system given by,
F = f/d, (5.2.3)
where f is the focal length of the lens system and d is the
aperture diameter or the waist of the input beam (which ever
is smaller).
Thus for a collimated beam of spot size w, again shown
in Figure 5.4, incident on the lens, the two spot sizes, w0
(waist radius of focused spot) and w can be related by (33],
wo = fA/(Tiw). (5.2.4)
Using the criterion that the focusing lens must have a diam-
eter d=3w to pass the incident light, and since 86% of
energy will be focused into the area of diameter 2w 0 , the
focused spot can be defined to have a full diameter of only
d 0 = 2w 0 (33). This focused spot diameter then gives,
d 0 "' 2£\/d, (5.2.5)
where F = f/d "' f/3w, thus,
d"' 2FL (5.2.6)
A collimated beam of waist radius w0 diverges bet'ore
and after collimation. The waist size of the diverged beam
can be written as [33],
w(z) = Wo
64
~ [l+(Az/(1TW02))2] 2, (5.2.7)
where w(z) is the waist at some point z as shown in Figure
5. 5.
Assuming w0 = A/10, where A is the SAW wavelength, we
can calculate the maximum distance the mirror can move for
change in spot radius by 10%. Thus, using Equation 5.2.7,
for a change in spot radius by 10%, i.e. w(z) = 1.1 x w0 ,
l.lw 0
0.21
~ w D [ 1 + ( ( AZ ) I ( 'ITW D 2 ) ) 2 l 2 I
Z = 0 . 461TW o 2 /A.
Using Equation 5.2.4 Equation 5.2.10 becomes,
(5.2.8)
(5.2.9)
(5.2.10)
(5.2.11)
where w1 is the diameter of the input beam. This z is the
movement of surface in one direction only. Thus the surface
can move 2z before it spot radius increases more than 10% of
its minimum value w0 •
Using actual values for f which is 50 mm, A. is 6328 x
10- 10 m and w is 20 mm in Equation 5.2.11, we get the maxi-
mum permissible distance to be,
z - 11.6 x 10-4 mm.
65
l --·- .-.---·--·1-·-
I 2z = 2 7T'W! If
RAYLEIGH RANGE
FIGURE S.S. Collimated gaussian laser beam. This is actually a long slender beam waist of length 2ZR, where ZR is defined as the distance from the waist to the point where the beam area has doubled (33].
66
5.3 MEASUREMENTS
The fiber differential interferometric system was
applied to the detection of pulsed broadband ultrasonic sur-
face waves similar to those generated by acoustic emission
events in stressed solids. To simulate these events, 0.5mm
diameter graphite pencil lead was broken against the surface
of a front surfaced mirror. Several authors have investi-
gated the acoustic signals produced by such a source and
have shown that the resulting particle displacements approx-
imate those which in principle would be generated by a step
function load applied to the surface (31,32]. In these
experiments, the normal component of the particle displace-
ment was detected at several positions near the location of
the acoustic source. Typical output from the digital oscil-
loscope is shown in Figure 5.5 and compared to theoretical
predictions.
5.4 RESULTS
The fiber differential interferometer allows the prac-
tical detection of surface displacements on large material
structures using sensitive optical techniques. All of the
optical components which require either stable alignment or
critical adjustments are housed in a rigid enclosure. This
10
rnV/div.
"' u '1 1 J.-'- 6.2 '.). 3
,.., ••J
x 10 sec.
17- .11 1.5. 5 18.6
FIGURE 5.6. Data got by generating SAW on specimen surface by breaking 0.5 mm. pencil leads against the surface.
"' '-J
68
enclosure is connected to a small detection head using
cabled optical fiber waveguide. The head then may be scanned
conveniently over the surface of the specimen without moving
the entire optical system. Potential applications in a var-
iety of nondestructive evaluation environments are sug-
gested.
Chapter VI
BULK WAVE DETECTION USING DIFFERENTIAL INTERFEROMETRIC TECHNIQUES
6.1 TECHNIQUE FOR THE DETECTION OF BULK WAVES
The detection of bulk waves in transparent solid and
liquid media usually involves the acoustooptic interaction
between the waves and a beam of light. One such technique
has been briefly descibed in Chapter 4. Our goal in this
research was to develop an optical system for the detection
of compressional waves in transparent, specifically liquid,
media, which
1. Was insensitive to low frequency vibrations,
2. Could be used to determine the direction of propa-
gation of standing or traveling compressional
waves,
3. Had sensitivity which was tunable over a range of
ultrasonic frequencies, and which
4. Was sensitive to a pulsed acoustic wideband bulk
wave traveling through liquids.
These requirements suggested modification to the type
of differential interferometric system developed by Palmer,
69
70
Claus and Fick [23]. Since their two beam system could not
accurately determine the direction vector of the bulk wave,
modifications were needed to develop a four beam differen-
tial interferometer.
6.2 TWO BEAM DIFFERENTIAL SYSTEM FOR BULK WAVE DETECTION
Referring to Figure 6.1, a 2.0 mW helium-neon laser
beam is expanded and collimated to give a beam 1.0 cm in
diameter. This beam is incident on a Ronchi ruling with a
grid period of 200 lines/inch. The resulting output diffrac-
tion spectrum is then focused using lens Ll with a 200 mm
focal length onto an aluminium mask. The mask allows only
the +l and -1 spectral orders to be transmitted. Lenses L2,
L3, and L4 form a varifocal lens system which collimates the
two beams and individually focuses the beams inside the tank
so the diameter of each focused beam is less than one tenth
the wavelength of the ultrasonic bulk wave. The tank itself
is constructed using 4 cm x 4 cm glass slides with a 1.5 cm
diameter X-cut quartz crystal transducer mounted at the bot-
tom of the tank as shown in Figure 6.2. The beams emerging
from the tank are superimposed using a long focal length a
lens and the resulting interference pattern is spatially
filtered by a Ronchi ruling with a grid spacing 0~ 133
LASER
BE AM COLLIMATOR
L2
~ RONCHI GRID G1
TRANSDUCER
TANK WATER
MIRROR
10 x EYEPIECE
L5------
RO NC HI GRID I I ·zg G2 . I
L6
PHOTO DETECTOR -------. DIGITAL
STORAGL OSCILLOSCOPE
~~·-\ I
FIGURE 6.1. Two beam differential interferometric system for detection of compressional waves in water. Ronchi grid G1 illuminated by an expanded laser beam is imaged onto a mask wnich permits only the +l and -1 orders of diffrction pattern to pass through to form the interferometer. Lenses L3 and L4 form the varifocal lens system. Lens L5 collimates and superimposes the two beams to give an interference pattern which is spatially filtered by G2 .
---1 I-'
GLASS SLIDES
~ , ,
I
I I
I
I I I ' I I
72
~-- -- - - - - - -I I ,. . ' '
I !-·· • - ·-- - - - - - -
I I
I
I ,.
LEADS
I
----_.,..__._1
TRANSDUCER
FIGURE 6.2. Water Tank used for detection of compressional waves in water.
73
lines/inch. The spatially filtered pattern is focused onto a
photodetector receiver which demodulates the optical signal
and generates an rf electronic signal. This . 1 . s1gna~ is fil-
tered and stored using a digital storing oscilloscope.
The experiment was performed in two parts. The two
beams in the tank were separated by 0.275 cm which is 8.65 x
A/2 where, A is the wavelength of the bulk wave which in
this case had a frequency of 2.25 MHz. First, a sinusoidal
signal with a 300 volt peak-to-peak amplitude was applied to
the transducer to produce a sinusoidal bulk wave of fre-
quency 2.25 MHz. The output as seen by the detector was a
sinusoidal wave with an amplitude dependent on the relative
position of the beams in the tank. Due to the size of the
tank, a standing wave was set up and, as the beams were ver-
tically scanned, the amplitude of the signal varied as shown
in Figure 6.3. This variation agrees with the theory that
describes the dependence of the sensitivity of the system on
the relative focus positions of the two beams on the sta-
tionary waves. This is shown in Figure 6.~.
The second part of the experiment consisted of the
detection of a pulsed ultrasonic bulk wave traveling in the
water. The pulsed broadband bulk wave was generated by
->O mV/<li'l.
<J ;:J p, J,J ;:l 0
)1 0 jJ (.) Q) .:J CJ ~
0 J L I I I I I
2.5 5.0 7.5 10.0 12.5 15.0 17.5 -3 x 10 m.
Vertical Displacement of the tank.
FIGURE 6.3. Data got by scanning the two beams of the two beam differential interferometer across the standing wave generated by a 2.25 MHz sinusoidal wave. The beams scanned the water tank vertically, for a distance of 20 mm.
'-l ~
75
L, WATER TANK /
l .-----·---
p
p
A;---.1 ~f;-1-?Zi?A-m -+-rl--111'
TRAN SO UCER
Q
(a)
LASER BEAMS
z
~A-I
p Q
z
FIGURE 6.4. Positions of the laser beams on the compressional waves travelling in water (a) maximum sensitivity of the system occurs when P and Q are half the acoustic wavelength apart, and (b) the system is least sensitive when the beams are separated by a multiple of the acousttc wavelength.
76
applying a 300 volt 10 nanosecond pulse to the transducer
using a Metrotek MP215 pulser u~it. Typical recorded results
from this experiment are shown in Figure 5.5; other results
are included in the Appendix C. Theoretical calculations for
a bulk wave traveling with a velocity of 1430 meters
second predict that such a pulse would take 1.8 microseconds
to travel the distance of 0.275 cm between the two beams.
Refering to Figure 6.5, points A and B are 1.8 microseconds
apart and are also 180 degrees out of phase, which is also
predicted by theory. The pulse continues to reflect in the
tank and crosses the two beams several times before it is
significantly attenuated. The timings for the pulse cross-
ing the beams, which appear in the output as points C, D, E,
and F, were noted as shown in Figure 6.6 and were within
3.6% of the calculated theoretical values. The calculated
and the observed values are listed in Table 6.1. From this
table one notices discrepancy in the results towards the
later part of the table. This is probably due to the trans-
ducer not being perfectly horizontal and the pulsed bulk
wave not traveling perpendicular to the beams as was assumed
for the theoretical calculation. To rectify this problem,
the four beam system descibed below was developed.
c B
so ~nv I div.
0 31.0 62.0 93.0 -6 x 10 sec.
124.0 155.0 186.0
FIGURE 6.5. Data for detection of a traveling ultrasonic pulse packet in the tank using the two beam differential interferometer.
.~
'-.] '-.]
LASER BEAMS
PATH
78
..__ ___ .... '9F.\--· -__ ._,,,_,, -
~ t ~ ' ' I • ' . : ' I I
t~ i I '
I • I t ' ' . •.
TRANSDUCER
(a)
n . \ • • I
OF
TANK
WATER
PATH OF THE PULSE
TANK
~ LASER BEAMS
THE PULSE TRANSDUCER
( b)
FIGURE 6.6. Path of ultrasonic pulse in water tank. (a) Water level is parallel to the transducer. (b) Water level is at any arbritrary angle to the
transducer.
79
PATH OF ULTRASONIC r PULSE
__ ----:-~- ___ I WATE~ I , ! l 23· 75 mm
36-75 mm 2 ·75 mm
l _i r 2Z5 mm
t 2·5mm TRANSDUCER
POSITION
A B c D E F H G
LASER BEAMS
TABLE G .1.
DISTANCE TRAVELED BY PULSE
mm
7.75 10.50 58.00 60.75 76.25 79.00
126.50 127.25
TIME TAKEN TIME TAKEN CALCULATED EXPERIMENTAL
VALUE VALUE -6 x 10 sec -6 x 10 sec
5.419 5.4 7.343 7.2
40.559 38.7 42.482 40.8 53.320 55.240 88.460 84.9 90.380 88.2
Data for the detection of ultrasonic pulse in water using two beam sytem.
80
6. 3 FOUR BEAM DIFFEP.ENTIAL SYSTEM FOR DETECTION OF BULK ---WAVES
The four beam differential system is a modification of
the basic two beam system. Effectively, it is a dual two
beam differential interferometer of the type discussed by
Turner and Claus [15]. Their system, however, is too bulky
and rather difficult to set up. Due to fewer critically
aligned optical components, the four beam system described
here is relatively insensitive to small misalignments.
Referring to Figure 6.7, a 2.0 mW helium-neon laser
beam is expanded and collimated to give a beam 1.0 cm in
diameter. This beam is incident on a pair of Ronchi rul-
ings, with grid periods of 200 lines/inch, placed such that
the ruling lines are at 90° to each other and the ruled
sides are facing each other, preferably against each other
as shown in Figure 6.8a. The resulting output diffraction
spectrum, similar to the diffraction pattern from a square
hole as shown in Figure 6.8b, is then focused using lens Ll
with a 200 mm focal length onto an aluminium mask. The mask
allows only the the +l and -1 spectral orders, i.e. beams
8 3 and 64 , to be transmitted such that they lie at
the four corners of a square just above the transducers in
the water tank. Lenses L2, L3, and L4 form a varifoc~: lens
CROSSED
LASER ~ •
BEAM EXPANDER ! AND CO LUMA "TOR
-- HORIZONT Al PAIR OF BEAMS
---- - - VERTICAL PAIR OF BEAMS
DIGITAL STORAGE
OSCILLOSCOPE
L2
TRANSDUCER
TANK
.:.~·.· ..
WATER MASK
-·-/=11.-~2 ... LI •r- ..,.,..,. __
MIRROR
I Ox EYEPIECE
RONCHI GRID 62 --
L6 PHO TODETECTOR
----------. l AMPLIFIER ·~
['JGlJRI!: 6, 7. ~·our beaio differential J.nterferometer for detection of ultrasonic com1>ress1onal waves in water. 'fhe crossed paJ r of Ranchi grids illuminated by an expanded laser beam is imaged onto a mask M1 which p~rmits the +i and -1 orders to pass through, Mask M selects Che desired pair of beams to be transmltteJ to detection optics. ~he interference pattern is spatially filtered hy Rond1i grid G7 and detected by Lhc photodetector.
co I-·-'
PLANE WAVE
82
RONCHI RULING
• • • •
(a) Diffraction pattern due to a single Ranchi ruling.
PLANE WAVE CROSSED RONCHI RULING
LENS
• • • • • • • • • •
(o). Diffraction pattern due. to a pair of crossed Ranchi rulings-.
FIGURE 6,8.
83 . system which collimates the four beams and individually
focuses the beams inside the tank so the diameter of each
focused beam is less than one tenth the wavelength of the
ultrasonic bulk wave. The tank itself is constructed using 4
cm x 4 cm glass slides with a 1.5 cm diameter X-cut quartz
crystal transducer mounted at the bottom of the tank as
shown in Figure 6.2. The beams emerging from the tank are
are then filtered using a mask M2 such that only two diago-
nally opposite beams are transmitted to detection optics.
The detection of the pulsed compressional waves in
water was performed in two parts. First, the mask M2 tran-
smitted only the vertical pairs of beams to the detection
system. For the next part the mask was rotated to transmit
the horizonatal pairs of beams. The transmitted beams in
both cases are then superimpos-ed using a long focal length
lens and the resulting interference pattern is spatially
filtered by a Ronchi ruling with grid spacing of 200
lines/inch. The spatially filtered pattern is focused onto a
photodetector receiver which demodulates the optical signal
and generates an rf electronic signal. This signal is fil-
tered and stored using a digital storage oscilloscope. The
two sets cf signals, one produced by the horizontal pair of
pair of beams and one by the vertical pair, is then analyzed
84
to give the required data on the direction and magnitude of
the pulsed wave.
The inconvenience of rotating the output optics for
detection of the second pair of beams can be avoided by sim-
ultaneous detection of both the horizontal and vertical
pairs of beams as shown in Figure 6.9. The beam pairs can
be isolated by using pair of thin mirrors to reflect the
horizontal pairs of beams and transmit the vertical pairs of
beams. However, this cannot be done by etching a transparent
line in the mirror because the glass from the etched part
still reflects. Though weak, this reflection tends to inter-
fere with the inteference caused by the horizontal beams,
hence an arrangement consisting of two mirrors, with a small
gap between them for transmission of the vertical pairs of
beams, has to be used for reflection of the horizonatal
pair.
To detect a pulsed ultrasonic bulk wave traveling in
water, a pulsed broadband bulk wave was generated by apply-
ing a 300 volt 10 nanosecond pulse tb the transducer using a
Metrotek MP215 pulser unit. Typical recorded results from
this experiment are shown in Figure 6.10; other results are
included in the Appendix D. Theoretical calculati0n~ for a
CROSSED RONCHI GR ID MASK TANK G1 \.,. ~
WATER SPLIT
\--~J~ .. ·-=-=--_-~4-+=. -.;;=~-~~~,:.,/~ LASEll__j-~. - . -- I
----------BEAM EXPANDER I • L 2 L3 L4 f=" 0 t MIRROR!:
; . A ND COLLIMATOR
__ llORIZONT AL PAIR OF BEAMS
VERTICAL PAIR OF BEAMS
DUAL CHANNEL DIGIT AL STORAGE
OSCILLOSCOPE
TRANSDUCER L~......---
. . . I
~~ ·., ..
~ E yEPIECES * . : \ i I RONcH1 GRm · mnmlrmmumnnrm G2'
62 l l : I
Le--_ ---
I A.MPLIFIE8=1------
~ ~MPLIFIER l----
!.!~ 6'--,~
9 FIGURE 6.9. Hodified four beam differential interferometric syotem for detection
of the direction of the compreosional waves in water by simultaneous evaluation of data from the horizontal nn<l vertical pairs of beams.
0:) U1
-·A llB
30
mV/div.
0 7.75 15.50
C1 D
23. 25 x 10-6 sec.
31.00
F
E
38.75 46.50
FIGURE 6.10. Detection of an ultrasonic pulse packet traveling in a water tank using the four beam differential system. (A) This is data got by analyzing the interference pattern caused by
the vertical pair of beams.
00
°'
87
bulk wave traveling with a velocity of 1430 meters per sec-
ond predict that such a pulse would take 4.2 x 10- 5 seconds
to travel the distance of 0.6 cm between the two beams.
Referring to Figure 6.10, points A and Bare 3.9 x 10- 5 sec-
onds apart and are also 180 degrees out of phase, which is
also predicted by theory. The pulse continues to reflect in
the tank and crosses the two beams several times before it
is significantly attenuated. This explains the generation
of other pulses. The calculated and the observed values are
listed in Table 6.2. As can be seen from table 6.2 the
experimental and theoretically calculated results differ are
within 3.5% of the calculated values. This difference can be
attributed to various reasons. However, the major reason
could be the level of water not being perfectly parallel to
the transducer as discussed before.
Measurements to detect the direction of propagation of
the pulse packet were made. A pair of diagonally opposite
beams were allowed to interfere. The data obtained from this
is shown in Figure D.4. Next the remaining diagonally oppo-
site pairs of beams were used. The data obained from this
is shown in Figure D.S. Both of these results were stored
on a floppy disk in the digital storage oscilloscope. For
reasons discussed in Appendix D accurate direction of the
88
propagation of a pulse packet could not be determined. The
simultaneous detection technique discussed above will give
accurate results.
6.4 RESULTS
The two beam and four beam differential interferometric
systems for the detection of direction of the propagation of
the ultrasonic pulse packet in water were developed and
used.
rnent.
7.
These are basic systems and require further develope-
Some suggested improvements are discussed in Chapter
POSITION
A A' B c ()'
D E E'
0.53crn
~, 1~ WATER
f t ----···----:-····-;;-,---. I PATii OF ULTRASONIC PULSE I I· ···---;-) • 65cm I +: ..
3 05 _u_ --------1~!.~-~l~·-'·~-------. cm I 1 O. 5cm _____ ..,..11 . .. ~l--~o' • .L ___ tf..... .... ~ o oc;cni -rL .... --~~-e\ ..... /o··· :·"-------··· .ta5 ci! . ...
... , _j__
t THANSDUCER d 1,<l2 ,d 3 , and d4 are
focussed laser beams.
VEHTICAL PAlR OF BEAMS llOIHZONTAL PAIR OF BEAMS DISTANCE TRAVELED TIME TAKEN TIME TAKEN TIME TAKEN TIME TAKEN
UY TllE PULSE CALCULATED EXPERIMENTAL CALCULATED EXPERIMENTAL VALUE VALUE VALUE VALUE
-6 -6 -6 -6 cm x 10 sec. x 10 sec. x 10 sec. x 10 sec.
0 0 0 0 0 0.05 - - 0.35 0.3 0.55 3.85 3.825 3.85 26.93 26.935 4.35 - - 30.42 4.40 30. 77 29.950 30. 77 6.10 42.26 41.50 6.15 - - 43.01 Lil. 75
TABLE 6.2
Data for detection of pulsed ultaso11ic wave in water using four beam differential interfernmetric system.
00 \()
Chapter VII
CONCLUSIONS AND FURTHER REFINEMENTS
The fiber differential system developed was sensitive
to pulses generated by step impulse functions. However, the
system barely detected the continuous SAW generated on the
mirror surface by a wedge transducer.j.This lack in sensitiv-"\
ity can be attributed to various practical difficulties
involved in the system.\ Considering the system itself, due
to the use of single mode fiber the intensity of the output
pattern is low. This is further reduced considerably by use
of two beamsplitters; more than 50% of the intensity of the
output pattern is lost at each beamsplitter. This low inten-
sity coupled with a shot noise limited wideband detector
made it difficult to see SAW signals of very low magnitude.
Laser power could not be increased as laser noise increases
with power of the laser. Recommended improvements in the
system would be (1) an electronic detector which has a
higher signal-to-noise ratio and which can be tuned to
reject the laser noise, (2) custom made biconvex or plane-
co~vex lenses be used because aspheric lenses have tc be
used within the paraxial region 6nly or the output pattern
is distorted, ( ( 3) input laser power be increased,) ( 4) fiber
system be improved to avoid the use of two beamspl~tters,
90
and if possible,
be used.
( 5 )
9l
single mode fibers of larger diameter
The two beam system for detection of bulk waves was
more sensitive to pulsed and countinous compressional waves
in water than the four beam system. This again was due to a
great reduction of intensity of the output pattern when
crossed gratings were used; the crossed gratings reduce the
intensity of the individual beams by more than 50%. The
major intensity of the laser beam is now divided between
nine spots as compared to three spots due to diffraction by
a single grating as shown in Figure 7.1. The experiment as
performed by us also had the system spread over a large
area, larger than necessary for this system. This was a
practical difficulty because we were limited by the focal
lengths and sizes of lenses available to us when this exper-
iment was performed. Reducing the size of the system will
not only increase intensity of the light at the output of
the system due to less spreading of light but will also
reduce the number of lenses involved, thereby reducing the
sensitivity of the system to low frequency vibrations.
Another major improvement in the four beam system would be
the simul~aneous detection of both the horizcntal and verti-
cal pairs of beams, as explained in Chapter 6, using a pre-
92
(a) Diffraction pattern due to a pair of crossed Ronchi rulings.
(b) Diffraction pattern due to a square aperture.
FIGURE 7.1.
93
calibrated detection system. A computer aided data recording
system could easily be developed to per~it simultaneous
acquisition and analysis of such four beam data to give
immediate results which, in cases such as the alignment of
the system and the detection of propagation direction of the
wave are useful.
REFERENCES
[l] R. M. White, "Surface elastic waves," Proc. IEEE, Vol. 58, pp. 1238-1276, No. 8, August 1970.
[2] D. E. Bruins and C. W. Garland, "New interferometric methods for piezoelectric measurements," Rev. Sci. Instrum., Vol. 46, pp. 1167-1170, No. 9 September 1975.
[3] R. M. De La Rue, R. F. Humphreys, I. M. Mason and E. A. Ash, "Acoustic surface-wave amplitude and phase measurements using laser probe, " Proc. IEE, Vol. 119, pp. 117-126, February 1972.
[4] T. E. Owen, "Surface wave phenomenon in ultrasonics," Prog. Appl. Mat. Res. (GB), 6, 69 (1964).
[5] A. Alippi, A. Palma, L. Palmieri and G. Socino, "Incidence angle and polarization dependence of light diffracted acoustic surface waves," Journal of Applied Physics, Vol. 45, pp. 1492-1497, No. 4, April 1974.
[6] M. Hercher, "The spherical mirror Fabry-Perot interferometer," Applied Optics, Vol. 7, pp. 951-966, No. 5, May 1968.
[7] B. J. Hunsinger, "Analysis of interferometers with acoustic surface waves on one mirror," Applied Optics, Vol. 10, pp. 390-395, No. 2, February 1971.
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[9] R. L. Whitman and A. Karpel, "Probing of acoustic surface pertubations by coherent light," Applied Optics, Vol. 8, pp. 1567-1576, No. 8, August 1969
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[ 11] "An introduction to piezoelectric transducers," supplement by Valpey-Fisher Corporation, July 1972.
94
95
(12] M. Imai, T. Ohashi and Y. Ohtsuka, "Fiber-optic Michelson interferometer using optical power divider," Optical Society of America, preprint submitted Ju~e 1980.
[ 13] J. C. Wade, P .· S. Zerwekh, and R. 0. Claus, "Detection of acoustic emission in composites by optical fiber interferometry," Proc. 1981 IEEE Ultrasonics Symposium (Chicago, IL), October 1981.
[14] R. 0. Claus and J. H. Cantr-ell, "Rayleigh wave detection by Wideband differential interferometry," Acoustical Society of America Annual Meeting (Los Angeles, CA), Nov. 1980; J. Acoust. Soc. Am., 68, 5108 (1980).
[15] T. M. Turner and R. 0. Claus, "Dual differential interferometer for measurements of broadband surface acoustic waves," Proc. 198l IEEE Ultrasonics Symposium (Chicago, IL), October 1981.
(16] R. 0. Claus and J. H. Cantrell, "DC calibration of the strain sensitivity of a single mode optical fiber interferometer," Proc. 1981 IEEE Region 3 Conf. (Huntsville, AL), April 1981.
[17] T. M. Turner, R. 0. Claus and S. L. Ocheltree, "Pulse-echo interface wave characterization of bolted plates," Proc. 1981 IEEE Region 3 Conf. (Huntsville, AL), April 1981.
(18] R. 0. Claus and R. T. Rogers, !!Waves guided by a thin viscoelastic layer between elastic solids," Proc. 1981 IEEE Ultrasonics Symposium (Chicago, IL), April 1981.
(19] H. M. Frost, "Electromagnetic-ultrasound transducers: principles, practice, and applications," in Physical Acoustics, Vol. 14, W. P. Mason and R. N. Thurston eds., Academic Press (New York) 1979.
(20] A. Karpel, L. J. Laub, and H. L. Sievering, 11 Measurement of acoustic waves propagation characterization by reflected light," Applied Physics Letters, Vol. 10, pp. 295-297, No. 10, May 15, 1967.
(21] S. Sizgoric and A. A. Gundjan, Proc. IEEE 57, 1313 (1969).
96
[22] Stress waves in solids, H. Kolsky, Dover publications: New York, 1963.
(23] C. H. Palmer, R. 0. Claus, and S. E. Fick, "Ultrasonic wave measurement· by differential interferometry," Applied Optics, Vol. 16, pp. 1849-1856, No. 7, July 1977.
(24] D. P. Jabalonowski, "Simple interferometer for monitoring Rayleigh waves," Applied Optics, Vol. 17, pp. 2064-2070, No. 13, July 1978.
[25] A. 0. Garg and R. 0. Claus, "Optical fiber path differential wideband interferometer," .~coustical Soc. of America (Chicago, IL), April 1982.
(26] R. 0. Claus and A. 0. Garg, "Measurement of pulsed ultrasonic waves in liquids by wideband differential interferometry," Acoustical Soc. of America (Orlando, FL), November 1982.
(27] J. H. Cantrell and M. A. Breazeale, "Elimination of transducer band corrections in accurate ultrasonic-wave velocity measuremenL.s by use of capacitive transducers", J. Acoutic Soc. of America, Vol. 61, pp. 403-406, No. 2, February 1977.
[28] H. Shimiz~ and A. J. Bahr, IEEE Ultrasonics Symp. Proc. Cat. No. 76 CH 1120-SSU p.17, 1976.
[29] G. I. Stegeman, "Optical probing of surface waves and surface wave devices," IEEE trans. on Sonics and Ultrasonics, Vol. SU-23, pp 33-63, No. 1, January 1976.
[30] C. H. Palmer, R. A. Klien, and R. E. Green, "A comparison of optically , and piezoelectrically sensed acoustic emission signals," Journal of Acoustical Society of America, Vol. 64, pp. 1633-1639, No. 6, December 1978.
[31] L. Knopof=:, "Surface Motion of a thick plate," Journal of Applied Physics, Vol. 29, pp. 661-670, No. 4, April 1958.
[32] C. L. Pekeris, "The seismic surface pulse," Proc. National Academy of Science Vcl. 41, pp. 649, (1955).
(33) An Introduction to Lasers and Masers, A. E. Siegrnan, McGraw Hill: New York, 1971.
97
[34] M. I. Cohen and R. B. Snyder, "Lightwave systems: an overview," The Western Electric Engineer, special issue on Lightwaves, Winter 1980.
[35) W. Sachse and.H. M. Hsu, "Ultrasonic transducers for mechanical testing and characterization," in Physical Acoustic, Vol. 14, W. P. Mason and R. N. Thurston eds., Academic Press (New York) 1979.
[36] J. F. Martin and R. B. Thompson, "The twin magnet EMAT configuration for exciting horizontaly polarized shear waves," 1981 IEEE Ultrasonics Sympossium Preprint.
Appendix A
PREPARATION OF SINGLE MODE FIBERS FOR EXPERIMENTS
Optical glass fibers have been used for communication
purposes due to their ability to transmit a larger bandwith
of information per unit area than conventional copper
cables. The strength of a smooth glass fiber can far exceed
that of a comparable metal wire, but small surface cracks
quickly degrade their strength (34).
A simple circular lightguide is one in which a glass
cladding ~aterial with a refractive index n 2 surrounds a
core with refractive index n 1 which is higher than n 2 by a
small amount 6.. A typical value for the refractive index of
the cladding is 1.46 and that for the core is 1.48. A ray of
light traveling in the core is partially refracted into the
cladding and partially reflected within the core unless the
ray angle e is less than a ''critical" value as shown in Fig-
ure A.l. This critical value for total internal reflection,
or complete guiding of the ray, is defined from Snell's law,
cose = n 2 /n 1 , r (A. 1)
where 8 is the critical angle for total internal reflec-r
ti on.
98
eo
/ /
r------ ---- ------• COATING
i ------. . ........ ...____,
CORE n1 1--~-"''--~~~-"'L-~~~~~~~~~~~~~~~~~---1-------·...-------'
FICURE A. l.
CLADDING n2 _____ ....
. . ----------- -- _ ... - . -·
Path of light through a step index optical fiber. A is the critical angle below which the light r~y refracts into the cladding [34].
INDEX PROFILE
n1 = I ·48
n2=1·46 <..O \.0
100
If Equation A.l is applied to the glass air boundary at
the input end of the fiber and the refractive index of air,
n 0 is assumed to unity, a basic parameter known as the num-
erical aperture (NA) may be defined by
NA = sin8 0 (A. 2)
This parameter defines the maximum
allowable angle for a ray of incident light to be totally
internally reflected.
The propagation of light in an optical fiber is
governed by Maxwell's electromagnetic field equations, which
predict the number of "modes" that will propagate through a
certain glass fiber of a given core diameter and refractive
index. The solutions of Maxwell's equations also predict
propagation of light in the cladding. The number of modes
that a given lightguide can support is related to a dimen-
sionless quantity usually referred to as the V number,
V = 2Tia(NA)/A, (A. 3)
(A.4)
where A is the wavelength of the light being transmitted and
a is the core radius of the fiber. It can be shown tha~ the
101
number of propagating modes is approximately equal to M
where,
(A.5)
This is valid for step index fibers only. Thus, it can be
seen from the Figure A.2 and above equations that single
mode propagation in a step index fiber takes place when the
value of Vis below 2.405 [34]. Below this value all other
modes are forced into cutoff. To obtain very low V number
for operating wavelength of 0.82 x io-s m and 1.6 x io-s m,
the product of core radius and NA must be small [34],i.e.,
k a(a) 2 < 0.24 for 1.3 x io-s m, and
k a(a) 2 < 0.15 for 0.82 x io-s m.
This shows that single mode fibers must have core diam-
eters of less than 10 x io-s m and must also be made with a
small index difference ~.
The optical fibers are highly sensitive to microbending
and microfractures which can occur when fibers are placed in
structures that impose random bends in their axes, resulting
in a loss of optical power. These microbends make the
selection of materials used in cable jacketing extremly cri-
tical. Optical fibers used for underground cabeling purposes
102
900 FOR
800 A= O· 82 µm STEP INDEX NA= 0·23 PROFILE 700
a = V/ 1 ·76 (J) 600 w 0 0 50'0 :?
lJ... 400 0
a: 300 GRADED INDEX w Ill PROFILE ~ 200 :::> z
100
10 20 30 40
v NUMBER
1-4 6 11 17 23
CORE RADIUS, 10- 6 m
FIGVRE A.2. Number of transmmission modes in a light guide increases with core radius a and v· number. Single mode fiber have V number less than 2.405 [34].
103
have a PVC coating extruded over the coated lightguide
fiber. This is then imbedded between strands of Kevlar and
further protection is supplied by enclosing the fibers in
PVC and metal tubings.
However, optical fibers used for laboratory purpose are
not subjected to strains experienced by underground fiber
cables. The laboratory optical fiber supplied to us by ITT
had a RTV sleeving and a plastic jacketing over the glass
lightguide. Both of these coatings could be easily scraped
off using a razor blade and Acetone. The RTV sleeving and
plastic coating were removed from t~e first 10 cm of both
ends of the fiber. These ends were then cut by scribing the
fiber at approximately 2 cm from the tip. By applying slight
lengthwise pressure, the fiber snapped giving "good" ends. A
"good" end is defined as a flat end with no pits or jaged-
ness on its surface. The exposed cylindrical ends of the
fibers were then coated with a index matching mode stripping
fluid to eliminate the interferenc~ of light traveling in
the cladding with that traveling in the core.
The prepared ends of the fibers were placed in brass
fiber holders which were positoned using six axis position-
ers as shown in Figure l of Chapter 2.
Appendix B
COMPUTER PROGRAM FOR CALCULATING THE POSITIONS OF LENSES FOR VARIOUS SAW FREQUENCIES
The following pages contain two computer programs which
were used with the fiber differential interferometer. The
first program calculates all the different positions possi-
ble for a given lens sytem. These positions correspond to
the different frequencies the system can be tuned to. The
second program plots out the sensitivity curve for various
spot separations. A set of plots for two spot separations of
2 mm and 18 mm have been included for comparison. Also plots
as a function of d/A = n + d/\ , where d is the spot separa-
tion and \ is the acoustic wavelength, have been included
for comparison. In the plots LA = A.
104
l REM 2 REM 3 REM 4 REM 5 REM
20 REM 30 REM 40 REM 50 REM ~~ REM
. 70 REM 80 REM
IJE:::;. ·~~~:1 F.·E=·t·I ... -· . -
100 F::EM 110 PEM
****************~******************************************** AUCL6.BAS NOV-10-81 A.O.GARG ~~~·ti~~1-~~~~~~~~~~~~~~~~~~~·t~~~~·t·~~~~~~~~~~~~~~~~~~·~~~~~~~~~·**~ ·1 · ·1 · ·1'· · · ·1 · · ··•'I" ·T· ·1'· ·T··1 • ·1'··1 · ·1'· ·T· ·T· ·1 · ·t· ·1 · ·1 · ·'f· ·1'· ·t· ·1 · ·1"· · ··T· ·T· ·T·· • -1 · ·1 · ·1'·•1'• ·t· "T··"f·.,-. 1"··1"··,.· If'· ·'f··l"··T· .,._,, .. T·-1"··T·'1'· ...---?·"1"· 'f· ·f'.1"· -t'·1"· ........
TH IS I:::; ~i ::WEC I t:il PROGF.:?if·l FOP THE U:3E IN FI BEF.: . OIFFERENTiru_ INTERFEROMETER DESIGNED BY MR.A.0.GARG ANO [·,c::. F·' f'I r·L ·:· 11·::· _ r'. . · .. _ . _. -~ i _ ·-·· . THI::; F'F.'.OGP{if·l ::rrnTE:::; THE HUME~'.IC~iL APEF~:TUF.:E OF. THE FIBER AND .-:···L r:t IL"""TE'.=: i"HE" '.:;f·r:::·E·"·[1 It·' E:Er-t"'"l ·"·T 1.1···~·1n11::: (IJ'.:;T·"·t··r·E~ .. H _ .. .. H _ . ... 1~. -t1 . . . 1 r 1· H , 1-ir~.. -· - - - 1-i 1..- _ •
THIS PROGRAM ALSO CALCULATES THE REQUIRED POSTION OF THE LEN::; ~iND THE FOC~~L LENGTH OF THE LEt-r::ES FOR • . ..'fiRIOUS :::At·J FREOIJENC
l 20 PR I HT I I MPUT t·fUMEF.: I CAL ~iF'EF.:TUF;:E OF THE FI BE~: I .i
130 INPUT Nt'.:t 140 FRINT ·INPUT THE FOCAL LENGTH oF THE FIF.:::::r LENS IN MM ONLY • _. l ::;o I HPUT F 1 i i:.o PF: r NT • r NPUT THE DI :::r ~iNCE OF Fr E:ER FORM THE LENS r M MM ONL..... • .i 17'0 INPUT Ul 180 Vl=FllUl/(Ul-Fl) 190 F'F.'.Hff I INPUT THE :::EPEF.'.fiTION E:ETMEEN THE FIBERS IN MM I.:
·::·i:::1n I t··IF'll1- :=;[: .: ... -· .. -· ·-2 l 0 Pt'.iGE 220 REM SIN(ANGLE OF ACCEPTANCE)=NUMER!CAL APERTURE 230 REM FOR SMALL ANGLE SINE OF THE ANGLE = THE ANGLE ?4t1 D==~i nv NA ) 250 SP=(0/2)*(Ul) 260 H1=2l(2tSP+SE) 270 PRINT 'THE MINIMUM HEIGHT OF THE FIRST LENS= ';Hl 2:::0 pf;,: I MT I THE I f'l•iGE I::;; ( I .• I.) 1 .• I > MM FOF~M THE FI ~:ST LEHS' 290 PF.'.INT 'THE SPOTS ARE ( ';Ul/Ul; I) ~U1 APART'
I-' 0 U1
:-:•:~:1n F:·t~· J .. t· 11···· ... -· ... - . . 1
PF:IMT .. ··.
F'l?lHT"·· ..
F'PlNT"··. PP It-ff"·· .. PklMT
~ 1 :, F·r:· l. · 11· • · E~·. nE:· 1r:r·Y [1 I ·=··1· ··· t·•r·E ? • ; ·-· t f". . t 1 t ~ -~ ! ... ..... - ... I . · •• • H 1 ... • .
320 I HPUT O:t: ~J~ ~;:i:1 c. ··· r·r:: _ -· -· r· H .l ·-
340 IF 0$='Y' THEN GOTO 120 350 PF.:Hff • Mm·J ME HILL CALCUL.t1TE THE SPF.:EAD IM BEAM :::POT OH SIF.:FACE' :-:~.:::·f1 F·c· I ·'T • llt·1[·1E·c:·rT11· t·1I· TE-::-1· 1 • .... • -·· o•• ... o t 1 H• 1 . _r .. O~ - • 1 _, 0 ·-·
:·.p·~~1 l·'H··· Ii· 1 c1ru-:1 ·-· -· .f ----... -. - F· .·. ,-E . . : .. :.~.:.1 HJ -:::s~o PF::nff • M~ii<IMUM DIST~iNCE BETl·~EEN THE FIRST ~iMO LAST LENS • _; 400 lNPUT DM 410 P~: I NT I FOC~il LEt·~GTH OF THE SECOND LEMS I .i
4~~0 H~PUT F2 430 PRINT 1 FOCAL LENGTH OF THE THIRD LENS '; 440 INPUT F3 4~~0 PP INT I FOC~iL LENGTH OF THE FOUF.:TH LEHS I ,i
460 JMF'UT F4 4?0 PAGE 4:::0 pp I NT I FOC~iL LENGTH OF FI F.:ST LEHS = ' i F 1 4 90 pp I MT ' FOC~il LEJ~GTH OF TH I RD LEHS ::: I .: F2 ~:;(10 PP I HT • FOC~il.. LENGTH OF THI~::[I LEM::: ::.-: I .i F3 ~~ 10 PF: I MT ' FOCt~L LEMGTH OF FOUPTH LEHS :: 1 .• F 4 ~;20 PPIHT • roT~iL DH:;r~1MCE BETHEEN FIF~::::r {iMD LAST LENS == • .i Df'I c.-~ -· F··F·· l. t •r·· ..... .::.t.1 . : .. ·1 •·•
PPIHT"··. PF.:It~r·· .. PF.:IHT'"··. PF.:IHT'"·· Pf~: I Mr· ..
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107
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890 900 910 920 930 940 950 960 970 980 ~0
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F·r:1·t 11·· F·c- F-.··· '" ··c··r1 L1 •• ·1· .. ·· 11·-tL1·-· ·' 1·-:~ . . ·1 ._:. .• · t:. .• .=·· •. • '·· ..I • ~- .,. ..' .• .• t:. .• ··· ~=· · r1 1:•
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F·.c:-· It a·y· 1 I 1 ··· L I IE'-. •· F' F" J f-.-.. F-' f"4 .-;. ·· '·" "t 1 •• . · r~. ·1 ..• ..... • ..• • •. :. IJ .. • · .:::. .• -.:!• .• • ! •.. I ·" ·1 ) ·'
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PF.'.INT"·· .. f'F.:IMT"·· .. PF.:I t-tr· ... F'F.'.IMT
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I-' 0 00
109
* *
* *
a~a :..;.
. :.+-* r··-;.f · .. ·~· .. ·
~~~
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111
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CCO 01 IFFR t·f Ol·U:~pf-1 670 08(1)=20~LOG<OE(I )/MA) 6f:(1 ()t~EPF:: MOL·~~iPN t::~~O t·IE:>::T l ?OC1 DI ==M l t-10:: Db > 7 ln F-n~ ~=~ i·n t·•f:(~) ~TE:F~ 1 I •. .• I', I , '\., •. 1 , •• • •• .• -, -· - 1· F' [" E . .. -· l"l E" I [' E . • . . (" I ( :::'.~J . . .I .K t::, _)::;~.::I d :h ..I.::•:. :: .. )::: _I ?30 NE::O::T K 740 PRINT TA8(30); 1 08 PLOT OF SENSITIUITY 1
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7'90 IMPUT F.:E:f 800 IF RE$= 1 N1 THEN GOTO 850 810 PRltlT 'SAME UALUES OF FREQ ANO VELOCITY ? S FOR SAME~O FOR OIFFERNT'
:::::::::o I MPUT ::~•.,.t:f 830 IF SU$= 1 0 1 THEN GOTO 100 840 IF SUt= 1 S 1 T~EN GOTO 350 850 PRINT 1 REORAW SENSITIUITY CURUE ? Y/N 1
::::i::o I HF'UT PD:;: 870 IF ROf= 1 Y1 THEN GOTO 500 :=:::::a:1 ~=;-r f ·1 F' ...... - - ...
F.'.E~iD\' l
..... ..... N
113
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c ....... • . ...;_ w
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Appendix C
DATA FOR THE DETECTION OF PULSED WAVE IN WATER USING TWO BEAM DIFFERENTIAL SYSTEM
The following plots are data for the detection of
ultrasonic compressional waves in water using the two beam
differential interferometric system. Figure C.2 is a compar-
ison of the rf noise generated by the Metrotek pulser to the
signal due to the pulsed compressional wave traveling
through the water tank. Laser noise was not seen during this
experiment. This is probably due to the long
the laser had before it was used.
117
warm up ~· ~ime
20 mV/div.
0
A
B
31 62 93
~
124 155 186 x 10-6 sec.
FIGURE C.l. Data for detection of an ultrasonic pulse packet traveling in water tank 11sing the two beam system. The notations used are identical to those used in Chapter 6. TI1e above data is within 5% of the calculated theoritical value.
,-
f-' f-' 00
so mV/div.
0
R.F. noise
31 62 93 124 155 x 10-6 sec.
FIGURE C.2. Comparison of the rf noise (due to Metrotek pulser) to the signal (due to ultrasonic pulse traveling in water tank).
186
I-' I-' l.O
Appendix D
DATA FOR DETECTION OF THE DIRECTION OF PULSED WAVE IN WATER USING FOUR BE~~~ SYSTEM
The following plots are data from the detection of
ultrasonic pulses in the water tank using the four beam sys-
tern. Figure D.3 is the rf noise due to the Metrotek pulser
unit and laser noise due to the laser. Both are rf signals
and are unaffected by the presence of the optical signal at
the photodiode. Figures D.4 and D.5 were obtained for beams
positioned to form a square and diagonally opposite pairs of
beams were used for interference. However, since the system
had to be reset for every measurement, these results do not
give an accurate indication of the direction of propagation
of the pulse packet. A much better result can be obtained if
both pairs of beams are simultaneously evaluated using pre-
calibrated detectors.
However, if data from Figures D.4 and D.5 is considered
correct the vertical amplitude for the pulse packet A in
Figure D.4 is 240 mV while amplitude of pulse packet A in
Figure D.5 is 90 mV. Using the formula
tans = amplitude of A in Figure D.5/amplitude of A
in Figure D.4
we get
120
121
a= tan- 1 (90/240)
a = 20.55° to the left of the diagonal formed by two
spots used for interference for Figure D.S. Thus e gives the
direction of propagation of pulse packet in water.
result seems reasonable.
This
Cl ID
E IF
30
m\'/c~iv.
,-- ' 0 15.5 31.0 46.5 62.0 77 .5 93.0
-6 x 10 sec.
FIGURE D.l. Data for detection of ultrasonic pulse packet traveling in water. This detection was done by using the vertical pair of beams of the four beam system. The notations are identical to ones used in Chapter 6. Pulse packets of laser noise are also clearly seen in this plot.
I-' N N
30
mV/div.
A D
E
+-~~~~~~~...&.~~~~~~~-'~~~~~~~~-L-~~~~~~~-L~~~~~~~_j___~~~~~~·...&.~~~~
0 15.5 31.0 46.5 -6 x 10 sec.
62.0 77 .5 93.0
FIGURE D.2. Data for detection of an ultrasonic pulse packet in water using the horizontal pairs of beams of the four beam differential system. The data is within 10% of the calculated value. The notations are identical to those used in Chapter 6. The pulse packets not named are due to laser noise. This laser noise makes identification of ultrasonic pulse very difficult.
~ .... ~..)
(.,)
30
mV/div. ~ --
0 31 62 93 124 155 186
x 10-6 sec.
FIGURE D.3. This data is obtained when the laser beam is blocked . The large initial pulse is the rf pulse generated by the Metrotek pulser. ~he following pulse packets are rf noises generated by the laser itself.
...... N +:--
A
B c D F
E H
30
mV/div.
G
1 I I I
0 15.5 31.0 46.5 62.0 77.5 93.0
x 10-6 sec..
FIGURE D.4. Data for the detection of ultrasonic pulse packet traveling in a water tank using the four beam differential interferometric system. The four beams of the interferometer were positioned such that they lay at the four corners of of a square. The experiment was conducted in two parts. First, a set of diagonally opposite pairs of beams were superimposed and the interference pattern detected. This is shown above. The next part was . .same using the remaining diagonally opposite pairs, results of which are shown in Figure D.5. Unfortunately as the system had to be realigned everytime it could not be calibrated and hence accurate results could not be obtained.
I-' N lJ1
'° N ......
15
mV/div.
[ _ _,______~____,_______.__ _ __.___ _ __,___
0 15.5 31.0 46.5 62.0 77. 5 93.0
x 10-6 sec.
FIGURE D.S. Data for the direction of ultrasonic pulse traveling in a water tank. As explained in Figure D.4. accurate results were impossible. However, one does notice a change in amplitude of the ultrasonic pulse when compared to those in Figure D.4. This can help us to conclude that the direction of the pulse was oriented more along the diagonal formed by the two beams used for Figure D.4.
The vita has been removed from the scanned document
APPLICATION OF OPTICAL FIBERS TO WIDEBAND DIFFERENTIAL
INTERFEROMETRY AND MEASUREMENTS OF PULSED WAVES IN LIQUIDS
by
Avinash 0. Garg
(ABSTRACT)
Wideband differential interferometry has been applied
to the detection of SAW on specimen surfaces and ultrasonic
compressional waves in liquids. Herein is described the
performance of a wideband differential system which uses
single mode optical fibers to transmit coherent light from
input optics to a surface which supports which supports
ultrasonic waves. Polarized light from a 2.0 mW helium-neon
laser source is divided and coupled to two flexible bundled
single mode optical fibers which transmit the light to a
small remote detection head. The light at the output end of
the fibers is collimated and focused by a varifocal lens
system to points on the surface of a specimen to be
inspected. Elastic waves on the specimen differentially
modulate the relative phases of the two optical beams due to
periodic changes in particle displacement at the surface.
Upon reflection, the two beams are superimposed, filtered,
and detected to produce an optical signal directly propor-
tional to instantaneous displacements.
Also described is the development of two beam and four
beam differential systems for the detection of ultrasonic
compressional waves in water. Two laser beams are transmit-
ted through a water tank and combined to produce an inter-
ference pattern. The detected motion of the pattern yields a
differential measure of the acoustic field amplitude at the
location of the two probe beams. If a pulsed ultrasonic wave
is generated in the tank in a direction perpendicular to and
coplanar with the probe beams, each beam is modulated inde-
pendently and output signals of opposite phase are produced.
The acoustic sensitivity of both the above systems may
be adjusted by changing the separation between the two spots
on the surface or the two beams in the tank. The system
effectively discriminates against low frequency noise vibra-
tions, while the upper acoustic frequency response exceeds
100 MHz. Applications requiring flexibility allowed by a
remote detection head can use the fiber system to their
advantage while potential applications of the four beam sys-
tem to three dimensional mapping and ultrasonic field scat-
tering is suggested.