# Model for a Torsional-Mode Ultrasonic Transducer for an Acousto-Optic In-Fiber Isolator

Authors: Gerald T. Moore
Journal: Advances in OptoElectronics
 (2010)

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## Abstract

Torsional ultrasound modes can couple the optical polarization states in a birefringent fiber. Polarization coupling produced by interaction with a higher-order torsional mode slightly above its cutoff may provide a route to producing an in-fiber isolator suitable for use in narrow-band high-power fiber amplifiers. This paper describes a model of a transducer generating
torsional modes in a cylindrical fiber. This model predicts that almost all of the power applied to the transducer is radiated into the desired mode. The paper also discusses effects produced by acoustic absorption and the dependence of the acoustic velocity on temperature.


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## Body

## 1. Introduction

By matching the optical polarization beat lengthLB in a birefringent silica optical fiber to the axial wavelength of a traveling torsional wave of angular frequency Ω propagating in the fiber, it is possible to couple light from one polarization to the other [1, 2]. When light is coupled from the slow polarization to the fast polarization, it is down-shifted in frequency by Ω if the light and sound are copropagating, but up-shifted if the light and sound are counter-propagating. This nonreciprocal frequency shift can be used to make an in-fiber acousto-optic (AO) isolator. This requires placing two torsional transducers on the fiber separated by D=πvg/2Ω, where vg is the group velocity of light in the fast polarization. These transducers propagate sound in the same direction. One watt of acoustic power from each transducer is sufficient to couple 50% of the light from one polarization to the other over a few centimeters [2]. The polymer jacket is removed from the fiber in the interaction regions to prevent acoustic damping. The relative acoustic phase of the two transducers is adjusted such that in the forward direction all of the light at the wavelength of interest returns to the slow polarization, whereas in the backward direction all of the light at this wavelength goes into the fast polarization. Polarizers at both ends, such as 45-degree tilted fiber Bragg gratings [3], remove light in the fast polarization to make an isolator. To date an isolator based on torsional acoustic waves has not been made, but 100% polarization switching has been demonstrated using the lowest-order (s=0) torsional mode [1]. However, an analogous isolator was demonstrated using the lowest-order flexural mode at Ω/2π=4.31 MHz [4]. In this case coupling was between the two transverse modes of a two-mode fiber. Although a 22 dB extinction ratio was reported, the large D = 11 m spacing between the transducers makes this approach unattractive for high-power operation. The key to decreasing this spacing is to increase Ω, while using an acoustic mode for which phase matching is possible at high frequency. Raising the frequency to about 50 MHz reduces the spacing D between transducers to about 1 m. Except for the short regions following the transducers where acoustic coupling occurs, the fiber between the transducers can be coiled and jacketed with polymer. Figure 1 shows the layout of an AO isolator at four different length scales.Figure 1
Components of an AO isolator are shown schematically at four different length scales. Sizes are approximate. Forward propagating light enters from the left with slow polarization. Polarizers (possibly45∘ tilted fiber Bragg gratings) are oriented to pass the slow polarization. Copropagating torsional acoustic waves generated by transducers act as 50% polarization couplers. Transducer 2 returns forward light to the slow polarization, while transducer 1 shifts backward light entirely to the fast polarization.The phase-matching acceptance for polarization switching, which occurs over a few centimeters, is much wider than the transmission features produced by the transducer spacingD and the linear polarizers. The transmission in the forward direction as a function of wavelength λ is a comb with periodicity λLB/D, while the backward transmission is an out-of-phase comb. This is illustrated in Figure 2. The position of these combs depends on the relative acoustic phase of the two transducers. Hwang et al. [4] found that it was necessary to use a feedback circuit to adjust this phase to compensate for shifting of the combs produced by vibrations or temperature changes. The width of the comb maxima and minima is sufficient to prevent backward propagation of light produced by stimulated Brillouin scattering in narrow-band Yb-doped fiber amplifiers. The isolator can be used for multiple wavelengths commensurate with the comb period, such asthose thatmight be produced by spectral beam combination. However, it cannot protect against inadvertent lasing at other wavelengths within the gain bandwidth of Yb. This type of isolator can be tuned for use with other types of fiber amplifier besides Yb, such as Er or Tm.Figure 2
Calculated forward (red) and backward (green) transmission through an isolator using fiber with beat lengthLB=3 mm and transducer separation D=105 cm.A transducer spacing of 1 m imposes a power limitation on operation of an AO isolator, since undesirable nonlinear effects can build up over this distance. For example, we estimate that the nonlinear refractive index of fused silica will limit isolator operation to about 200 W in a 10μm core fiber and about 1 kW in a 25 μm core fiber. By contrast, present fiber-coupled isolators are limited to about 50 W. Bulk isolators can withstand higher power but distort the beam quality at powers above about 100 W.The frequency for phase-matching of the lowest-order torsional mode is too low for use as a high-power isolator, sinceD becomes very large and the comb spacing very narrow. However, a transducer producing 100% polarization coupling with this mode can be used as a tunable notch filter [1], when placed between crossed polarizers. This can filter out undesired wavelengths, including wavelengths within the gain bandwidth of the amplifying medium.


## 2. Matching of Transducer Modes and Free-Oscillation Modes

In the analysis below we consider the fiber to be a homogeneous elastic cylindrical glass rod, neglecting perturbations which might arise because of different elastic properties of the core or the stress rods. Torsional waves in a cylindrical rod are characterized by a displacementu(r,z) which is entirely in the azimuthal direction, but independent of the azimuthal coordinate θ. If the cylinder radius is a, we can introduce a dimensionless frequency γ=Ωa/V, where V is the transverse sound velocity. This velocity is variously reported by Engan to be 3750 m/s [2] or 3764 m/s [5] in fused silica. Vacher et al. [6] found that V at 5 MHz and 16 GHz are the same to within 0.1% at room temperature,suggesting that dispersion is small. However, V was found to increase with temperature at 0.3 m/s kelvin. It is convenient to express r and z in units of a. Then the torsional waves are of the form u=(1/2)rexp(±iγz) or u=J1(αr)exp(±iβz), where β2=γ2-α2.The torsional modes of a free elastic cylinder are a subset of all the possible vibrational modes [7]. In general the displacement u has an azimuthal dependence cos(nθ) or sin(nθ). The modes with n=0 can be further subdivided into torsional and axial-radial. The modes with n=1 or higher are called flexural. The dispersion relations for the modes, except for the torsional modes, depend on the Poisson ratio for the material. Figure 3 shows the dispersion relations for n=0 (red) and n=1 (green) for the Poisson ratio 0.17 of fused silica. The lowest and highest red curves shown are the two lowest torsional modes. The other red curves are axial-radial. The lowest torsional, radial-axial, and flexural modes are the only ones with no cutoff. For torsional oscillations the two nonzero components of strain (with proportional components of stress) are 2εrθ=r∂(u/r)∂r and 2εzθ=∂u/∂z [8]. Our model for the transducer is a section of fiber between z=-L and z=0 where u at r=1 is a single-frequency oscillation independent of z. The model does not specify how such oscillation is produced. However, at the end of the paper we cite some methods that have been used to excite torsional vibrations in fibers and rods. εzθ=0 at the surface of the fiber in the transducer, whereas εrθ=0 at the surface of the free fiber. The displacement in the transducer is of the form
(1)u=J1(γr)+∑n=1J1(Ynr)[Dnexp(iκn(z+L))+Hnexp(-iκnz)],
where Yn is the n'th zero of J1, κn2=γ2-Yn2, and κn is positive real for propagating modes or positive imaginary for cutoff modes. Dn and Hn are the modal amplitudes. We could multiply the first term above by a constant, but we choose to normalize in this way for now. Outside the transducer the fiber is uncontrained at the surface; so εrθ should vanish at r=1. Since ((rd/dr))[(1/r)J1(αr)]=-αJ2(αr), we choose α=Zn, where Zn is the n'th zero of J2, and write the displacement for z>0 in the form
(2)u=12C0rexp(iγz)+∑n=1CnJ1(Znr)exp(iβnz),
where βn2=γ2-Zn2 and βn is positive real for propagating modes or positive imaginary for cutoff modes. For positive z the propagating modes with modal amplitudes Cn carry power only in the positive z direction. The mode with a cutoff at γ=Zn we call the s=n mode. Since Z1=5.136, the s=1 cutoff frequency for a fiber of diameter 2a=125 μm is Ω/2π=VZ1/2πa=49 MHz. By operating just above the cutoff for the s=n mode, we can match the axial wavelength 2πa/βn to the optical polarization beat length LB (typically about 3 mm). The phase velocity Vγ/βn approaches infinity at cutoff, while the sound group velocity Vβn/γ approaches zero. The s=0 mode, corresponding to the C0 term, has no cutoff, propagates at speed V without dispersion, and can only be phase matched at much lower frequency. Since Z1 is greater than Y1=3.832, a propagating mode inside the transducer already exists when γ passes through the s=1 cutoff.Figure 3
Dispersion relations for torsional, radial-axial, and flexural modes for an elastic cylinder. Lowest and highest red curves are torsional; other red curves are axial-radial; green curves are flexural.β is longitudinal wave vector in units of 1/a. γ is angular frequency in units of V/a.Atz<-L we write the displacement as
(3)u=12F0rexp(-iγ(z+L))+∑n=1FnJ1(Znr)exp(-iβn(z+L))+12G0rexp(iγ(z+L))+GpJ1(Zpr)exp(iβp(z+L)).
Here Fn are the modal amplitudes for sound propagating in the -z direction. The last two terms with amplitudes G0 or Gp are inserted to describe reflections of one of the modes above cutoff back into the transducer. For example, if the s=1 mode is above cutoff, we take G1 to be nonzero and G0=0. The case of nonzero G0 is not of much practical interest but is included for completeness. When the G coefficients are zero, equal acoustic power is radiated from the transducer in both directions. The backward power is undesirable. It can be damped by leaving the jacket on the fiber at z<-L. However, more efficient operation might be possible by reflecting the power. For a mode near cutoff, reflection can be produced by raising the fiber temperature behind the transducer. This increases V, which puts the mode below cutoff in this region. If the reflection is total, then |Gp|=|Fp|, but the effects of the reflection depend on the phase Θ of Gp. This phase depends on the location of the thermal gradient producing the reflection and cycles through one period when this location shifts by half the longitudinal sound wavelength in the unheated fiber. Under phase-matched conditions this is also half the optical polarization beat length LB. Reflection should be produced close to the transducer in order to minimize AO coupling by light going in the -z direction.Atz=-L and z=0 both u and ∂u/∂z should be continuous. This leads to the following set of four equations:
(4)J1(γr)+∑n=1(An-iTnBn)J1(Ynr)=12F0r+∑n=1FnJ1(Znr)+12G0r+GpJ1(Zpr),(5)∑n=1κn(TnAn+iBn)J1(Ynr)=-iγ12F0r-i∑n=1βnFnJ1(Znr)+iγ12G0r+iβpGpJ1(Zpr),(6)J1(γr)+∑n=1(An+iTnBn)J1(Ynr)=12C0r+∑n=1CnJ1(Znr),(7)∑n=1κn(TnAn-iBn)J1(Ynr)=-iγ12C0r-i∑n=1βnCnJ1(Znr).
Here we have introduced
(8)An=12(1+eiκnL)(Dn+Hn),(9)Bn=12(1+eiκnL)(Dn-Hn),(10)Tn=tan(κnL2).
Note that in the absence of reflection (G0=0, Gp=0) we can take Bn=0, F0=C0, and Fn=Cn, so that emission from the transducer is symmetrical.The torsional modes outside the transducer are orthogonal, as can be seen from the following identities:(11)(α2-ε2)∫01drrJ1(αr)J1(εr)=αJ1(ε)J2(α)-εJ1(α)J2(ε),∫01drrJ12(Znr)=12J12(Zn),∫01drr2J1(αr)=1αJ2(α).
Multiplying (4)–(7) by either r or J1(Zmr), integrating, and using the above identities, we obtain
(12)18(F0+G0)=1γJ2(γ)+∑n=1(An-iTnBn)1YnJ2(Yn),(13)-18iγ(F0-G0)=∑n=1κn(TnAn+iBn)1YnJ2(Yn),(14)18C0=1γJ2(γ)+∑n=1(An+iTnBn)1YnJ2(Yn),(15)-18iγC0=∑n=1κn(TnAn-iBn)1YnJ2(Yn),(16)12FmJ1(Zm)+12δmpJ1(Zp)Gp=γγ2-Zm2J2(γ)+∑n=1(An-iTnBn)YnYn2-Zm2J2(Yn),(17)-12iβmFmJ1(Zm)+12iδmpβpJ1(Zp)Gp=∑n=1κn(TnAn+iBn)YnYn2-Zm2J2(Yn),(18)12CmJ1(Zm)=γγ2-Zm2J2(γ)+∑n=1(An+iTnBn)YnYn2-Zm2J2(Yn),(19)-12iβmCmJ1(Zm)=∑n=1κn(TnAn-iBn)YnYn2-Zm2J2(Yn).
We can eliminate F0, Fm, C0, and Cm from these equations to obtain a set of equations to be obeyed by An and another set of equations to be obeyed by Bn. In fact, if we define Z0=0 and β0=γ, the equations derived from (12)–(15) can be treated on the same footing as those derived from (16)–(19). We obtain
(20)18G0+12δmpJ1(Zp)Gp=∑n=1Bn(-iTn+κnβm)YnYn2-Zm2J2(Yn),(21)-γJ2(γ)+18γ2G0+12δmpβp2J1(Zp)Gp=∑n=1An(1-iκnTnβm)γ2-Zm2Yn2-Zm2YnJ2(Yn).
If one first specifies a value of Gp (or G0), these equations constitute a set of linear inhomogeneous equations for the amplitudes An and Bn. In order to solve these equations we choose an integer N (typically 200) and truncate by letting n run from 1 to N and m run from 0 to N-1. Then we obtain An and Bn by numerical matrix inversion. The coefficients F0, Fm, C0, and Cm needed for the modal expansions of u outside the transducer are then obtained from (12), (14), (16), and (18).If, for example, one is interested in the situation where thep mode is totally reflected at z<-L, we repeat the calculation for different values of |Gp| in order to home in on the value of |Gp| for which |Gp|=|Fp|. The result depends on the phase Θ of Gp, which in turn depends on how and where the reflection occurs.To check the convergence of our numerical procedure, we can plot the real and imaginary parts of the left and right sides of (4)–(7) as a function of r to see if they match. Equations (4) and (6) represent the displacements u(-L,r) and u(0,r), while (5) and (7) are proportional to the strain εzθ. We can also calculate -r∂(u/r)∂r from (4) and (6) to obtain expressions proportional to the strain εrθ. The real parts correspond to times when the transducer amplitude (the displacement at r=1) is maximal, while the imaginary parts correspond to times when the transducer amplitude is zero. In making these plots the number of terms we retain in the sums (typically 140) is less than N, since the final terms can be corrupted by the matrix truncation.We find that the matching of the external and internal displacements and strains is good. The differences appear as low-amplitude, high-frequency oscillations. The differences are most apparent inεzθ, which is zero at r=1 in the transducer but appears to be discontinuous as a function of z at z=-L and z=0 when r=1. The displacements and strains are insensitive to the choice of N if N is not too small.


## 3. Energy Considerations

Since our model neglects sound absorption in the fiber, the power radiated in the modes which are above cutoff should equal the powerPT applied to the transducer. Modes below cutoff are exponentially attenuated away from the transducer and do not propagate power. Let U be the amplitude of the transducer motion at r=1. Then the modal coefficients calculated in the previous section should be multiplied by U/|J1(γ)| to determine the physical displacement amplitudes. By comparison with the power expressions given in [2], we see that the power propagating in the s=0 mode at z>0 is Ps=0,+=[γ|C0|/2J1(γ)]2𝒫, where 𝒫=(1/4)πρV3U2 and ρ=2200 kg/m2 is the density of fused silica. If, for example, U=90 nm, then 𝒫=0.738 W. The power in higher-order modes which are above cutoff is Ps=n,+=2[|Cn|J1(Zn)/J1(γ)]2βnγ𝒫. Analogous expressions apply to the power propagating at z<-L.Division by|J1(γ)| is not possible when γ=Yn for some n. In this case there is no steady state in the absence of damping. When Y1<γ<Z1, there is one propagating mode inside the transducer. We call this the t=1 mode. This mode can radiate only to the s=0 mode outside the transducer, and resonances occur as a function of L. Internal values of u are typically large compared to u at the surface, and the t=1 power within the transducer can be much larger than the power driving the transducer. When γ exceeds Z1, the s=1 channel opens, sound vibrations are no longer trapped in the transducer, the t=1 power is small, and the generated s=1 power is almost independent of L. In general the t=n power propagating in the forward and backward direction is given for modes above cutoff by
(22)Pt=n,±=12𝒫γκn[J2(Yn)|An±Bn|J1(γ)cos(κnL/2)]2.
To calculate the time-averaged power driving the transducer we use the stress
(23)σrθ=2ρV2εrθ=-ρV2Ua|J1(γ)|{γJ2(γ)cos(Ωt)}+Re{∑n=1YnJ2(Yn)[Dnexp(iκn(z+L))+Hnexp(-iκnz)]exp(-iΩt)∑n=1}
evaluated at the surface of the fiber. The time-averaged power dPT driving the transducer over the surface area a2dθdz is obtained by multiplying this stress by the surface velocity -UΩsin(Ωt) and averaging over time,
(24)dPT=12adθdzU2ρV2Ω|J1(γ)|×∑n=1YnJ2(Yn)Im[Dnexp(iκn(z+L))+Hnexp(-iκnz)].
Integrating over the surface of the transducer and using (8) and (10) yields
(25)PT=8𝒫γ|J1(γ)|∑n=1YnJ2(Yn)Im(TnAnκn).
It is often more meaningful to express powers relative to PT than in terms of 𝒫.


## 4. Numerical Results

Let us begin by considering a transducer withL=10 and γ=5.13767, slightly above the s=1 cutoff. For a fiber with a diameter of 2a=125 μm this corresponds to a frequency Ω/2π=49.06 MHz and an axial s=1 wavelength 2πa/β1=2.7 mm, on the order of the polarization beat length LB in polarization-maintaining optical fibers. One watt of power in this mode corresponds to an amplitude at r=1 of 85.7 nm. At this frequency the s=0 wavelength 2πa/γ=76.4μm is much too small for phase matching. We wish to compare the situation where the sound is emitted equally in both directions to the case where the s=1 mode is perfectly reflected at z=-L with phase Θ=0 or 180∘. U is held constant in Figures 4 and 5, but PT depends on whether there is reflection. The red curves are at z=0 with reflection, the green curves are at z=-L with reflection, and the blue curves are at either end with no reflection.Displacementu(r) (a) and (d), strain εrθ(r) (b) and (e), and strain εzθ(r) (c) and (f) are shown at the two ends of the transducer. Transverse coordinate r is relative to the fiber radius a. Scaling is arbitrary. The normalized frequency is γ=5.13767. Red (z=0) and green (z=-L) curves are for unit reflectivity of the s=1 mode back towards z=-L with phase Θ=0. Blue curve is for zero reflectivity and the same transducer amplitude U. (a), (b), (c), and (d) show the real parts, corresponding to times when u(1)=U. (d), (e), and (f) show the imaginary parts, corresponding to times when u(1)=0. High-frequency oscillations in some of the curves are a numerical artifact. Since εzθ(r) in the absence of reflection has opposite signs at z=0 and z=-L, the right-hand green plots have been multiplied by minus 1 for better comparison with the blue plots.
(a)(b)(c)(d)(e)(f)Displacementu(r) (a) and (d), strain εrθ(r) (b) and (e), and strain εzθ(r) (c) and (f) are shown at the two ends of the transducer. This is for the same conditions as in Figure 4, except that the phase of the reflected s=1 mode is 180∘.
(a)(b)(c)(d)(e)(f)In the caseΘ=0, PT=1.47𝒫 with reflection, but PT=2.96𝒫 with no reflection. Thus, reflection acts to reduce the power needed to drive the transducer to a given amplitude U but does not greatly affect the way the transducer vibrates. The modal efficiencies with reflection are Ps=0,+/PT=0.56%, Ps=1,+/PT=98.64%, and Ps=0,-/PT=0.07%. Ps=1,-/PT=25.76% propagates in each direction between the point of reflection and z=-L. Within the transducer Pt=1,+/PT=0.028% and Pt=1,-/PT=0.776 %. The amplitude at r=1 of the s=1 mode is 0.985U.In the caseΘ=180∘, PT=120.60𝒫; so it becomes much harder to drive the transducer to a given amplitude U. The modal efficiencies are Ps=0,+/PT=58.76%, Ps=1,+/PT=4.94%, and Ps=0,-/PT=36.18%. Thus, the transducer becomes a poor emitter of s=1 ultrasound, although a large power Ps=1,-/PT=1943.6% propagates in each direction in the region z<-L between the point of reflection and the left end of the transducer. Within the transducer Pt=1,+/PT=63.71% and Pt=1,-/PT=2.02%. The transducer motion is qualitatively quite different because of the reflection.In Figure6 we plot the efficiency Ps=1,+/PT as a function of Θ. We see that the efficiency is high over a broad range. On the other hand, without reflection 49.73% of the applied power PT is emitted into the s=1 mode in each direction, and the undesirable backward sound must be damped to prevent interaction with light in the fiber core.Figure 6
EfficiencyPs=1,+/PT as a function of the phase Θ of the reflected s=1 mode at z=-L.The transducer simulations described below are for no reflections atz<-L. Above the s=1 cutoff the applied power PT and the radiated power are only weakly dependent on L. Figure 7 shows the s=1 efficiency for each direction as a function of L at γ=5.13767. The s=0 and internal t=1 powers are much smaller than the s=1 power. The situation is different below the s=1 cutoff, where acoustic energy can leave the transducer only in the s=0 channel. This is illustrated in Figure 8 for γ=5.12, such that 2π/κ1=1.85. While the efficiency for generating the s=0 mode in each direction remains at 1/2 (red), PT goes to zero at resonances when L is a multiple of 2π/κ1 (blue). Consequently the ratio Pt=1/PT becomes large near these resonances (green). We expect that damping effects not included in our model will act to suppress these resonances, but it may be best to avoid them by a suitable choice of L.Figure 7
Efficiency fors=1 generation at γ=5.13767. Transducer length L is in units of a.Figure 8
Efficiency fors=0 generation (red) at γ=5.12 remains at 1/2, but PT (blue) becomes small near resonances. As a result the internal t=1 efficiency Pt=1/PT (green) is large at the resonances.In order to increase the frequencyΩ, so as to shorten the distance between the two transducers in an isolator, or to use a larger-diameter fiber, it is of interest to consider increasing γ above the cutoff for higher-order modes. Figure 9 shows the s=2 efficiency as a function of L at γ=8.41849, slightly above the Z2=8.41724 cutoff (red). This figure also shows the s=3 efficiency at γ=11.62075, slightly above the Z3=11.61984 cutoff (green). We see that, as desired, most of the acoustic power goes into the mode that is just above cutoff. Scaling to large Ω will eventually be limited by the increased attenuation of ultrasound at very high frequencies.Figure 9
Efficiencies for generating thes=2 mode (red) and the s=3 mode slightly above their cutoffs.Atγ=8.416, just below the s=2 cutoff, there is no dominance of s=1 over s=0. Figure 10 shows Ps=0/PT (red) and Ps=1/PT (green), as well as the internal resonances Pt=1/PT (blue) and Pt=2/PT (violet). The s=0 and s=1 efficiencies in each direction sum to 1/2.Figure 10
Efficiencies for generating thes=0 mode (red), the s=1 mode (green), the t=1 internal resonance (blue), and the t=2 internal resonance (violet) slightly below the s=2 cutoff.


## 5. Acousto-Optical Coupling, Acoustic Attenuation, and Thermal Effects

According to Engan [2] the coupling of the optical polarization states by phase-matched torsional acoustic waves is sinusoidal. That is, one polarization amplitude increases as sin(Knz), while the other decreases as cos(Knz). Here z is position (not in units of a) along the fiber. We call Knz the coupling angle. The coupling constant Kn for the s=n mode, provided that mode is above cutoff, is
(26)K0=(24.7m)(PW)1/2[125μm(2a)]2,Kn=K0Zn22|J1(Zn)|[1+(Znβn)2]-1/4,
where P is the acoustic power injected at z=0 into the phase-matched mode. Coupling of 50% of the light from one polarization to the other occurs over a distance Lc=π/(4Kn). For 1 W of power in a fiber with a 2.7 mm polarization beat length and a 125 μm diameter, the coupling length for the s=1 mode is Lc=3.54 cm and the phase-matching frequency is 49.06 MHz. For the same power and beat length, but a 250 μm diameter, the coupling length for the s=4 mode is Lc=3.58 cm and the phase-matching frequency is 70.66 MHz.When one takes damping of the sound waves into account, the power decreases exponentially after the sound leaves the transducer atz=0. This means that βn has an imaginary part even above cutoff. The coupling angle at position z now becomes [Kna/Im(βn)][1-exp(-Im(βn)z/a)]. This means that a coupling angle of π/4 is only possible if Lc<La, where the absorption length is defined as La=a/Im(βn). The acoustic power decays as exp(-2z/La). When there is damping the distance over which sufficient coupling occurs is greater than Lc.We assume that the damping of thes=0 mode is the same as that found for transverse sound waves in bulk fused silica. Room-temperature measurements by Krischer [9] in the 200 to 1000 MHz range found the power attenuation to be 5.7×10-18dB/μsec(f/Hz)2, where f=Ω/2π. This agrees well with the value given by Kul’bitskaya and Shutilov [10] but is smaller than the value 1.4×10-17dB/μsec(f/Hz)2 reported by Fraser et al. [11]. Measurements by Krause [12] at 590 MHz showed a decrease in attenuation with increasing temperature with a minimum at about 375 C. For the present discussion we assume that Krischer's result can be extrapolated to lower frequencies. Dividing by V and neglecting dispersion in the speed of sound, we find that Im(β0)/a=4.43×10-18Ω2sec2/m or β0=γ+i(a0/a)γ2, where a0=6.63×10-11m.For thes=0 mode β0/a is the total wave vector, and the transverse wave vector is zero. For higher-order modes we take βn=(β02-Zn2)1/2, since the transverse wave vector is Zn/a. Note that damping smears out the cutoff, and that βn has both real and imaginary parts on either side of the cutoff. Suppose that the beat length is LB=2.7 mm. For the example above of 2a=125μm and f=49.06 MHz, the absorption length for the s=1 mode is La=6.32 cm. The minimum power required at z=0 to achieve 50% optical coupling is P=0.313 W. The s=2 mode in this fiber at 80.39 MHz has La=1.44 cm and requires at least P=2.36 W. For the example 2a=250μm and f=70.66 MHz, the absorption length for the s=4 mode is La=2.12 cm and at least 2.87 W in this mode is required. Absorbed acoustic power can produce a temperature gradient along the fiber. This can cause a chirp in βn, adversely affecting phase matching with the optical field. On the other hand, the phase-matching acceptance increases when the AO coupling length decreases. Heating can also be caused by optical power in the cladding. Cladding light can be removed before the isolator by embedding a section of fiber in high-index material. Air flow past the fiber can also reduce temperature gradients.Even in the absence of temperature gradients and acoustic damping, the temperature dependence ofV [6] affects the cutoff frequencies and the phase-matching conditions. Figure 11 shows the axial sound wavelength 2πa/|β1| as a function of temperature for fibers with diameters 124.9 to 125.2μm. The frequency f=49.2406 MHz is chosen to give an axial wavelength of 3 mm at 20 C in a 125.0μm fiber. To the right of the cutoff resonances the ordinate is the distance over which the power decreases by 1/e2. If the fiber diameter were to be slightly different at the locations of the two transducers in an isolator, phase matching for both transducers at the same frequency could be maintained by having the transducers at different temperatures. Backward acoustic power produced by a transducer can be reflected by heating the fiber behind the transducer over a sufficient length to prevent tunneling through the region where the reflected mode is below cutoff. The phase Θ of the reflected light depends on how and where this heating is done.Figure 11
Axial wavelength (left of cutoff resonances) and1/e2 attenuation length (right of resonances) is shown as a function of temperature for several fiber diameters. The frequency is chosen to produce an axial wavelength of 3 mm at 20 C for a 125.0μm-diameter fiber.


## 6. Discussion

Using higher-order torsional acoustic modes near cutoff to couple optical polarization states in a birefringent fiber allows phase matching to the polarization beat length at high frequencies in the 50 MHz range. Two torsional-mode transducers producing 50% polarization coupling and separated on the fiber by about 1 m can be used as an in-fiber optical isolator suitable for use with narrow-band fiber amplifiers of arbitrary wavelength. We have presented an analytical and numerical model of a torsional-mode transducer. This model indicates that the mode just above cutoff radiates most of the acoustic power applied to the transducer, irrespective of the transducer length. In the absence of acoustic reflection the power is radiated equally in both directions, and undesirable backward radiation must be absorbed. Reflecting the backward radiation towards the transducer with a suitable phase can enhance the efficiency in the forward direction to almost 100%.Various types of transducers have been developed for exciting torsional vibrations in fibers or rods, but not at the high frequencies needed for an AO isolator. Transducers for exciting thes=0 mode in optical fibers have used a conical glass horn with the fiber mounted along its axis and shear-mode piezoelectric transducers attached to its base [1, 13–15]. Other torsional transducers have been developed which use paired [16] or segmented [17, 18] piezoelectric elements. Torsional oscillations in metallic rods have been produced by electromagnetic-acoustic transduction [19]. Silicon-based micro-electromechanical systems (MEMSs) technology may provide a route to making higher-frequency torsional transducers. We are working with Sandia National Laboratories to explore this possibility.



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*Source: 823157-2010-04-11.xml*