NATIONAL RADIO ASTRONOMY OBSERVATORY

CHARLOTTESVILLE, VIRGINIA

ELECTRONICS DIVISION INTERNAL REPORT No. 255

A SYNTHESIZED, 90 120 GHz SIGNAL SOURCE

J. W. ARCHER AND M. J. CRAWFORD,

DECEMBER 1984

NUMBER OF COPIES: 150

A SYNTHESIZED 90-120 GHZ SIGNAL SOURCE

J. W. Archer and M. J. Crawford, Jr.

Table of Contents

I. Introduction . . . . . . • • • • • • • • • 0 • • • • • • • • 1SII. The 26.5-40 GHz Frequency Synthesizer . . . 2 . . . . . . . . ... . . 2

A. General Description . . . . • .. . • • • • • • • • • • • • • 2B. Design of the UHF Synthesizers . . . . . • . . . . . . * • . 5C. The Coarse Tuning and Bias Modulation Amplifiers • • • • • . 11D. The Main 26.5-40 GHz Phase Lock Loop • • • • • • • • • . 14

III. The 90-120 GHz Frequency Tripler . . • • • • • • • • • • • • • .7

21IV. The Complete Synthesized LO Source . • • • • • • • • •. . . . . 2V. Summary . . . • • • • • • • • • • • • 41 • • • • • • • • • . . 27VI. Acknowledgements . . • • • • • • • • • • 0 • 0 • • • •. . . . . 28

Figures

Figure 1 26.5-40 GHz Synthesizer Block Diagram . . • • • • • 3Figure 2 0.88-1.32 GHz Synthesizer Schematic . . • •• • • • • 7Figure 3 ROM and 9's Complement Encoder SchematicFigure 4(a)

(d)

Spectrum of 1.76-2.64 GHz Synthesizer Output• 9

Spectrum of 1.76-2.64 GHz Synthesizer Output • • •

.• • • . . 10

400-500 MHz Reference Signal Spectrum . .

.I.F. Spectrum in Main Loop . . • • . • • •

•

• • • • •• •.

•

. . . 12

:Figure 5

c

Tuning Coil Driver Schematic . • • • • ••••••

(b) 0(c) 51 . 14

Figure 6 Harmonic Mixer Triplexer Schematic . • • * • • • • •Figure 7 Sweep Generator Schemati . . • . . • • . . • • •. . . 18Figure 8 FM Coil Driver and Loop Amplifier Schematic • • • •

Figure 10. . . .ripler .

• • •

!!

Figure 9(b) Tripler Block: Cross-Sectional ViewOutput Power vs Output Frequency for T

Figure 11 Tripler Conversion Efficiency vs Input Power

. . 23Figure 9(a) Tripler Block: Cross-Sectional View . • • * • • • •

Alone and for Complete Signal Source . • . . .. . 26• . .

References . • • • • • • • • • • • • • • • • •• • • • . . • . 29

A SYNTHESIZED 90-120 GHZ SIGNAL SOURCE

J. W. Archer and M. J. Crawford, Jr.

I. Introduction

The advantages of all-solid-state millimeter wavelength receivers have

been clear to system designers for many years. Substantial savings in cost

and weight, and significantly enhanced system reliability, can be achieved with

a completely solid-state design. Until recently, achieving a widely tuneable

solid-state local oscillator system has proven to be a significant obstacle

to the development of broadband heterodyne receiver systems of this type.

Developments in millimeter wave harmonic generator design [1],[2] Gunn oscillator

technology [1],[3] and the reduction in the LO power requirements for heterodyne

receivers through the use of improved, cooled Schottky diode [4] [5] or super-

conducting mixer [6],[71 elements have now made it feasible to realise practical

receivers with solid state LO's. In many applications, frequency and/or phase

stability of the LO source is of prime importance. The construction of a highly

stable, widely tuneable synthesizer [8], such as described here, is therefore

a significant development.

The following sections of this paper will describe the design and construction

of the 26.5-40 GHz frequency synthesizer. Performance data will be given, which

illustrate the frequency stability, output power and spectral purity of the

phase locked source. The design of the frequency tripler is then described

and performance curves are given. Finally, data is presented showing the performance

of the complete synthesized LO source.

II. The 26.5-40 GHz Frequency Synthesizer

A. General Description:

The principal millimeter wavelength signal source in the LO system is a

YIG tuned GaAs Gunn oscillator manufactured by Watkins Johnson, Inc. (Model

WJ-5610-302F). This oscillator may be electronically tuned between 26.5 and

40 GHz by varying the magnetic field applied to a spherical YIG resonator to

which the Gunn diode is coupled. The magnetic field is produced by current

flowing in the coils of an electromagnet, whose pole pieces enclose the YIG

element. As the tuning coil current is varied linearly from 660 mA to 1015

mA, the oscillator frequency varies in a smooth, almost linear response from

26.5 to 40 GHz. The peak deviation from linearity is about -60 MHz near the

upper and lower tuning limits. The tuning coil resistance is about 10 ohm

with an inductance of 160 mH. Another electromagnetic circuit is provided to

enable fine tuning of the oscillator frequency. This coil gives a sensitivity

of 125 kHz/mA with a maximum current of + 800 mA, resulting in a peak attainable

deviation of + 100 MHz. In order to achieve the flattest output power response

as the output frequency is varied, the supply voltage to the Gunn diode must

be changed linearly and in synchronism with the tuning coil current - at 26.5

GHz the optimum Gunn bias is 5.2 volts and at 40 GHz the optimum bias is 3.4

volts. When the bias voltage is controlled in this manner, the output power

over the full tuning range is +13 dBm + 1 dB.

Figure 1 a block diagram of the 26.5 to 40 GHz synthesizer system, shows

how the YIG tuned oscillator is incorporated into the phase lock system. The

coarse tuning coil current and Gunn diode bias are derived by digital to analog

conversion of the BCD-encoded frequency select input, so that the initial oscillator

frequency is set as near as possible to the desired output frequency. An automatic

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fine frequency sweep signal can be injected at the input of the coarse tuning

coil bias amplifier in order to tune the oscillator close enough to the desired

frequency for lock acquisition. The microwave output from the YIG oscillator

is fed through a broadband waveguide isolator and then sampled by a 20 dB cross-

guide coupler. The sampled signal is fed to a harmonic mixer (Hewlett-Packard

Model 11517A) where it is mixed with the 15th harmonic of a 1.76-2.64 Gilt reference

signal. This signal is generated by extracting the second harmonic of the output

of one of two UHF frequency synthesizers in the system, both of which are locked

to a common, highly stable, 10 MHz reference signal. The frequency of the 2 GHz

reference is controlled by the first three digits of the frequency select input

data. Decimal 4 is subtracted from this number to correct for the 400 MHz offset

of the IF reference synthesizer and its 9's complement code generated, in order

to derive the required preset data to determine the division modulus for the

programmable divider in the UHF synthesizer. A numerical example will help

in understanding the relationships:

Let the selected frequency be 3j 543 1 GHz (no special significance).

The division modulus will be 316 - 11 = 312. The output frequency from the UHF

synthesizer will be (10 MHz/12) x 312 x ii = 1040 MHz. Its second harmonic component,

which is fed to the harmonic mixer, will be 2080 MHz. When the YIG oscillator

is tuned to the desired frequency, the IF output frequency from the harmonic

mixer will be 31,654.3 - 15 x 20 80 = 454.3 MHz.

The IF output from the harmonic mixer is amplified and fed to a phase detector

where it is correlated with a signal derived from the second UHF synthesizer.

The frequency of the ssoond synthesizer is controlled by the remaining three

digits of the frequency select command and incorporates a fixed frequency offset

of 1100 MHz. Thus, in the example above the output frequency would be

400 + 54.3 = 454.3 MHz, which is exactly the required frequency if the YIG tuned

oscillator is to lock at 31.6543 GHz. The output of the phase detector is filtered,

amplified and fed back to control the phase of the YIG oscillator via the bias

applied to the fine tuning (FM) coil.

The use of separate synthesizers for coarse and fine control of the reference

frequencies is essential if acceptable phase noise is to be achieved in the

spectrum of the locked millimeter wave oscillator. The phase noise of the output

signal, within a loop bandwidth separation from the carrier, will be determined

primarily by the phase noise characteristics of the harmonic mixer reference

signal. If only the 1.76-2.64 GHz reference is made variable and the other

reference is fixed at, say, 400 MHz, it would be necessary to operate the phase

detector at 833 Hz in the remaining synthesizer to achieve a 100 KHz increment

in the millimeter wave output signal. Since the carrier-to-noise ratio for

phase noise degrades as the square of the frequency ratio, the FM noise

characteristics of the primary reference oscillator would be degraded by about

70 dB in the final output spectrum - clearly an unacceptable situation for practical

oscillators. By controlling the frequency of both reference signals and carrying

out fine frequency adjustment using an IF frequency offset, the phase noise

degradation is reduced to about 40 dB, which is acceptable when a high quality

10 MHz reference oscillator is employed.

B. Design of the UHF Synthesizers:

The 1.76-2.64 GHz and 400-500 MHz synthesizers are very similar in design,

using essentially the same digital circuitry for prescaling, variable modulus

division and phase/frequency detection. The significant differences are the

different reference frequencies (833 kHz vs 25 kHz), the number of variable

modulus counter stages (3 vs 4) and the manner in which the frequency select

5

digits are derived. Because of the similarities, only the 1 .76-2.64 GHz synthesizer

circuit will be described in detail.

In this case, because of the technological constraints on prescaler performance,

the phase lock loop operates at half the desired output frequency, i.e.,

0.88-1.32 GHz. The oscillator employed is a varactor tuned transistor oscillator

(EMF VT0-JIB) which provides more than +13 dBm over the fundamental frequency

range and -25 dBm + 2 dB at the second harmonic. The output from the oscillator

is split by a 3 dB power divider. One output from the divider is further attenuated

by 10 dB and fed to a divide by 4, ECL prescaler. The other output is passed

through a bandpass filter, which passes the desired second harmonic component

but rejects the fundamental and other higher order harmonics from the oscillator.

The filter output is fed to a variable gain, broadband power amplifier chain

with a total maximum gain of 40 dB, boosting the signal power to a nominal maximum

of +15 dBm. A second identical bandpass filter follows, before the reference

signal is coupled to the harmonic mixer. The second filter prevents noise from

the power amplifiers reaching the high gain, low noise IF chain of the millimeter

wave phase lock loop.

The fixed modulus, divide by 4, ECL prescaler (Plessey SP8611B) at the

input of the digital divider chain is followed, as shown in Figure 2, by a dual

modulus (+10/ill) ECL counter (11C90). This counter is interconnected with

a series of synchronously clocked, presetable high speed TTL BCD decade counters

(70160) to implement a variable modulus counter using pulse swallowing techniques

[9]. The use of the Schmitt trigger (74S14) to generate the synchronous clock

signal for the 74E 1 160 counters helps eliminate false clocking problems encountered

at the higher input frequencies. Printed circuit, 50 ohm microstriplines are

used to couple the high frequency signals to the 5P6611B and 11C90 counters.

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holes.

The division modulus preset digits to the programmable counters are derived

using 9's complement encoders, one channel is illustrated in Figure 3. The

subtract decimal 4 function is performed prior to 9's complement encoding using

a look-up table stored in a set of read only memories. The complete circuit

and table are given in Figure 3. The output signal from the programmable divider

is fed, via a level translating resistor network, to an ECL phase frequency

detector (12040). The 833 kHz reference input for the detector is derived from

the 10 MHz standard using a divide by twelve, 74LS92 counter. The output pulses

from the phase detector are coupled to an active second order loop filter/integrator

with adjustable damping controls. An AM-464 (Analog Devices) operational amplifier

is used, which is capable of handling the high voltages required to directly

bias the tuning varactor in the VCO for complete coverage of the oscillator

tuning range. A common problem with a loop of this type is the appearance of

spurious components in the spectrum of the locked oscillator spaced at harmonics

of 833 kHz from the desired output frequency. These arise because of insufficient

filtering of the sharp output pulses from the phase/frequency detector at the

varactor bias output. In the present design, with a loop natural frequency

of about 20 kHz [10], RC pulse prefiltering (0.01 g capacitors in the input

resistor network) and a series resonant LC trap at the op-amp output are used

to reduce the amplitude of the spurious signals to acceptable levels. Photographs

of the typical output spectrum (at 2 GHz) from the 1.76-2.64 Grit synthesizer,

shown in Figures 4(a) and 4(b), demonstrate that the unwanted components are

at least 60 dB below the carrier. A simple lock indicator circuit is implemented

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As for a) but with horizontal scale = 500 KHz/div.

Fig. 4. Photographs of typical signal spectra at importantmonitor points in the synthesizer system.

10

using a differential amplifier to detect the presence of a frequency correction

signal from the 12040 followed by a dual threshold comparator which gives a

5 volt output signal when the loop is unlocked.

Figure 4(c) shows the typical output spectrum from the 400-500 MHz synthesizer.

The VCO used in this phase locked loop is an Avantek 8040 varactor tuned device.

A bandpass filter is required between oscillator and prescaler to eliminate

false triggering of the divider due to the second harmonic component at the

output of the VCO. In this loop, four 74F160 counters are used to implement

the variable modulus counter, but the most significant digit is fixed at a count

of 4. The code for the 3 remaining digits is a 9 1 8 complement encoded version

of the last three digits of the frequency select command input.

C. se

Figure 5 gives a schematic diagram of the coarse tuning coil current driver

and Gunn diode bias modulator. A pair of three digit BCD, digital-to-analog

converters are used to generate an analog voltage from the BCD frequency select

input. The resultant tuning voltage at the output of the summing amplifier

A is equal to the selected frequency in GHz divided by 10. This voltage drives

a linear voltage to current converter (op-amp B and ECG261 transistor) whose

gain and offset can be adjusted so that the YIG tuned oscillator frequency is

as close as possible to the desired locking frequency. Coil current is sensed

by a precision 1 ohm resistor in series with the windings. The output voltage

from amplifier A is also used to control the bias voltage applied to the Gunn

diode in order to minimize the variations in YIG oscillator output power with

operating frequency. The voltage from amplifier A is fed to non-inverting amplifier

C, which has a voltage gain of 3.3 and includes an adjustable offset control.

The output from this amplifier is fed via a 14.3K resistor to the control input

11

a) The 400-500 MHz reference signal to the phase detectorquadrature hybrid - set at 450 MHz. Analyzer B.W. = 3 KHz,horizontal scale = 20 KHz/div., vertical scale = 10 dB/div.

The spectrum of the IF signal at the input to the phasedetector - YIG oscillator locked at 30.450 GHz.Analyzer B.W. = 30 KHz, horizontal scale = 100 KHz/div.,vertical scale = 10 dB/div.

Fig. 4. Photographs of typical signal spectra at importantmonitor points in the synthesizer system.

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sensitivity of the inverting control input is set by a variable 10K feedback

potentiometer connected between the regulator output and ground. By suitably

adjusting the gain and offset controls, the Gunn bias voltage can be made to

vary linearly from 5.2 to 3.6 volts as the tuning voltage varies from 2.65 to

4.0 volts. The 1N1186 diodes connected between the Gunn diode and the regulator

provide a constant voltage drop of 1.2 volts, allowing the LAS15U to operate

at output voltages between 6.8 and 4.8 volts, which are above its minimum output

voltage limit of 4.0 volts. The zener diode and fuse protect the Gunn diode

against overvoltage conditions that might occur in the event of failure of the

regulator or other circuit element.

Op-amp D, connected as a comparator, is used to prevent an incorrect input

code from causing the application of an excessive bias voltage to the Gunn

oscillator. Should a BCD input number be selected which is less than 26.5 GHz,

the comparator output swings positive, forcing the tuning voltage to remain

constant at 2.65 volts. If the selected frequency is above 40 GHz, then the

Gunn voltage will be below 3.5 volts and the tuning coil current is limited

to a safe value of less than 1.5 amps by the internal resistance of the windings.

D.

As described previously, a ample of the YIG tuned oscillator output is

fed to a Hewlett Packard harmonic mixer where it is mixed with the 15th harmonic

of a reference signal in the range 1.76-2.64 GHz. The reference signal, mixer

bias and IF output signal are coupled to and from the single coaxial port of

the mixer using a triplexing filter shown schematically in Figure 6. The triplexer

is comprised of a pair of three-element, lowpass filters which isolate the hie)

power, 2 GHz reference signal from the 450 MHz IF amplifiers, and both of these

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signals in turn from the mixer DC bias input. DC blocking capacitors are provided

at the RF and IF ports. The triplexing filter was fabricated using microstripline

techniques on aluminum-backed, Teflon fiberglass dielectric material.

The harmonic mixer, which has widely varying sensitivity over the range

1.76-2.64 GHz, is operated in a zero voltage bias mode at a constant forward

current of 4.8 mA. The bias current is held constant by adjusting the power

of the 2 GHz input using a servo loop (S11010, in Figure 6), which controls the

gain of the reference signal power amplifier. Operation at a constant bias

current ensures a more uniform sensitivity for the harmonic mixer between 26.5

and 40 Gliz and reduces variations in the IF power at the phase detector.

The 400-500 MHz IF output from the triplexer is passed to a lowpass filter

(500 MHz cutoff), which further attenuates the 2 GHz reference signal, before

being fed to a low noise, high gain amplifier (3 dB NF, 45 dB gain). The first

amplifier is followed by a 400-500 MHz bandpass filter, a monitor directional

coupler, a limiting amplifier and a 10 dB attenuator, resulting in a nominal

input power to the phase detector power divider of +3 dBm. The reference signals

for the two double balanced mixer phase detectors are derived from the amplified

400-500 MHz synthesizer output using a quadrature hybrid. Nominal input power

to the hybrid is +3 dBm.

In order for the loop to be able to acquire lock, the difference frequency

between the IF signal from the harmonic mixer and the phase detector reference

signal must be less than the bandwidth of the loop filter (about 500 KHz).

This will not be the case when the YIG oscillator frequency is preset by the

coarse tuning coil because of the deviation of the tuning current vs frequency

response from linearity. Nevertheless, the difference frequency should be less

than 60 MHz for the oscillator used here. Provision is made in the design of

the coarse tuning coil driver amplifier for the injection of a small sweep offset

voltage which can be used to bring the YIG oscillator frequency within the

lock range of the loop.

The sweep circuit is illustrated in Figure 7. The sweep function is implemented

digitally, a technique which has significant advantages over an analog method.

A 256 Hz clock pulse generated by a 555 timer is fed via a control gate to a

cascade of two 741,8193 binary up/down counters. The counter outputs are coupled

to an eight-bit D/A converter, which generates a repetitive voltage ramp as

the counters are clocked. The voltage ramp is fed via an appropriate scaling

resistor to the input of the coarse tuning coil driver amplifier, resulting

in a modulation of the YIG oscillator frequency by about + 100 MHz in synchronism

with the sweep voltage. When the YIG oscillator frequency comes within the

capture range of the loop (about 1 MHz) and lock is acquired, a voltage comparator

connected to the output of the quadrature phase detector senses the locked condition

and generates a +5 volt signal which disables the clock to the sweep counters.

The coarse tuning bias is thus latched at the condition at which lock was acquired.

A problem that has been encountered with the YIG oscillator used here is

significant frequency vs temperature dependence. In operation, after the loop

is locked, ambient temperature Changes can cause the oscillator to drift out

of the range of the loop correction signal. A simple addition to the sweep

circuit has enabled this problem to be overcome. As shown in Figure 7, the

current in the YIG oscillator FM coil is converted to a suitable proportional

voltage and sensed by a dual threshold comparator with hysteresis which is

triggered should the correction voltage exceed + 2 volts (available range is

+ 4 volts at a sensitivity of 0.1V/A). The comparator outputs control gates

which feed the clock signals to the up or down clock inputs of the binary counter

1 7

2 x

AMPL

IFIE

RSM

CL—

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BPF

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200

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. 7. T

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amp

gene

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r us

ed t

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he Y

IG o

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lato

r fr

eque

ncy

unti

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acq

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ed.

A d

etai

led o

per

atio

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des

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tion i

s g

iven

in

th

e te

xt.

cascade: If the FM coil current exceeds the threshold level, the clock is applied

to the counters in such a way as to change the coarse tuning voltage to result

in a reduction of FM coil current magnitude. A 0.5 volt hysteresis for the

comparator thresholds provides an overcorrection safety margin.

The FM coil driver and loop filter functions are combined in a single circuit,

shown in Figure 8. An LH0022 FET input op-amp is used in conjunction with a

diode biassed, complimentary-darlington connected, transistor power amplifier

to implement the FM coil driver, voltage to current converter circuit. This

configuration is capable of delivering currents of + 0.8 A to bias the FM coil,

with current limiting provided by 0.5 ohm emitter resistors at + 1.0 A. Coil

current is sensed by a precision 10 ohm resistor in series with the ground side

of the coil. When connected as an amplifier with a gain of 10 V/A (feedback

capacitor and damping resistor replaced with 10K) the amplifier small signal

bandwidth is greater than 1 MHz and crossover distortion is undetectable at

the output for a 5 volt peak to peak sinusoid at the input, for frequencies

below 50 KHz. When configured as an integrator for the loop filter function,

the 0.01 gF feedback capacitor and 10K input resistor result in a loop natural

frequency of about 150 KHz (phase detector sensitivity, K d = 0.25 V/rad, oscillator

sensitivity, Ko = 7.85 x 105 rad/sec/mA). As can be seen from Figure 8, the

feedback capacitor and damping resistor are shunted by an 18M resistor. Limiting

the DC gain (to 1800) in this manner aids in lock acquisition by keeping the

coil driver amplifier from latching in a current limiting state with the loop

in the unlocked condition. The 0.18 sec time constant introduced by the extra

gain limiting resistor in the feedback path does not significantly affect the

behaviour of the loop. An offset trim control is provided at the op-amp in

19

6

2 2K

10K

IOW

D45

C8

+15

0-10

0,01

. T

he

circ

uit

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gra

m o

f th

e F

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dri

ver

am

pli

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whic

h i

nco

rpora

tes

the

loo

p f

ilte

r fo

r th

e Y

IG o

scil

lato

r p

has

e lo

cked

loop.

DE

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2N 3

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DES

IN

914

610

0

100

MM

5416

order to allow compensation for the DC offset associated with the balanced mixer

phase detector.

Figure 4(d) shows'the spectrum of the IF signal measured at the IF monitor

coupler output with the YIG oscillator phase locked at 30.4500 GHt. The spectrum

is free of spurious non-harmonically related components to at least 30 dB below

the carrier. The noise side bands characteristic of a spectrum from a phase

locked oscillator with a 3 dB loop bandwidth of about 400 KHz are clearly seen.

The 90-120 GHZ Frequency Tripler

The frequency tripler employs a split block construction which has been

successfully used in a number of different frequency multiplier designs [1],[11].

Details of the multiplier design are given in Figure 9. The tripler is a

geometrically scaled version of a design used at 200-290 Wiz [11].

Power incident in the full height 14111-28 input waveguide is fed to the varactor

diode via a tuneable probe transition and a seven-section suspended substrate

lowpass filter, which passes the pump frequency with low loss, but is cut-off

(fo = 56.5 GHz) for higher harmonics. The transmission line and channel dimensions

for the stripline filter were directly scaled by a factor of 1.89 from the higher

frequency design [11]. The varactor chip, a 0.1 mm sided cube, is mounted on

the filter substrate adjacent to the reduced height output wavegpide. One of

the many diodes on the chip is contacted and coupled to the output waveguide

with a post mounted, 0.31 mm long x 0.0125 mm diameter, phosphor bronze whisker,

which has been suitably pointed and prebent. Output tuning is accomplished

with the aid of an adjustable backshort in this guide. DC bias is brought to

the device by a transmission line filter. The design of the filter has been

described extensively in other papers [11] - it will suffice to state that the

21

_T_

3. 5

6CO

NTACTIN

GBACKSH

ORT

WH

ISKER

PIN

OU

TPU

T G

UID

EW

ITH

WH

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ON

TACTED

DIO

DE C

HIP

WAVEG

UID

ETO

STRIP

LIN

ETRAN

SIT

ION

••

2.3

4

Fig

. 9. a

) A

vie

w o

f th

e 95

-120

GH

z tr

iple

r bl

ock,

spl

it a

long

the

par

titi

on b

etw

een

bloc

ks, s

how

ing

the

inpu

t gu

ide,

the

str

ipli

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ss f

ilte

r, t

he b

ias

circ

uit

and

the

outp

ut w

aveg

uide

. Dim

ensi

ons

in m

illi

met

ers.

SECTIO

N A

A

**.

.0

0

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D

TRAN

SFO

RM

ER D

IMEN

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WH

ISKER P

IN

WAVEG

UID

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AN

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ESU

BST

RATE

STEP

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HT

02.4

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8

12.2

80.6

1

1.8

40.7

8

31

650.8

3

INPU

TW

AVEG

UID

E

b )

Fig

. 9.

A s

ecti

on t

hro

ugh t

he

blo

ck d

etai

ling t

he

wav

egu

ide

tran

sfor

mer

and

dio

de m

ount

ing

arra

ngem

ent.

bias line approximates a quarter-wave, short circuited stub at 50 GHz, thus

minimizing the effect of the bias circuit on the performance of the lowpass

filter near cut-off.

A quarter-wave, two section impedance transformer couples the 2.48 mm x

0.48 mm reduced height guide to the 1.66 mm x 0.83 mm output guide. Power can

flow in the wider guide at the second harmonic, whereas the output guide i

out off at this frequency. The transformer is thus used to implement a reactive

second harmonic idler termination by spacing it approximately X g/2 (at the second

harmonic wavelength) from the plane of the diode.

The varactor diode is a Schottky-barrier device fabricated by R. Mattauch

at the University of Virginia (designated 8P2) with a zero bias capacitance

of 28 fF, a DC series resistance of 10.3 ohms and a breakdown voltage of 20

volts at uA. These devices have a highly non-linear capacitance versus voltage

law which approximates the inverse half power behaviour of an ideal abrupt junction

varactor to within 5 volts of the breakdown limit.

The performance of the multiplier has been measured at 1500 MHz intervals

for output frequencies between 90 and 120 GHz. The output power response as

a function of output frequency for constant 50 MW pump power is shown in Figure

10. Backshort tuning and DC bias were optimized at each measurement frequency.

Typically the bias conditions for optimum performance were a reverse bias voltage

of about 4 volts and a forward current between 1 mA and it mA. More than 2 MW

output power is obtained at any frequency between 90 and 120 GHz, corresponding

to a minimum conversion efficiency, for 50 mW pump power of 4%. The peak output

power obtained was 4 mW at 110 GHz, corresponding to an efficiency of 8%.

Figure 11 shows how the multiplier conversion efficiency varies with pump

power at three different output frequencies. Bias and tuning were optimized

211

x,.

• • •

iv°

XX

— X

—

\X

‘

■X°.

..4(

)(.4

W

.•••

•....

S...

...

10

OU

TPU

TPO

WER

(14 W

)

9010

512

0O

UTP

UT

FFtE

CLU

ENCY

(G

FIz)

Fig

. 10.

Outp

ut

pow

er v

ersu

s o

utp

ut

freq

uen

cy f

or

the

trip

ler:

A)

at c

onst

ant

50 m

W i

nput

pow

er (

from

a k

lyst

ron

sour

ce)

and

B)

whe

n pu

mpe

d by

the

26.5

-40

GH

z Y

IG o

scil

lato

r.F

or

curv

e A

), t

he

trip

ler

bia

s an

d t

un

ing

wer

e o

pti

miz

ed a

t ea

ch f

requen

cy,

wher

eas

for

curv

e 1

3)

the

tun

ing

was

op

tim

ized

bu

t th

e b

ias

was

fix

ed, as

des

crib

ed i

n t

he

text.

EFFIC

IEN

CY

Yo)

50

INPU

T P

OW

ER (

mW

)

Fig

. 1

1.

Co

nv

ersi

on

eff

icie

ncy

ver

sus

pu

mp

po

wer

at

thre

e dif

fere

nt

outp

ut

freq

uenc

ies.

Bia

s an

d tu

ning

wer

e op

tim

ized

at

each

mea

sure

men

t po

wer

.

for best performance at each pump level. Although the tripler can safely handle

input powers of up to 120 mW, the best conversion efficiency occurs at input

powers of about 30 mW.

IV. The Complete Synthesized LO Source

Figure 10 shows the output power response of the complete synthesized LO

system, with the tripler pumped by the phase locked, YIG-tuned Gunn oscillator.

More than 1 mW output power is available at any frequency between 90 and 120 GHz

when the tripler tuning is optimized at each operating frequency. The tripler

bias was fixed at a voltage of 3.5 volts for these measurements. The tuning

curves (position vs operating frequency) for the tripler backshorts are monotonic

and very repeatable. Motorized servo tuning of the multiplier backshorts could

easily be implemented automatically by using the frequency select input, resulting

in completely automatic operation of the synthesized local oscillator system.

V. Summary

The synthesized 90-120 GHz local oscillator system described in this paper

was designed for use with cooled Schottky diode or SIS mixer heterodyne radiometers.

The system is fully automatic in operation and exhibits adequate output power,

wide tuning range and excellent frequency stability, making it an ideal choice

for application as an LO source in millimeter-wave spectrometer receivers.

There clearly exist other areas of application for such a signal source. Some

possibilities are: i) as a phase stable local oscillator for the receivers

in a phase coherent millimeter wave antenna array, ii) as a synthesized swept

frequency signal generator for laboratory test applications. The unit described

here is to be incorporated in the near future into a 100-120 GHz SIS receiver

27

system [12] to be installed on the NRAO 12 meter diameter radio telescope near

Tucson Arizona.

VI. Acknowledgments

The authors gratefully acknowledge the assistance of N. Horner Jr. who

assembled the tripler block and G. Taylor who fabricated the tripler mount.

Prof. R. Mattauch of the University of Virginia is thanked for providing the

Schottky diodes used in the multiplier. Thanks also go to M. Balister who provided

helpful comments and advice during the construction of the synthesizer.

28

References

1. J. W. Archer, "All Solid-State Receiver for 210-2 110 GHz," IEEE Trans on

MIL , vol. MTT-30 p. 1247, August 1982.

. . R. Erickson, "A High Efficiency Frequency Tripler for 230 GHz " Proc.

12112/ar,„Ktan..2,011, (Helsinki, Finland), p. 288, Sept 1982.

J. E. Carlstrom, R. L. Plambeck and D. D. Thornton, "A 60-115 GHz Tuneable

Gunn Oscillator" submitted for publication to IEEE Traus. on MTT,

August 1984.

. C. R. Predmore N. R. Erickson, P. F. Goldsmith and J. L. R. Marrero, "A

Broadband Ultra Low-Noise Schottky Diode Mixer Receiver from 80 to

115 GHz," IZELIrana,QAM., vol. MTT-32, p. 1198, May 19811.

. 14. Archer and M. T. Faber, "A Very Low-Noise Receiver for 80 to 120

GHz, Int. J. 1.R. and MM-Wav_es vol. 5, no 8, p. 1069, August 19811.

6. S-K. Pan, M. J. Feldman, A. R. Kerr and P. Timbie, "A Low Noise 115 GHz

Receiver Using Superconducting Tunnel Junctions, h ,

vol. 43, p. 786, 1983.

7. L. R. D'Addario, "A 90-120 GHz KS Mixer Having Gain and Wide Bandwidth,"

'Qt. J. 1,R. and MM-Waves, vol. 5, no. 10, October 19811.

8. F. M. Gardner, "Phaselock Techniques", p. 208, John Wiley, New York, 1979.

9. "Pulse Swallowing Revisited," Fairchild ECL Data Book, p. 9-56/581, Fairchild

Camera and Instrument Corp., Mountain View, CA, 1977.

10. F. M. Gardner, ibid, p. 11.

11. J. W. Archer, "An Efficient 200-290 GHz Frequency Tripler Incorporating

a Novel Stripline Structure," IEEE Trans. on MTT, vol. MTT-32,

p. 1116, April 19811.

29

12. J.W. Archer, "A High Performance 2.5K Cryostat Incorporating a 100-120

GHz Dual Polarization Receiver", submitted for publication to Rev,

ad".....Ingda7,4 October 1984.

30