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IEEE TRANSACTIONS ON VERY LARGE SCALE INTEGRATION (VLSI) SYSTEMS 1
A Low-Power Gigabit CMOS Limiting Amplifier
Using Negative Impedance Compensation
and Its Application
Jungwon Han, Student Member, IEEE, Kwisung Yoo, Dongmyung Lee, Student Member, IEEE,
Kangyeop Park, Student Member, IEEE, Wonseok Oh, Member, IEEE, and Sung Min Park, Member, IEEE
Abstract—This paper presents a low-power, gigabit limiting
amplifier (LA) for application to optical receivers that employ the
negative impedance compensation technique not only to enhance
the gain and bandwidth characteristics simultaneously, but also
to allow low-voltage, low-power operations. Test chips of the LA
were implemented in a standard 0.18- m CMOS process, demon-
strating 2.5-Gb/s operation with 40-dB gain, 0.053-UI rms jitter
for ��� � pseudorandom bit sequence inputs, 9.5-mV
��
input
sensitivity for �� �� bit error rate (BER), and 5.2-mW power
dissipation from a single 1.2-V supply. The chip core occupies
the area of only 0.25 0.1 mm�. The proposed LA was adopted
to realize a low-power, gigabit optical receiver. Fabricated using
the same 0.18- m CMOS technology, the measured results of
the optical receiver chip reveal 132.6-dB � transimpedance gain,
2.7-GHz bandwidth even with a large 1.5-pF input parasitic
capacitance, 16-dBm optical sensitivity for 10 �� BER, and
51-mW power dissipation from a single 1.8-V supply. The area of
the whole chip is 1.75 0.45 mm�.
Index Terms—CMOS, DC-balanced transimpedance amplifier,
limiting amplifier, negative impedance compensation, optical re-
ceivers.
I. INTRODUCTION
T HE proliferation of Internet access and multimedianetworks has mandated the development of high-speed
communication for enormous data. Therefore, optical com-
munications have become very attractive even for short-reach
applications, because optical communication systems can
provide a number of advantages over copper-based systems,
such as wider bandwidth, lower loss, lower crosstalk and elec-
tromagnetic interference. Although most commercial products
of optical systems have been implemented by using costly
Manuscript received August 21, 2010; revised November 25, 2010; accepted
December 21, 2010. This work was supported by the Basic Science Research
Program through the National Research Foundation of Korea funded by the
Ministry of Education, Science, and Technology under Contract 20100001557.
J. Han, and S. M. Park are with the Department of Electronics Engineering,
Ewha Womans University, Seoul 120-750, Korea (e-mail: hjw.jasmine@gmail.
com; smpark@ewha.ac.kr).
D. Lee and K. Yoo were with the Department of Electrical and Electronic
Engineering, Yonsei University, Seoul, 120-749, Korea, and now are with the
Semiconductor R&D Center, System LSI Business, Samsung Electronics Co.,
Ltd., Gyeonggi-Do 446-711, Korea.
K. Park is with the Department of Electrical and Electronic Engineering,
Yonsei University, Seoul 120-749, Korea.
W. Oh is with Korea Electronics Technology Institute, Seongnam 463-816,
Korea.
Digital Object Identifier 10.1109/TVLSI.2010.2104333
technologies such as GaAs, InP-based HBTs or SiGe HBT pro-
cesses, CMOS technologies have been rapidly advanced over
the past decades. Thus, the currently available, low-cost CMOS
processes enable the fabrication of gigabit front-end circuits on
a single silicon substrate along with other digital circuitry. Yet,
deep-submicron CMOS devices demand significant scaling,
i.e., low-voltage operations, thereby requiring novel circuit
techniques to facilitate the stringent design constraints.
A number of broadband techniques have been introduced to
achieve wide bandwidth, including inductive peaking, reverse
scaling, active feedback, and modified Cherry-Hooper. How-
ever, the inductive peaking technique requires either a large
chip area to implement passive inductors [1], [2] or a high
supply-voltage to realize active inductors [3]–[5]. The reverse
scaling technique may increase the power consumption due
to the additional buffers [3], while the active feedback tech-
nique needs large power dissipation to compensate the reduced
DC-gain [6]. Finally, the modified Cherry-Hooper topology
with negative capacitance still suffers the voltage-headroom
issue, thus requiring zero- transistors [7].
In this work, the negative impedance compensation technique
is incorporated to realize a low-power, low-voltage, gigabit lim-
iting amplifier (LA) with a very small chip area [8]. Also, the
proposed LA is applied to realize a low-power, gigabit optical
receiver which consists of a DC-balanced transimpedance am-
plifier (TIA), the LA, and an output buffer.
Section II presents the architecture of the proposed,
low-power, low-voltage LA. Section III demonstrates the
measured results of the LA. Section IV describes the architec-
ture of the differential optical receiver and the building blocks
with its experimental results. Finally, the conclusion follows in
Section V.
II. CIRCUIT DESCRIPTION: PROPOSED LA
Typically, a front-end optical receiver consists of a TIA, an
LA, and a clock and data recovery (CDR) circuit. Among these
blocks, LA particularly mandates high-gain and wide-band-
width characteristics in order to guarantee the reliable operation
of the following CDR circuit and to avoid intersymbol inter-
ference (ISI) problems. In addition, it requires low noise
characteristic to avoid degrading the input sensitivity even
under a low supply voltage.
Fig. 1(a) presents a conceptual schematic diagram of a
conventional voltage amplifier, where the voltage gain is deter-
mined by the transconductance and the output impedance
1063-8210/$26.00 © 2011 IEEE
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2 IEEE TRANSACTIONS ON VERY LARGE SCALE INTEGRATION (VLSI) SYSTEMS
Fig. 1. Conceptual schematic diagrams of (a) a conventional voltage amplifier
and (b) the improved voltage amplifier with negative impedance.
. Although higher load resistance increases the midband
voltage gain, it may incur a significant voltage drop across the
resistor, thus prohibiting low-voltage operations.
A novel remedy is to add a negative resistance in parallel with
the load resistance, as shown in Fig. 1(b). Then, the total output
resistance of the improved voltage amplifier is given by
(1)
where the negative resistance is selected to be close to
so that the output resistance reaches a very high value, thereby
producing a high midband gain.
The negative resistor is implemented with active devices to
avoid a large voltage drop across the load resistor. This, how-
ever, decreases the 3-dB bandwidth rapidly due to both the in-
creased output resistance and the parasitic capacitances from the
active devices. Therefore, a negative capacitance circuit is added
in parallel with the load capacitance to enlarge the bandwidth.
Then, the total output capacitance is equal to ,
and the bandwidth can be significantly extended by selecting
close to .
Fig. 2 shows a block diagram of the proposed LA, consisting
of an input buffer with 50- input-matching networks, four-
stage gain cells, an offset cancellation feedback network, and
an output buffer. Each gain cell includes the negative resistance
and the negative capacitance circuits.
Following careful considerations of design tradeoffs in LA,
the number of the cascaded stages is set at four. This is because,
for a circuit with identical stages in which each stage is an
ideal voltage amplifier with the gain of and the 3-dB band-
width of , the bandwidth of the overall circuit shrinks rapidly
Fig. 2. Block diagram of the proposed LA.
Fig. 3. Schematic diagrams of (a) the negative resistance circuit and (b) the
negative capacitance circuit.
[9]. Thus, it may provide high gain, but very limited bandwidth
for a large . Nonetheless, the shrinkage of bandwidth becomes
less than 15% even though increases from 5 to 10. Further-
more, the gain per stage should become lower for a fixed overall
gain, which may lead to rapid accumulation of input-referred
noise [2]. Hence, each gain cell of this work is designed to pro-
vide a 3-dB bandwidth of 6 GHz, which corresponds to a total
bandwidth of 2.5 GHz.
Fig. 3(a) depicts a schematic diagram of the negative resis-
tance circuit, where the positive feedback loop formed by
and causes the difference of the output currents to
have opposite polarity with the differential voltage .
Thus, the equivalent output resistance is given by
, and the total output resistance is given by
(2)
Then, an extremely high output resistance can be obtained if
is close to . Yet, the absolute value of the negative
resistance should be kept smaller than to prevent latching.
Fig. 3(b) presents a schematic diagram of the negative capaci-
tance circuit [2], where the positive feedback is set so that the
charge difference is in the opposite direction to that of the
voltage difference . Then, the equivalent impedance of the
negative capacitance circuit is given by
for (3)
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HAN et al.: LOW-POWER GIGABIT CMOS LA USING NEGATIVE IMPEDANCE COMPENSATION AND ITS APPLICATION 3
Fig. 4. Nyquist plot of the admittance of the negative capacitance circuit for the
frequency range up to 2.5 GHz (� � 4 �m, � � ���� �m, � � 40 �A,
� � 35 fF, and � � �� fF).
Fig. 4 shows the Nyquist plot of the admittance of the negative
capacitance circuit. The admittance of the load capacitance
is always located on the imaginary axis because it is a positive
capacitance, whereas the admittance of the negative ca-
pacitance has both a real part and an imaginary part. Thus, the
total output admittance hardly changes with increasing
frequency due to the negative phase response of . This main-
tains the high gain characteristic, while the negative capacitance
enlarges the bandwidth of the LA.
Fig. 5 illustrates the schematic diagram of a gain-cell in the
proposed LA. The transfer function of the gain-cell is given by
(4)
Here, one zero and two poles occur in the transfer function as
(5)
For , the zero may be located at a lower fre-
quency than the dominant pole , and this zero gives rise to
a high-frequency peaking, thus extending the bandwidth. The
poles of the proposed gain cell should always be negative to en-
sure circuit stability, which requires the following inequality:
(6)
HSPICE simulations were conducted for this proposed LA by
utilizing the model parameters of a standard 0.18- m CMOS
technology. Fig. 6 shows the simulated frequency responses,
where 16-dB larger voltage gain is achieved with the negative
resistance and the 3-dB bandwidth is extended to 2.4 GHz
Fig. 5. Schematic diagram of a gain cell in the proposed LA.
Fig. 6. Simulated frequency responses of the proposed LA.
by the negative capacitance. Namely, the total gain–bandwidth
product is enhanced by a factor of 6.8 when compared with a
conventional LA with simple differential pairs.
III. EXPERIMENTAL RESULTS OF THE PROPOSED LA
Test chips of the proposed LA were implemented in the
0.18- m CMOS process. Fig. 7 shows the chip microphoto-
graph, where the chip core occupies an area of 250 100 m ,
and each pad includes an electrostatic discharge protection
diode, with a parasitic capacitance of 0.5 pF. For the mea-
surements, test chips were mounted on an FR-4 PC-board test
fixture.
Fig. 8 demonstrates the measured frequency response of the
proposed LA, where the midband voltage gain of 41 dB and the
bandwidth of 2.4 GHz are achieved, respectively.
Fig. 9 presents the measured output eye-diagrams for
2.5-Gb/s input pseudorandom bit sequence (PRBS)
with voltage levels of 10 mV , 100 mV , 500 mV , and
1 V . For all cases, the single-ended output voltage is mea-
sured as 240 mV .
Fig. 10 depicts the measured bit error rate (BER) for
PRBS with various input signal levels, where the achieved elec-
trical sensitivity is 9.5 mV for BER. Even for a large
1.2-V input overload-level, the measured BER remains below
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4 IEEE TRANSACTIONS ON VERY LARGE SCALE INTEGRATION (VLSI) SYSTEMS
Fig. 7. Chip microphotograph of the proposed LA.
Fig. 8. Measured frequency response of the proposed LA.
. Hence, the dynamic range of the proposed LA is esti-
mated to be greater than 42 dB.
DC measurements reveal that the proposed LA chip dissipates
only 5.2 mW from a single 1.2-V supply. Table I summarizes
the performance in comparison with that of previously reported
CMOS gigabit LAs.
IV. APPLICATION: GIGABIT OPTICAL RECEIVER
The LA proposed in the previous sections was applied to re-
alize a low-power gigabit optical receiver. Fig. 11 illustrates the
architecture of the differential optical receiver which consists of
a dc-balanced transimpedance amplifier (TIA) and a four-stage
LA with negative impedance compensation.
A. DC-Balanced TIA
The front-end TIA is one of the most critical blocks that de-
termine the overall performance of the optical receivers, such
Fig. 9. Measured eye-diagrams of the LA for 2.5-Gb/s � � � input PRBS
with the following input voltage levels. (a) 10 mV . (b) 100 mV . (c) 500
mV . (d) 1.2 V .
Fig. 10. Measured BER of the LA for 2.5-Gb/s � � � PRBS.
as operation speed and sensitivity. Particularly, the degrada-
tion of bandwidth caused by the large input parasitic capaci-
tance from the optical device, i.e., p-i-n photodiode, has led to
the development of several input configurations to alleviate the
problem, such as common-source with input ladder filter [11],
regulated cascode (RGC) [12], [13], and cascode with inductive
peaking [14]. Among these, the RGC input configuration en-
hances the effective input transconductance, thus lowering the
input impedance significantly [12]. Thereby, large input para-
sitic capacitance can be effectively isolated from the TIA band-
width determination.
Although both the common-source with ladder filter and the
cascode with shunt-inductive peaking can relax the effect of the
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HAN et al.: LOW-POWER GIGABIT CMOS LA USING NEGATIVE IMPEDANCE COMPENSATION AND ITS APPLICATION 5
TABLE I
PERFORMANCE COMPARISON WITH THE PREVIOUSLY REPORTED CMOS GIGABIT LIMITING LAS
Fig. 11. Architecture of the differential dc-balanced optical receiver with the proposed LA.
Fig. 12. Simplified schematic diagram of the RGC TIA stage.
Fig. 13. Chip microphotograph of the proposed optical receiver.
large input parasitic capacitance, they require large chip areas
due to the implementation of on-chip passive inductors [14].
In this work, the RGC input configuration (as shown in
Fig. 12) is exploited to boost the effective transconductance of
the input stage, thus providing virtual-ground impedance at the
input node. This certainly relaxes the design tradeoff between
gain and bandwidth [12].
Also, a third-order ladder filter network is employed as an ad-
ditional input broadband circuit between the p-i-n photodiode
and the RGC input stage. The ladder filter is easily realized by
using a bond-wire inductor and an additional on-chip
capacitor , since the photodiode is electrically mod-
eled as a current source with a parasitic capacitance .
Meanwhile, the TIA adopts a cascaded voltage-gain stage and
a dc-balance buffer with a couple of low-pass filters (LPFs). The
cascaded voltage-gain stage targets to achieve wide bandwidth,
so that the total ac-response can guarantee the optimum speed
even at the cost of signal gain.
The dc-balance buffer takes the configuration of a current-
mode-logic differential amplifier, where the size of its main tran-
sistors is judiciously determined by simultaneous consideration
of both the driving capability and the operation speed. The LPF
comprises a couple of passive RC components, of which the
cutoff frequency is designed to be a few hundred kHz in order to
cancel the dc offsets generated in its differential structure. This
provides a more suitable solution than the conventional large
ac-coupling off-chip capacitors.
B. Experimental Results
The proposed optical receiver was fabricated using the same
0.18- m CMOS technology. Fig. 13 shows the chip micropho-
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6 IEEE TRANSACTIONS ON VERY LARGE SCALE INTEGRATION (VLSI) SYSTEMS
TABLE II
PERFORMANCE SUMMARY AND COMPARISON WITH RECENTLY PUBLISHED GIGABIT CMOS OPTICAL RECEIVERS ���� � ���
Fig. 14. Measured optical eye-diagrams of a single-ended output of the optical
receiver for � � PRBS at the following different data rates of (a) 1.25 Gb/s,
(b) 2 Gb/s, (c) 2.5 Gb/s, and (d) 3.125 Gb/s.
tograph, where the whole chip occupies the area of 1.75 0.45
mm . For optical measurements, the chip is integrated with a
GaAs p-i-n photodiode on an FR-4 chip-on-board assembly.
The responsivity of the p-i-n photodiode is 0.6 A/W at a wave-
length of 850 nm and its parasitic capacitance is 1.5 pF under
3.3-V reverse bias voltage.
Fig. 14 demonstrates the optically measured eye-diagrams
for PRBS inputs at different data rates of 1.25, 2, 2.5,
and 3.125 Gb/s. Here, the single-ended output voltage levels are
measured to be 200 mV with a 25- equivalent output load
resistance.
Fig. 15 depicts the measured frequency response of the
optical receiver, achieving a measured transimpedance gain
of 132.6 dB and a 3-dB bandwidth of 2.7 GHz even for
the large 1.5-pF input capacitance. This corresponds to a tran-
simpedance gain-bandwidth product of 11.5 GHz . Also, the
average input noise current spectral density is obtained to be
Fig. 15. Measured frequency response of the optical receiver and its equivalent
input noise current spectral density.
47 pA/sqrt(Hz), which corresponds to the optical sensitivity of
16 dBm for the BER of .
DC measurements reveal that the whole optical receiver chip
dissipates 51 mW from a single 1.8-V supply. Table II summa-
rizes the performance of the proposed optical receiver in com-
parison with recently published gigabit CMOS optical receivers.
V. CONCLUSION
A low-voltage gigabit LA was realized in a 0.18- m CMOS
process, incorporating the negative impedance compensation
technique to obtain low-power, high-gain, wide-bandwidth, and
small chip-area characteristics simultaneously. This LA circuit
was successfully exploited to realize a gigabit optical receiver in
the same 0.18- m CMOS technology. The measured results of
the proposed optical receiver confirm the circuit techniques, and
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HAN et al.: LOW-POWER GIGABIT CMOS LA USING NEGATIVE IMPEDANCE COMPENSATION AND ITS APPLICATION 7
hence provide a potential solution for applications to low-power,
small-size, high-gain, gigabit optical links.
REFERENCES
[1] W.-Z. Chen and D.-S. Lin, “A 90 dB� 10-Gb/s optical receiver analog
front-end in a 0.18-�m CMOS Technology,” IEEE Trans. Very Large
Scale Integr. (VLSI) Syst., vol. 15, no. 3, pp. 358–365, Mar. 2007.
[2] S. Galal and B. Razavi, “10-Gb/s limiting amplifier and laser/modu-
lator driver in 0.18 �m CMOS technology,” IEEE J. Solid-State Cir-
cuits, vol. 38, no. 12, pp. 2138–2146, Dec. 2003.
[3] E. Säckinger and W. C. Fischer, “A 3-GHz 32-dB CMOS limiting am-
plifier for SONET OC-48 receivers,” IEEE J. Solid-State Circuits, vol.
35, no. 12, pp. 1884–1888, Dec. 2000
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