Abstract:
A voltage regulator includes first and second closed-loop amplifiers and a N-type transistor. The first amplifier receives a first reference voltage and a feedback voltage. The second amplifier is responsive to the first amplifier and to the regulated output voltage of the regulator. Both amplifiers are biased by a biasing voltage. The second amplifier has a bandwidth greater than the bandwidth of the first amplifier and a gain smaller that the gain of the first amplifier. The N-type transistor has a first terminal responsive to the output of the second amplifier, a second terminal that receives the input voltage being regulated, and a third terminal that supplies the regulated output voltage. The feedback voltage is generating by dividing the regulated output voltage. An optional fixed or dynamically biased current source biases the first terminal of the N-type transistor. The voltage regulator optionally includes an overshoot correction circuit.

Description:
CROSS-REFERENCES TO RELATED APPLICATIONS 
     The present application claims benefit under 35 USC 119(e) of U.S. provisional Application No. 60/865,628, filed Nov. 13, 2006, entitled “Fast Low Dropout Voltage Regulator Circuit,” the content of which is incorporated herein by reference in its entirety. 
    
    
     BACKGROUND OF THE INVENTION 
     Low Drop-Out (LDO) linear voltage regulator integrated circuits are widely used in electronic systems, particularly in applications which require power supplies with low noise and low ripple. In portable applications, LDO regulators supply power to the analog baseband stages, radio frequency stages and to other noise-sensitive analog circuit blocks. 
     The efficiency and the physical size of the power supply solution are two important aspects in portable applications where the amount of energy stored in the battery is limited and board space is at a premium. The efficiency loss of an LDO regulator has two principal components, namely thermal dissipation, and ground current. 
       FIG. 1  is a block diagram of an LDO regulator  10 , as known in the prior art. LDO regulator  10  includes a pair of closed-loop amplifiers  12  and  14 , and a PMOS pass transistor  16 . Thermal dissipation is determined by the difference between the input and output voltages of the LDO regulator  10 , and the current through PMOS transistor  16  which nearly equals the load current. When the difference between the input and the output voltages is large and high currents are delivered to the load, a large amount of power is dissipated by transistor  16 . Minimizing the input-output voltage differential minimizes the energy so wasted for a given load current. Thus it is advantageous to operate the LDO regulators at a low input-output voltage differential. Minimizing the input-output voltage differential would require lowering of the supply voltage of the internal circuitry in LDO regulator  10  to a level close to the regulated output voltage, which in turn, poses a significant design challenge as lower output voltages are demanded from the output of the LDO regulator  10 . 
     The ground current of an LDO regulator mostly includes bias currents for biasing of internal circuitry and for generating reference voltages and currents. The ground current does not contribute to the load current as it flows from the input supply to ground, through internal circuitry. Although at low load currents, stable LDO regulator operation can be achieved using relatively low bias currents, high load currents usually require high bias currents to ensure stable operation while ensuring good transient response. Conventional LDO regulators, such as that shown in  FIG. 1 , employ a constant biasing scheme with high internal bias currents to provide a stable operation at high load currents. Such a biasing scheme wastes valuable current at light loads and the light load efficiency suffers as a result. Another conventional approach is to keep the bias currents constant at a low to moderate level, but such an approach deteriorates the transient response of the LDO regulator. 
     BRIEF SUMMARY OF THE INVENTION 
     In accordance with one embodiment of the present invention, a voltage regulator circuit includes, in part, first and second closed-loop amplifiers and a N-type transistor. The first amplifier is adapted to receive a first reference voltage and a feedback voltage and is biased by a first biasing voltage. The second amplifier is responsive to the output of the first amplifier and to the regulated output voltage supplied by the regulator circuit. The second amplifier is also biased by the first biasing voltage and has a bandwidth that is greater than the bandwidth of the first amplifier and a gain that is smaller that the gain of the first amplifier. The N-type transistor has a first terminal responsive to the output of the second amplifier, a second terminal that receives the input voltage being regulated, and a third terminal that supplies the regulated output voltage. The feedback voltage is generating by dividing the regulated output voltage. 
     In one embodiment, the N-type transistor is an N-type MOS transistor. In another embodiment, the N-type transistor is a bipolar NPN transistor. In one embodiment, a current source supplies a substantially fixed current to the first terminal of the N-type transistor. In another embodiment, the current supplied to the first terminal of the N-type transistor is proportional to a current flowing through the second terminal of the N-type transistor. In one embodiment, the current source includes a current mirror responsive to the first biasing voltage, and a second N-type transistor that is responsive to the output of the second amplifier and to the current mirror. 
     In one embodiment, the voltage regulator circuit includes a comparator, and an NMOS transistor. The comparator is responsive to the output of the first amplifier and to the regulated output voltage. The NMOS transistor is responsive to the output of the comparator. The NMOS transistor has a source terminal that is coupled to a ground terminal and a drain terminal coupled to a first terminal of a resistor which has a second terminal adapted to receive the regulated output voltage. In one embodiment, an offset voltage is applied between the second amplifier and the comparator. 
     A method of regulating a voltage, in accordance with one embodiment of the present invention includes, in part, applying a first reference voltage and a feedback voltage to a first amplifier, applying an output signal of the first amplifier and a regulated output voltage to a second amplifier, biasing the first and second amplifiers using a first biasing voltage, and applying an output of the second amplifier to a first terminal of an N-type transistor. The N-type transistor has a second terminal receiving an input voltage being regulated, and a third terminal supplying the regulated output voltage. The second amplifier has a bandwidth that is greater than a bandwidth of the first amplifier and a gain that is smaller that a gain of the first amplifier. The feedback voltage is generated from the regulated output voltage. 
     In one embodiment, the N-type transistor is an N-type MOS transistor. In another embodiment, the N-type transistor is a bipolar NPN transistor. In one embodiment, a current source supplies a substantially fixed current to the first terminal of the N-type transistor. In another embodiment, the current supplied to the first terminal of the N-type transistor is proportional to a current flowing through the second terminal of the N-type transistor. In one embodiment, the current source includes a current mirror responsive to the first biasing voltage, and a second N-type transistor that is responsive to the output of the second amplifier and to the current mirror. 
     In one embodiment, the method further includes, in part, comparing an output voltage of the first amplifier to the regulated output voltage, and providing a discharge path from the third terminal of the first N-type transistor to a ground terminal when the output voltage of the first amplifier is detected as being smaller than the regulated output voltage. In accordance with one embodiment, an offset voltage is applied between the second amplifier and the comparator. 
    
    
     
       BRIEF DESCRIPTION OF THE DRAWINGS 
         FIG. 1  is a block diagram of a low drop-out (LDO) voltage regulator, as known in the prior art. 
         FIG. 2  is a block diagram of an LDO voltage regulator, in accordance with one embodiment of the present invention. 
         FIG. 3A  illustrates the short-term transient response of the output voltage of the LDO regulator of  FIG. 2 . 
         FIG. 3B  illustrates the long-term transient response of the output voltage of the LDO regulator of  FIG. 2 . 
         FIG. 4  is a schematic diagram of an exemplary low-gain high-bandwidth amplifier disposed in the LDO voltage regulator of  FIG. 2 , in accordance with one embodiment of the present invention. 
         FIG. 5  is a schematic diagram of an exemplary high-gain low-bandwidth amplifier disposed in the LDO voltage regulator of  FIG. 2 , in accordance with one embodiment of the present invention. 
         FIG. 6  is a block diagram of an LDO voltage regulator, in accordance with another embodiment of the present invention. 
         FIG. 7  is a schematic diagram of an exemplary low-gain high-bandwidth amplifier disposed in the LDO voltage regulator of  FIG. 6 , in accordance with one embodiment of the present invention. 
         FIG. 8A  shows the frequency responses of the closed-loop low-gain high-bandwidth amplifiers of  FIGS. 2 and 6 . 
         FIG. 8B  shows the quiescent ground currents of LDO voltage regulators shown in  FIGS. 2 and 6 . 
         FIG. 9  is a block diagram of an LDO voltage regulator, in accordance with another embodiment of the present invention. 
         FIG. 10  shows the time variations of the output voltages of LDO regulators of  FIGS. 3 ,  6  and  9 , in accordance with one embodiment of the present invention. 
     
    
    
     DETAILED DESCRIPTION OF THE INVENTION 
       FIG. 2  is a block diagram of a low drop-out (LDO) linear integrated circuit  100 , in accordance with one embodiment of the present invention. LDO  100  is shown as including amplifiers  102 ,  104 , N-type pass element  106 , and current source  136 . Amplifiers  102  and  104  form a dual-feedback loop control circuit adapted to regulate output voltage VOUT delivered to output node  122 . The following description is provided with reference to an NMOS transistor  106 . It is understood that any N-type transistor, such as a bipolar NPN transistor, may also be used. 
     Amplifier  102  is a high-gain low-bandwidth amplifier (HGLBA) forming a relatively slower feedback loop (SFL) adapted to control the DC accuracy of regulator  100 . Amplifier  104  is a low-gain, high-bandwidth amplifier (LGHBA) that together with NMOS transistor  106  form a fast and high current unity gain voltage follower. Amplifier  104  forms a fast feedback loop (FFL) adapted to maintain output voltage VOUT within a predefined range in response to a fast load transient. Current source  136  (I CB ) supplies a constant bias current to node  132  (VG) and is used to define the output resistance r O  of amplifier  104 . 
     Input terminal  118  is used to supply biasing voltage VBIAS to LDO regulator  100 . Input voltage VIN regulated by LDO regulator  100  is applied to input terminal  120 . Reference voltage VREF applied to amplifier  102  is received by input terminal  126  but may be internally generated using any one of a number of conventional design techniques. Because in accordance with the present invention biasing voltage VBIAS is separate from input voltage VIN, input voltage VIN may be lowered to a value that is above output voltage to increase efficiency, while keeping VBIAS at a sufficiently high level for biasing the internal circuitry. 
     Components collectively identified using reference numeral  150  are externally supplied to ensure proper operation of LDO regulator  100 . Resistors  114  and  112  divide the output voltage VOUT—delivered to output terminal  122 —to generate a feedback voltage VFB that is supplied to amplifier  102  via input terminal  124 . Accordingly, voltage VOUT is nominally defined by the following expression:
 
 V OUT= V REF*( R 1 +R 2)/ R 1  (1)
 
where R 1  and R 2  are the resistances of resistors  112  and  114 , respectively.
 
     Resistor  110 , having the resistance R L , represents the load seen by LDO regulator  100 . Output capacitor  108 , having the capacitance C OUT , is used to maintain loop stability and to keep output voltage VOUT relatively constant during load transients. Capacitance C OUT  is typically selected to have a relatively large value to keep output voltage VOUT within a predefined range while the dual-feedback loops respond and regain control in response to a load transient. Resistor  130  represents the inherent equivalent series resistance (ESR) of output capacitor  108 . The resistance R ESR  of resistor  130  is defined by the construction and material of capacitor  108 . Inductor  144  represents the inherent equivalent series inductance (ESL) of output capacitor  108 . The inductance of inductor  144  is defined by the construction and material of the capacitor  108 . In voltage regulator applications where fast transient response is important, capacitor  108  is typically a ceramic chip capacitor which is characterized by low ESR and ESL values compared to its tantalum and aluminum electrolytic counterparts. For a typical 1 μF 10V ceramic chip capacitor  108 , representative values for the ESR and ESL are R ESR =10 mΩ, L ESL =1 nH. 
     Referring to  FIGS. 2 and 3A  concurrently, assume the load current I L  changes from a low level I L1  to a higher level I L2  in a time interval Δt that is small compared to the response time T DFFL  of the FFL and that the current through resistor  114  is negligible compared to currents of I L1  or I L2 . Also assume that the voltage VINT applied to the input terminal of amplifier  104  remains relatively constant within time intervals close to T DFFL . These are valid assumptions since the response time T DSFL  of the SFL is much larger than T DFFL . The output load transient event is illustrated in  FIG. 3A . 
     When a large load current transient is applied to the output, it causes on the output voltage (i) a voltage spike induced by the ESL, (ii) an offset voltage induced by the ESR and (iii) a voltage droop caused by the loop response time. The effects of L ESL  and R ESR  can be kept relatively small by proper selection of external components and by following proper layout techniques. As an example, a load current step of 0 to 100 mA in 100 ns would cause a peak output voltage deviation of 1 mV due to 1 nH of ESL. The contribution of ESR to the transient output voltage deviation is also relatively small. As an example, a load current step of 0 to 100 mA would cause a peak output voltage deviation of 1 mV due to 10 mΩ of ESR. The voltage droop is caused by the non-zero loop response time T DFFL . Assuming that ΔI L  is the difference between I L2  and I L1 , the following approximation can be written about the droop rate:
 
 d ( V OUT)/ dt=ΔI   L   /C   OUT   (2)
 
     During the period T DFFL , the load current is supplied by C OUT . At the end of T DFFL , the maximum output voltage deviation from the initial regulation value of VOUT L1  may be written as:
 
Δ V OUT MAX   =ΔI   L   *T   DFFL   /C   OUT   (3)
 
     After the expiration of T DFFL , the FFL brings the output voltage to VOUT L2     —     TR , as shown by the following expression.
 
Δ V OUT TR   =V OUT L1   −V OUT L2     —     TR   ≅ΔV   GS   /A   LGHBA   (4)
 
     In expression (4), A LGHBA  represents the voltage gain of the amplifier  104 , ΔV GS  is the voltage difference between the gate-to-source voltages V GS2  and V GS1  of NMOS  106  at drain current levels of I L2  and I L1  respectively, and ΔVOUT TR  represents the transient load regulation characteristic of the LDO regulator  100 . 
     The following are exemplary numerical values of a few parameters associated with LDO regulator  100  of  FIG. 2 . This example shows that the FFL catches the output voltage at a voltage level 30 mV lower than the no-load output voltage in response to a fast-load transient: 
     I L1 =0 
     I L2 =100 mA 
     A LGHBA =20 
     T DFFL =300 ns 
     C OUT =1 μF 
     V GS     —     L1 =500 mV (at I L1 =0) 
     V GS     —     L2 =900 mV (at I L2 =100 mA) 
     d(VOUT)/dt=ΔIL/C OUT =100 mV/μs 
     ΔVOUT MAX =ΔI L *T DFFL /C OUT =30 mV 
     ΔVOUT TR =ΔV GS /A LGHBA= 20 mV 
     After the initial events described above, amplifier  102  which has a response time of T DSFL  brings the output voltage back to DC regulation as shown in  FIG. 3B . The output voltage is brought back to within ΔVOUT of VOUT L1  after the time period T DSFL  by amplifier  102 . Voltage difference ΔVOUT which characterizes the DC load regulation characteristic of the LDO regulator  100  is defined below:
 
Δ V OUT=Δ V   GS /( A   LGHBA   *A   HGLBA )*( R 1 +R 2)/ R 1  (5)
 
where A HGLBA  is the voltage DC gain of amplifier  102 .
 
     The following are exemplary numerical values of a few parameters associated with LDO regulator  100  of  FIG. 2 : 
     R 1 =R 2 =100 k Ω 
     A LGHBA =20 
     A HGLBA =400 
     V GS     —     L1 =500 mV (at I L1 =0) 
     V GS     —     L2 =900 mV (at I L2 =100 MA) 
     ΔVOUT=0.1 mV 
     As described above, the DC and transient performances of LDO regulator  100  are handled by two separate amplifiers used in a dual-feedback loop arrangement, thus enabling each loop&#39;s performance to be independently optimized. This, in turn, enables LDO regulator  100  to be relatively very fast and highly accurate. 
       FIG. 4  is a transistor schematic diagram of amplifier  104  of  FIG. 2 , according to one embodiment of the invention. As seen from  FIG. 4 , amplifier  104  is shown as including a folded cascode amplification stage buffered by a voltage follower output stage. Bias voltages VB 31  and VB 32  may be generated using any one of a number of conventional design techniques. In one embodiment, bias voltage VB 32  is connected to the output node of the LDO regulator (not shown). PNP transistors  302  and  304  form the input differential pair. Current source  306  sets the tail current of the input differential pair and defines the transconductance of the input stage, as shown below:
 
 g   m302,304   =I   306 /(2 *V   T )  (6)
 
     In expression (6), parameter V T  represents the thermal voltage. Cascode transistors  312  and  314  together with current sources  308  and  310 , transfer the transconductance of the input stage of the cascode to the output stage of the cascode where the current mirror formed by transistors  316  and  318  converts the differential signals to a single-ended signal. The output impedance of the cascode at the drain terminals of transistors  314  and  318  is large compared to the resistance of resistor  320 . Similarly, the input impedance of the NPN transistor  324  is large compared to the resistance of resistor  320 . Resistor  320  is thus used to set the output impedance at the output of the cascode. The voltage gain of the amplifier  102  is defined by the following expression:
 
 A   LGHBA   =g   m302,304   *R   320   (7)
 
     For example, when g m302,304 =200 μA/V, and R 320 =100 k Ω, A LGHBA  is 20. NPN transistor  324 , biased by current source I 322 , is used as an emitter follower to buffer the output of the cascode. PNP transistor  326  level shifts the output signal to a voltage level more suitable for driving the gate terminal of output pass-transistor, and provides further buffering. PNP  326  is biased by current source  136  which supplies a substantially constant bias current I CB . The output resistance of closed-loop amplifier  102  is defined by the small signal output impedance of transistor  326  and may be written as shown below:
 
 r   O   =V   T   /I   CB   (8)
 
     Referring back to  FIG. 2 , output resistance r O  and input capacitance C IN  of the output pass-transistor  106  contribute a pole at f P2 =1/(2*π*r O *C IN ) to the frequency response of LDO regulator  100 . For a stable operation, it is desirable to move this pole further away from the unity-gain bandwidth f 0  of the LDO regulator  100  to avoid the deterioration of the phase margin. Frequency f 0  is defined by the output impedance r OUT     —     LDO  of LDO regulator  100  as seen by terminal  122 , and by output capacitance C OUT . As r OUT     —     LDO  decreases with increasing load current, f 0  also increases. The current level of the constant bias current source I CB  is kept sufficiently high, so that f P2  is always higher than the highest possible value of f 0 . 
       FIG. 5  is a transistor schematic of amplifier  102  of  FIG. 2 , according to one embodiment of the invention. Amplifier  102  is shown as including a folded cascode input amplification stage, and a full-swing conversion stage buffered by a voltage follower output stage. Bias voltages VB 4  may be generated using any one of a number of conventional design techniques. PNP transistors  402  and  404  form the input differential pair. The current source  406  sets the tail current of the input differential pair and defines the transconductance of the input stage, as shown in the expression below:
 
 g   m402,404   =I   406 /(2 *V   T )  (9)
 
     In expression (9), V T  is the thermal voltage. Cascode transistors  412  and  414 , together with current sources  408  and  410 , transfer the transconductance of the input stage of the cascode to the output stage of the cascode. The current mirrors formed by PMOS transistor pairs  416 / 420  and  418 / 422  further transfer the transconductance of the input stage to the current mirror formed by NMOS transistors  426  and  428 ; this current mirror converts the differential signal to a single-ended rail-to-rail signal. The transconductance of the input stage and the output impedance of the differential to single-ended converter at the drains of transistors  422  and  428 , which is the parallel equivalent of their output impedances r OUT422  and r OUT428 , in parallel with the input impedance of emitter follower transistor  424  defines the gain of the amplifier  102 , as shown below:
 
 A   HGLBA   =g   m402,404   *r   OUT422   //r   OUT428   //r   IN424   (10)
 
     Since the output impedances of transistors  422  and  428 , and the input impedance of NPN  424  have relatively high values, the DC gain of amplifier  102  is relatively high. For example, in one embodiment, when g m402,404 =40 μA/V, and r OUT422 //r OUT428 //r IN424 =10 M Ω, A HGLBA  is 400. NPN transistor  424  provides buffering of the high impedance output node of the differential-to-single ended converter stage and is biased by current source  430 . Capacitor  432  and resistor  434  perform a frequency shaping function by providing a pole and zero pair of the loop transfer function. 
       FIG. 6  is a block diagram of an LDO regulator circuit  300 , in accordance with another embodiment of the present invention. LDO regulator  300  is similar to LDO regulator  100  of  FIG. 2 , except that LDO regulator  300  uses a dynamic biasing scheme in place of the constant biasing scheme provided by current source  136  of LDO regulator  100 . NMOS transistor  516  is a replica of output transistor  106  and is selected to have a channel-width to channel-length ratio (W/L) R  that is proportional to the channel-width to channel-length ratio (W/L) P  of output pass-transistor  106 . Transistor  516 &#39;s gate and source terminals are connected respectively with the transistor  106 &#39;s gate and source terminals. 
     As is well known, the drain current of an MOS transistor is nearly independent of the drain-to-source voltage of the transistor when the transistor operates in the saturation region. This principle is used by the replica transistor  516  to generate a current which is proportional to the current carried by transistor  106 . The drain current of transistor  516  is mirrored by the current mirror that includes PNP transistors  512  and  514 . The mirrored current I DB  flows to gate terminal of transistor  516  at node  132  and biases the output stage of amplifier  504 . Assuming the current mirror formed by transistors  512  and  514  has a 1:1 mirroring ratio, the level of current I DB  is defined by the input current I IN  and the ratio of (W/L) R  to (W/L) P , as shown in the following expression:
 
 I   DB   =I   IN *( W/L ) R /( W/L ) P   (11)
 
     The load current I L  flowing through load resistor  110  is the sum of the input and dynamic bias currents, in accordance with the following expression:
 
 I   L   =I   DB   +I   IN   (12)
 
     Often the ratio (W/L) P /(W/L) L  is selected to be very high, e.g., 1000, thus the load current I L  nearly equals the input current I IN . 
       FIG. 7  is a transistor schematic diagram of amplifier  504  of  FIG. 6 , according to one embodiment of the invention. Amplifier  504  is similar to amplifier the  104  of  FIG. 4  except that amplifier  504  has an output stage that is different from output stage  104  of  FIG. 4 . The output stage of amplifier  504  includes NPN transistors  602  and  606 , PNP transistors  604  and  608  and current source  620  supplying current I B . 
     Referring concurrently to  FIGS. 6 , and  7 , the output impedance r O  of amplifier  504  of  FIG. 7  is defined by the parallel equivalent of the output impedances of bipolar transistors  606  and  608 . When the load current I L  is zero, no dynamic biasing current is sourced into the gate node  132 . Neglecting the base currents, the output stage transistors  602 ,  604 ,  606  and  608  have emitter currents that are equal to the current supplied by current source  620 ; this sets the output impedance for transistors  606  and  608  at V T /I B . This output impedance r O , together with the input capacitance C IN  of the output pass-transistor  106  contribute a pole at f P2 =1/(2*π*r O *C IN ) to the frequency response of the LDO regulator  300 . Current I B  is selected such that it sets the output impedance of amplifier  504  to a low enough value so as to guarantee that f P2  is always sufficiently higher than f 0  at zero or very low load currents. At higher load currents, the dynamic biasing circuit, as described above, causes the bias current I DB  to increase, thus increasing the emitter current of PNP  608 , which in turn decreases the output impedance of the amplifier  504  in proportion with the load current. The unity gain frequency f 0  of the LDO regulator  300  moves to higher frequencies with increasing load current, and dynamic biasing circuit keep f P2  higher than f 0  as the load current changes. 
       FIG. 8A  illustrates the relationship between the load current and pole locations for both constant biasing scheme used in  FIG. 2 , and dynamic biasing scheme used in  FIG. 6 .  FIG. 8A  only takes into account the poles associated with amplifiers  104 / 504 , load resistance R L  and output capacitor C OUT . The contribution of amplifier  102  to the overall frequency behavior of the LDO regulators  100  and  300  is not shown in this Figure as it is independent of load current. It is understood that the overall frequency response of LDO regulators  100 / 300  may be obtained by simply adding the pole-zero pair of amplifier  102  to the frequency characteristics shown in  FIG. 8A . 
     Pole P 1  is determined by r OUT     —     LDO  and C OUT  and is a function of the load current I L  since both load resistance and the output impedance of the LDO regulators are tied to the load current. The location of pole P 1  is shown for two different values of load currents I L1  and I L2 . Pole P 2  is contributed by the output impedance r O  of amplifiers  104 / 504  and the input capacitance C IN  of pass-transistor  106 . At current level I L2 , the location of P 2  is the same for both constant and dynamic biasing schemes, shown as point  700 , and is set to be higher than the unity gain frequency f 0     —     IL2  for stability. As the load current decreases to a lower level I L1 , the dynamic biasing scheme moves the pole P 2  to new point  702  while keeping it higher than the new unity gain frequency f 0     —     IL1 . However the pole P 2  associated with the constant biasing scheme is maintained at substantially the same frequency. The new position of pole P 2  for the constant biasing scheme and associated with the smaller load current level I L1  is shown at point  704 . 
       FIG. 8B  shows the ground current I G  associated with LDO regulators  100  and  300 , shown respectively in  FIGS. 2 and 6 . The dynamic biasing scheme of LDO regulator  300  keeps the ground current proportional to the output current, as shown in plot  720 , to improve the efficiency of the LDO regulator at lower output currents. The constant biasing scheme keeps the ground current constant as the load current varies as shown in plot  740 . 
     LDO regulators  100  and  300  are adapted to source current, accordingly a sudden removal of a high load current causes a voltage overshoot at the output of such regulators. The cause of the overshoot is the response time T DG  of the control loop while trying to throttle back the current through the pass-transistor  106 . When the load is suddenly removed, the pass-transistor stays on for the duration of the response time and keeps supplying excessive charge onto the output capacitor. When the loop regains control, there is no pull-down current available at the output and it takes a finite amount of time for the LDO regulator to recover from this overshoot condition. Referring to  FIG. 10 , traces  905  and  910  respectively show the time variations of output voltage VOUT and input voltage VINT for regulators  100  and  300 . The recovery time is shown as T DONC . 
       FIG. 9  shows an LDO regulator  800  with dynamic biasing and overshoot correction circuit, in accordance with another embodiment of the invention. The overshoot correction circuit includes comparator  802 , NMOS pull down transistor  804 , pulldown resistor  806  (having resistance (R OC ) and an optional offset voltage source  808 . Assume that the voltage supplied by offset voltage source  808  is zero. The relatively low gain of amplifier  104  and the positive non-zero gate-to-source voltage of pass-transistor  106  ensure that voltage VINT present at node  128  is higher than output voltage VOUT when LDO regulator  800  is in regulation. When the load current is removed however, the output voltage VOUT overshoots and voltage VINT starts to droop at a rate defined by the bandwidth of amplifier  102  to counter the overshoot. At some point in time VINT goes below VOUT. Comparator  802  is adapted to detect when VINT falls below VOUT, and in response, switches its output state, thereby turning on NMOS transistor  804 . When NMOS transistor  804  is turned on, resistor  806  provides a discharge path to ground for the excess charge stored on output capacitor C OUT , thus bringing the output voltage VOUT back into regulation in a relatively short time interval. 
     Traces  915  and  920  of  FIG. 10  respectively show the time variations of output voltage VOUT and input voltage VINT for regulator  800 . The improved recovery time is shown as T DONC . Parameter T DG  represents the response time of the feedback loop while trying to throttle the pass-transistor  106 &#39;s current back and T DC  represents the delay of the comparator  802  in sensing the overshoot condition from the respective levels of VINT and VOUT. Offset voltage source  808  may be assigned a non-zero voltage to ensure that VINT is always higher than the voltage applied to the positive input terminal of comparator  802 , even in presence of device mismatches, different pass-transistor characteristics and other effects. Comparator  802  may be a conventional comparator. 
     The above embodiments of the present invention are illustrative and not limiting. Various alternatives and equivalents are possible. The invention is not limited by the type of amplifier, current source, transistor, etc. The invention is not limited by the type of integrated circuit in which the present invention may be disposed. Nor is the invention limited to any specific type of process technology, e.g., CMOS, Bipolar, or BICMOS that may be used to manufacture the present invention. Other additions, subtractions or modifications are obvious in view of the present disclosure and are intended to fall within the scope of the appended claims.