Frequency modulator

Abstract: A frequency modulator is formed in a monolithic integrated circuit as a whole. A direct current signal from a center frequency control circuit and an alternating current signal from a voltage controlled amplifier (VCA) which receives a modulation signal and outputs the alternating current signal are applied to a control input of a voltage controlled oscillator (VCO). A center frequency (Fo) of the VCO is determined by the direct current signal from the center frequency control circuit and a frequency deviation amount (Δ f) of the VCO is determined by the alternating current signal from the VCA, and therefore, a frequency-modulated signal of Fo + Δ f can be outputted from the VCO. The direct current signal from the center frequency control circuit is also applied to a control input of the VCA, and therefore, the center frequency of the VCO as well as an amplitude of the alternating current signal, that is, the frequency deviation amount can be controlled by only the direct current signal.

Description: The present invention relates to a frequency modulator. More specifically, the present invention relates to a frequency modulator which is utilized in a video or sound signal recording circuit, and etc. of a VTR, for example, and is constituted by a monolithic integrated circuit (IC). One example of a well-known frequency modulator is shown in Fig. 2. As shown in Fig. 2, a frequency modulator is generally constituted such that a modulation signal is added to a control voltage for a voltage controlled oscillator (VCO). In addition, a frequency-modulated signal (FM signal) can be represented by a center frequency Fo and a frequency deviation amount Δ f in a case where the modulation signal like a sound signal includes no direct current components. Then, assuming that an oscillation frequency of the VCO is F, the following equation (1) is obtainable. F = Kt · V where, V is a control voltage and Kt is a conversion coefficient. If the above described equation (1) is divided into the center frequency Fo and the frequency deviation amount Δ f, since the center frequency Fo and the frequency deviation amount Δ f are corresponding to a direct current control voltage Vo and a modulation signal Δ v, respectively, the equation (1) can be modified as follows: F = Fo + Δ f = Kt (Vo + Δ v) Normally, due to variations of characteristics of an oscillation capacitor and a coil within the VCO and temperature drift thereof, the equation (2) can be modified as follows: F = Fo + Δ f = Kt (Vo′ + Δ v′) = Kt (α Vo + β Δ v) In the equation (3), Vo′ = α Vo and Δ v′ = β Δ v, and therefore, in the frequency modulator as shown in Fig. 2, it is necessary to respectively adjust the direct current control voltage Vo and the modulation signal Δ v so as to correct the conversion coefficient Kt by correction values α and β so that the center frequency Fo and the frequency deviation amount Δ f become target values, respectively. In the frequency modulator of the above described prior art, it is necessary to adjust or control the center frequency Fo and the frequency deviation amount Δ f. By an application of an APC (Automatic Phase Control) by a PLL (Phase Locked Loop), the center frequency Fo can be maintained in a crystal accuracy without any adjustment; however, an adjustment of the frequency deviation amount Δ f is still indispensable to such a frequency modulator, and therefore, there were necessity of a component for adjusting the frequency deviation amount (normally such a component is variable resistor) and an adjustment step thereof. A frequency modulator according to the preamble of claim 1 is disclosed in GB-A-2 196 495. This frequency modulator uses a control voltage to control the voltage controlled oscillator and which is also supplied to a voltage conversion circuit which has a characteristic the reverse of the modulation sensitivity of the voltage controlled oscillator. This is used to operate an electronic volume control so as to keep the modulation sensitivity of the voltage controlled oscillator constant over a wide frequency band. GB-A-2 045 024 discloses a circuit design for frequency and amplitude control of frequency sources. This design comprises an oscillator which includes an amplifier and a variable band pass filter for feeding-back an output of the amplifier to an input thereof, and an output of the variable band pass filter is outputted as a frequency-modulated signal. It is an object of the invention to provide a novel frequency modulator without necessity of an adjustment of a frequency deviation amount (Δf). This object is achieved by a frequency modulator as defined in claim 1; the dependent claims are related to further developments of the invention. In accordance with the present invention, since both the center frequency Fo and the frequency deviation amount Δ f of the VCO can be controlled by only the direct current signal from the center frequency control means, it becomes possible to omit an adjustment for compensating variations of the characteristics of the VCO, temperature drift and the like to set the frequency deviation amount in an optimum condition. The objects and other objects, features, aspects and advantages of the present invention will become more apparent from the following detailed description of the embodiments of the present invention when taken in conjunction with accompanying drawings. Fig. 1 is a block diagram showing one embodiment in accordance with the present invention. Fig. 2 is a block diagram showing one example of a conventional frequency modulator. Fig. 3 is a graph showing a relationship between a voltage and a frequency of a VCO, wherein parameters are variations of characteristics thereof. Fig. 4 is a block diagram showing a major portion of Fig. 1 embodiment. Fig. 4A is a circuit diagram showing an output portion of a low-pass filter. Fig. 5 is a circuit diagram showing a VCA and associated portions as shown in Fig. 4. Fig. 6 is a circuit diagram showing one example of a variable filter capable of being utilized as a variable band-pass filter and a variable all-pass filter as shown in Fig. 4. Fig. 7 is a circuit diagram specifically showing Fig. 6 circuit. Fig. 8A - Fig. 8E are partial circuit diagrams showing an operational principle of Fig. 7 circuit. Fig. 1 is a basic block diagram showing one embodiment in accordance with the present invention, wherein an adjustment of a center frequency Fo is performed by a center frequency control circuit (Fo control circuit) 1 and an adjustment of a frequency deviation amount Δ f is performed by a voltage controlled amplifier (VCA) 2 which is controlled by an output of Fo control circuit 1. In a case where the output Vo′ of the Fo control circuit 1 is equal to α Vo where the direct current control voltage Vo is corrected by a correction value α as done in the prior art, assuming that the conversion rate of the VCA 2 is m, a correction value β for the VCA 2 is represented by the following equation (4). β = m α Vo On the other hand, dividing the equation (3), the following equations (5) and (6) can be obtained. Fo = Kt · α Vo Δ f = Kt · β Δ v Since the center frequency Fo is set to be coincident with a constant target value and the conversion coefficient Kt is also a constant value, the following equation (7) is obtainable in accordance with the equation (5). α Vo = Fo/Kt Therefore, α Vo also becomes constant. If the equations (7) and (4) are substituted for the equation (6), the following equation (8) is obtainable. Δ f = Kt · β · Δ v = Kt · m α Vo · Δ v = Kt · m · (Fo/Kt) Δ v = m · Fo · Δ v As clearly understood from the equation (8), the frequency deviation amount Δ f is not dependent on the conversion coefficient Kt and the same is determined by the conversion rate m of the VCA 2 and the center frequency Fo. Therefore, if the conversion rate m is set to be coincident with a target value, regardless of variations of characteristics of components such as a capacitor or the like of the VCO 3 which receives an added output of the output of the Fo control circuit 1 and the output of the VCA 2, and a temperature drift thereof, the frequency deviation amount Δ f is primarily determined with respect to a given center frequency Fo, and therefore, it becomes unnecessary to adjust the frequency deviation amount Δ f. Fig. 3 is a graph showing a principle why the adjustment of the aforementioned Δ f becomes unnecessary. In Fig. 3, a voltage V and a frequency F are respectively indicated on an abscissa and an ordinate, and slants of linear lines A and B respectively indicate the conversion coefficients Kt, which show a difference due to a temperature drift. In any characteristics of the linear lines A and B, a center frequencies Fo and frequency deviation amounts Δ f as targeted are the same with each other, respectively, and therefore, in a case of the linear line A, the direct current control voltage and the modulation signal become V OA and Δ v A , respectively, and in a case of the linear line B, the direct current control signal and the modulation signal become V OB and Δ v B , respectively. As clearly understood from Fig. 3, the direct current control voltage has a predetermined relationship with the modulation signal, and therefore, even if there are variations of the characteristics of the conversion coefficient Kt due to a temperature drift, when the modulation signal is controlled by the direct current control voltage, a predetermined frequency deviation amount Δ f can be maintained. Fig. 4 is a block diagram showing Fig. 1 block diagram in detail. In Fig. 4, the VCO 3 is constituted by current controlled variable band-pass filter (hereinafter, simply called as "variable BPF") 4 and a closed loop having the same phase and a fixed gain more than 1 through an amplifier 5. In addition, the Fo control circuit 1 includes a variable all-pass filter (hereinafter, simply called as "variable APF") 6 which receives a clock signal CK having a fixed frequency, a phase comparator 7 which performs a phase comparison of an input and an output of the variable APF 6, and a low-pass filter (LPF) 8 which receives an output of the phase comparator 7 and controls the variable APF 6 by an output thereof. As described above, if the variable APF 6 is controlled by the output of the LPF 8, that is, an error signal which is the output of the phase comparator 7, a resonant point of the variable APF 6 can be in proportion to a frequency of the clock signal CK. In addition, the phase comparator 7 outputs the error signal of zero when a phase difference between the input and the output of the variable APF 6 is zero. The clock signal CK may be generated by a crystal oscillator (not shown). With reference to Fig. 4A, the LPF 8 which receives the output of the phase comparator 7 includes a resistor R and a capacitor C, and an output of the LPF 8 is applied to a base of a transistor Q91 constituting a converting circuit 9. The converting circuit 9 is a circuit for converting the output voltage of the LPF 8 into a current which is in proportion thereto. An emitter resistor is connected to an emitter of the transistor Q91 and a collector thereof is connected to the voltage source +Vcc through a transistor Q92. The transistor Q92 forms a current mirror circuit along with transistors Q93 and Q94. Therefore, the output voltage of the LPF 8 is converted into a control current Io by the converting circuit 9. More specifically, when the transistor Q91 is turned-on by the output voltage of the LPF 8, an emitter current determined by the emitter resistor flows in the transistor Q91 and the emitter current is in proportion to the output voltage of the LPF 8. Then, in a transistor circuit, generally, a emitter current and a collector current is substantially equal to each other, and therefore, a current being in proportion to the output voltage of the LPF 8 flows in the collector of the transistor Q91, that is, the transistor Q92. Since the transistors Q93 and Q94 constitute the current mirror circuit along with the transistor Q92, the same current as that of the transistor Q92 flows in each of the transistors Q93 and Q94. Each of output currents of the transistors Q93 and Q94 becomes the control current Io, which is applied to the variable BPF 4 and the variable APF 6 respectively constituting the VCO 3 and VCA 2 as shown in Fig. 4. The variable APF 6 and the variable BPF 4 shown in Fig. 4 are formed in a single monolithic IC with the same circuit configuration, and more specifically, the same are constituted by utilizing a secondary variable filter which will be described later. Then, with reference to Fig. 6, a secondary variable filter 20 which can operate as the variable BPF and the variable APF utilized in this embodiment shown will be described. Fig. 6 is a circuit diagram showing a principle of the variable filter. In Fig. 6, transistors T5 and T6 constitute a differential pair, and emitters thereof are commonly connected to a constant current source circuit 11. The transistor T5 is supplied with the voltage +Vcc at a collector thereof, and a collector of the transistor T6 is connected to a constant current source circuit 12 and a base of a transistor T7 and to a terminal 15 through a capacitor C1. In addition, a current amount of the constant current source circuit 11 is set twice (2I1) a current amount I1 of the constant current source circuit 12. Transistors T9 and T10 also constitute a differential pair, and emitters thereof are commonly connected to a constant current source circuit 13. The transistor T10 is supplied with the voltage +Vcc at a collector thereof, and a collector of the transistor T9 is connected to a constant current source circuit 14 and a base of a transistor T8 and to a terminal 18 through a capacitor C2. In addition, a base of the transistor T10 is connected to a terminal 19. Furthermore, a current amount of the constant current source circuit 13 is set twice (2I2) a current amount I2 of the constant current circuit 14. The transistor T7 is paired with the transistor T8 and the voltage +Vcc is applied to respective collectors thereof. In addition, an emitter of the transistor T7 is connected to bases of the transistors T6 and T9 and a terminal 16, and an emitter of the transistor T8 is connected to a base of the transistor T5 and a terminal 17. In addition, V1, V2, V3, V4 and V5 respectively correspond to voltage values of signals at the terminals 15, 16, 17, 18 and 19. As to the differential pairs respectively constituted by the transistors T5 and T6 and the transistors T9 and T10 of the variable filter 20, each having the above described configuration, the following equations (9) and (10) are established, respectively. (V3 - V2)/2re1 = (V2 - V1)/ 1 j ω C1 (V5 - V2)/2re2 = (V3 - V4)/ 1 j ω C2 The principle why the equations (9) and (10) can be obtained will be described with reference to Fig. 8A - Fig. 8E. First, noting a differential pair composed of transistors T5 and T6 as shown in Fig. 8A, in which a load resistor RL is inserted in place of the constant current source circuit 12, in accordance with characteristics of the differential pair, a collector voltage V0 of the transistor T6 is represented by the following equation (1); V0 = gm · RL · (V3 - V2) where gm is a mutual conductance. Assuming that a charge of an electron is q (1.602 x 10⁻¹⁹ C), Boltzmann's constant is K (1.38 x 10⁻²³ J/K), and an absolute temperature is T, a relationship represented by the following equation (12) is established. gm = q · (2I1) 4KT = qI1 2KT In addition, by using the differential resistor rel = KT/qI1 = 1/2gm, the above equation (11) can be modified as follows: V0 = 1 2re1 · RL · (V3 - V2) Next, as shown in Fig. 8B, if the load resistor RL is replaced with a constant current source circuit 12 having a current amount of I1 and a capacitor C1 is connected between a collector of the transistor T6 and the ground, since an impedance of the constant current source circuit 12 can be regarded as infinity and an impedance 1/jω C1 is corresponding to the load resister RL, when the equation (13) is applied to Fig. 8B, the following equation (14) can be obtained. V0 = 1 2re1 · 1 j ω C1 · (V3 - V2) Now, as shown in Fig. 8C, if an alternating current voltage source having an output voltage of V1 is further connected between the capacitor C1 and the ground, assuming that a collector voltage of the transistor T6 is V0′, the following equation (15) is obtainable in accordance with the equation (14). V0′ = 1 2re1 · 1 j ω C1 · (V3 -V2) + V1 Next, as shown in Fig. 8D, when an emitter follower is constituted by a transistor T7, assuming that an emitter voltage of the transistor T7 is V0″, since the equation V0′ = V0″ can be established in the emitter follower, the following equation (16) can be obtained in accordance with the equation (15). V0″ = 1 2re1 · 1 j ω C1 · (V3 - V2) + V1 If a portion corresponding to Fig. 8D circuit is derived from Fig. 6, the portion can be illustrated as shown in Fig. 8E, and when the both are compared with each other, the equation V0″ = V2 can be established, and therefore, the following equation (17) can be obtained in accordance with the equation (16). V2 = 1 2re1 · 1 j ω C1 · (V3 - V2) + V1 If the equation (17) is modified, the above described equation (9) is obtained. As similar to the above, in connection to the differential pair constituted by the transistors T9 and T10, the above described equation (10) is obtainable in accordance with the same evaluating method. However, the differential resistor of the differential pair by the transistors T9 and T10 is re2. In the equations (9) and (10), when V3 is eliminated by jω = S, the following equation (18) is obtainable. S²·4re1re2·C1C2·V1 + S·2re2C2·V4 + V5 = (S²·4re1re2·C1C2 + S·2re2C2 + 1)V2 In the equation (18), by applying respective conditions as described later to respective values of V1, V2, V3, V4 and V5, it is possible to vary a characteristic of the variable filter as shown in Fig. 6. (Condition 1) V1 = V5 = 0, V4 = Vin and V2 = Vout In this case, the above described equation (18) is modified as follows: S·2re2C2·Vin = (S²·4re1re2·C1C2 + S·2re2C2 + 1)·Vout Vout/Vin = S·2re2C2/(S²4re1re2·C1C2 + S·2re2C2 + 1) Since the following equation (24) is obtained, the following equation (19) is obtainable. ω o = (1/4re1re2·C1C2) 1/2 = q 2KT (I1I2/C1C2) 1/2 Assuming that the Q is given as follows: Q = (re1C1/re2c2) 1/2 = (I2C1/I1C2) 1/2 Vout/Vin = S· ω o Q /(S² + ω o Q · S + ω o²) The equation (19) indicates a transfer function of a band-pass filter. Therefore, when the above described condition 1 is satisfied, that is, when the terminals 15 and 19 are connected to the ground in an alternating current and the terminals 18 and 16 are used as an input terminal and an output terminal of the variable filter 20, the variable filter 20 operates as a variable BPF. In the equation (19), ω o is an oscillation angle frequency of the BPF, which is variable by changing the current amounts 2I1 and 2I2 of the constant current source circuits 11 and 13. In addition, Q indicates a sharpness of the filter, which is also variable by changing the current amounts 2I1 and 1I2. In other words, by controlling the current amounts I1 and I2, it is possible to vary a characteristic of the variable BPF. (Condition 2) V1 = V5 = Vin, V4 = -Vin, and V2 = Vout In this case, in accordance with the above described equation (18), the following equation (20) is obtainable. Vout/Vin = (S² - ω o Q ·S + ω o²)/(S² + ω o Q ·S + ω o²) The equation (20) indicates a transfer function of an all-pass filter. Therefore, when the above described condition 2 is satisfied, that is, when the terminals 15 and 19 are commonly used as an input terminal and a signal having a reverse polarity to an input signal is inputted to the terminal 18 and the terminal 16 is used as an output terminal, the variable filter 20 shown in Fig. 6 operates as a variable APF, and a characteristic thereof is depend on the current amounts I1 and I2. (Condition 3) V1 = V5 = Vin, V4 = 0 and V2 = Vout In this case, in accordance with the above described equation (18), the following equation (21) is obtainable. Vout/Vin = (S² + ω o²)/(S² + ω o Q ·S + ω o²) The equation (21) indicates a transfer function of a band-elimination filter (BEF). Therefore, when the above described condition 3 is satisfied, that is, when the terminals 15 and 19 are commonly used as an input terminal and the terminal 18 is connected to the ground in alternating current and the terminal 16 is used as an output terminal, the variable filter shown in Fig. 6 operates as a variable BEF, and a characteristic thereof is dependent on the current amounts I1 and I2. (Condition 4) V1 = Vin, V4 = V5 = 0 and V2 = Vout In this case, in accordance with the above described equation (18), the following equation (22) is obtainable. Vout/Vin = ω o Q ·S² /(S² + ω o Q ·S + ω o²) The equation (22) indicates a transfer function of a secondary high-pass filter (HPF). Therefore, when the above described condition 4 is satisfied, that is, when the terminal 15 is used as an input terminal and the terminals 18 and 19 are connected to the ground in alternating current and the terminal 16 is used as an output terminal, the variable filter 20 operates as a variable HPF, and a characteristic thereof is dependent on the current amounts I1 and I2. (Condition 5) V1 = V4 = 0, V5 = Vin and V2 = Vout In this case, in accordance with the above described equation (18), the following equation (23) is obtainable. Vout/Vin = ω o²/(S² + ω o Q ·S + ω o²) The equation (23) indicates a transfer function of a secondary low-pass filter (LPF). Therefore, when the above described condition 5 is satisfied, that is, when the terminal 19 is used as an input terminal and the terminals 15 and 18 are connected to the ground in alternating current and the terminal 16 is used as an output terminal, the variable filter 20 operates as an LPF, and a characteristic thereof is dependent on the current amounts I1 and I2. As described above, by applying the respective conditions without changing the circuit configuration, it is possible to operate the variable filter 20 as shown in Fig. 6 as a variable BPF or variable APF, and it is possible to control the characteristic of the filter by the current amounts I1 and I2. Fig. 7 is a circuit diagram showing a specific variable filter in which the current amounts I1 and I2 can be controlled by applying the principle of the variable filter 20 as shown in Fig. 6, wherein the constant current source circuits are constituted by current mirror circuits composed of transistors and resistors so that the current amounts of the constant current source circuits can be controlled in response to a current value of the control signal Io. Then, the circuit as shown in Fig. 7 will be described briefly. In addition, by applying the same reference symbols to the same portions as that in Fig. 6, a duplicate description will be omitted. The constant current source circuit 11 is constituted by transistors T11 and T12 connected in parallel with each other and a resistor 22 having a resistance value of r, and a control current signal Io which is supplied to a terminal 50 is injected to a collector of a transistor T21 which constitutes a current mirror circuit along with the transistors T11 and T12. In addition, the constant current source circuit 13 is also constituted by transistors T13 and T14 connected in parallel with each other and a resistor 23 having a resistance value of r, and a current having the same current amount as the control current signal which is injected to the collector of the transistor T21 flows into the transistors T13 and T14 which constitute a current mirror circuit along with the transistor T21. The constant current source circuit 12 is replaced with a current mirror circuit constituted by transistors T15 and T16 and a constant current source circuit constituted by a transistor T17 coupled to the transistor T16 and a resistor 24 having a resistance value of 2r, and a current amount thereof is controlled by the control current signal which is injected into a collector of the transistor T21. Similarly, the constant current source circuit 14 is replaced with a current mirror circuit constituted by transistors T18 and T19 and a constant current source circuit constituted by a transistor T20 and a resistor 25 having a resistance value of 2r, and a current amount thereof is controlled by the control current signal which is injected to a collector of the transistor T21. On the assumption that a current amount flowing through the resistor 24 is i when the control current signal has an arbitral current value Io, the current amounts flowing through the constant current source circuits 11, 12, 13 and 14, that is, the current amounts flowing through the resistors 22, 24, 23 and 25 are as follows: a current of 2i flows through the resistors 22 and 23, a current of i flows through the resistor 25, and a collector current of each of the transistors T15 and T18 also becomes i by an operation of the current mirror circuit. Therefore, I1 = I2 = i and, when a resistance value of a resistor R26 is 2r, Io = i = I1 = I2. In addition, resistors R1, R2, R3 and R4 are inserted to set a gain. Furthermore, the resistors R2 and R4 are connected to the ground in alternating current, and it is necessary to apply thereto a direct current bias such as Vcc/2 when such a circuit is to be operated actually. In Fig. 7 circuit, assuming K = R2/(R1 + R2) and L = R4/(R3 + R4), if operations similar to the above described equation (9) and (10) are performed, the following equations (9′) and (10′) are established and, when V3 is eliminated, the following equation (18′) is obtainable. LV3 - KV2 2re1 · 1 j ω C1 = V2 - V1 V5 - V2 2re2 · 1 j ω C2 = V3 - V4 S²·4re1re2·C1C2·V1 + S·2re2C2·L·V4 + L·V5 = (S²·4re1re2·C1C2 + S·2re2C2·K + L)V2 By applying the condition 1 to the equation (18′), the following equations is obtained. Vout/Vin = S· ω 0′ Q′ / (S² + ω 0′ Q′ · S + ω 0′²) wherein, ω 0′ = (L/4re1re2·C1C2) 1/2 Q′ = 1 K (LI2C1/I1C2) 1/2 = 1 K (LC1/C2) 1/2 The above equation indicates a transfer function of the BPF. In addition, when the condition 2 is applied to the above described equation (18′), the following equation is obtained. Vout/Vin = (S² - ω o′ Q′ · S + ω o′²)/(S² + ω o′ Q′ · S + ω o′²) The above equation indicates a transfer function of the APF. Next, a description will be made on a voltage control oscillator (VCO) which is constituted by the variable filter 20 having the above described circuit configuration. In order to apply the condition 1 to the variable filter 20, the terminals 15 and 19 are connected to the ground in alternating current, the terminal 18 is used as the input terminal which is supplied with the output of the amplifier 5, the terminal 16 is used as the output terminal which is coupled to the input of the amplifier 5, and an added current Io + Δ i which is obtained by adding the current Io from the LPF 8 which is supplied to the terminal 50 as the control signal and a current Δ i from the VCA 2 (described later in detail), and then, the variable filter 20 operates as the variable BPF 4. BY inserting the amplifier 5 between an input and an output of the BPF, the VCO 3 is constituted, and a frequency modulated signal F = Fo + Δ f can be outputted. In addition, the above described variable filter 20 receives as the control signal therefor not the voltage but the current, and therefore, it is preferably that such a circuit is represented as a current controlled oscillator in practical; however, in this text, the circuit is represented as a voltage controlled oscillator (VCO) according to common usage because signals are generally sent and received between electronics equipments in a form of a voltage. In addition, by applying the condition 2 to the variable filter 20, the terminals 15 and 16 are used as an input terminal which is supplied with a clock signal CK, the terminal 18 is supplied with a signal having a reverse polarity to the clock signal CK, the terminal 16 is used as the output terminal which is coupled to an input end of the phase comparator 7, and the terminal 50 is supplied with the current Io as the control signal, the variable filter 20 operates as the variable APF 6. In accordance with the above described equation (24), in a case where the filter shown in Fig. 6 functions as the variable BPF, the oscillation angle frequency ω o is represented as follows: ω o = q 2KT (I1I2/C1C2) 1/2 when a circuit is designed to obtain conditions that C1 = C2 = C and that I1 = I2 = I, the oscillation frequency F of the variable BPF is given by the following equation (25). F = 2 π ω o = 2 π ·(q/2KT)·(I/C) = (π q/KT)·(I/C) Therefore, the oscillation frequency F is determined by the control current I, a capacitance value C of the capacitor and the absolute temperature T. Dividing the equation (25) into the center frequency Fo and the frequency deviation amount Δ f, the following equation (26) is obtainable. F = Fo + Δ f = 2 π ·(q/2KT)·(Io + Δ i)/C = (π q/KT)·(Io/C) + (π q/KT)·( Δ i/C) The control current Io is supplied from the Fo control circuit 1 which is an automatic correction circuit using the variable APF 6. Since the variable APF 6 and the variable BPF 4 are formed in the same monolithic IC with the same circuit configuration as described above, a resonant point of the variable BPF 4 is in proportion to the clock signal CK as similar to that of the variable APF 6, and therefore, in a state where a frequency of the clock signal CK from the external is maintained at a constant value, the center frequency Fo also becomes constant value. In addition, in accordance with the above described equation (26), since the equation Fo = ( π q/KT)·(Io/C) is established, the following equation (38) is obtainable. Io = FoKTC/π q Next, a specific circuit configuration of the VCA 2 is shown in Fig. 5. In addition, since all the elements of the block diagram of Fig. 2 are formed in the same monolithic IC, the VCA 2 is also formed in the same monolithic IC as similar to the variable BPF 4 and the variable APF 6. The VCA 2 is mainly composed of a differential pair 40 which is constituted by a pair of NPN transistors Q1 and Q2 and arranged at outside, and a differential pair 41 which is coupled to the differential pair 40 in series and constituted by a pair of transistors Q3 and Q4 and arranged at inside. Collectors of the transistors Q1 and Q2 are respectively coupled to bases of the transistors Q3 and Q4 and to emitters of NPN transistors Q5 and Q6 which are connected to each other in a diode fashion. In addition, a transistor Q9 is inserted between the collectors of the transistors Q5 and Q6 and a line for the voltage +Vcc. On the other hand, emitters of the transistors Q1 and Q2 are coupled to both ends of a resistor Re and to collectors of transistors Q10 and Q11. The transistors Q10 and Q11 are transistors which constitute a constant current source circuit along with respective resistors 30 and 31, and respective bases thereof are coupled to a base of a transistor Q12 constituting a bias circuit 42 (described later) to constitute a current mirror circuit. Bases of the transistors Q1 and Q2 are coupled through resistors 32 and 33 to a line 36 which is biased at a predetermined voltage by a direct current voltage source 35, and especially, the base of the transistor Q1 is further connected to an input terminal 34 for inputting the modulation signal Δ v through a capacitor 37 for cutting-off a direct current component. Emitters of the transistors Q3 and Q4 are coupled to a collector of a transistor Q13 which constitutes a current mirror circuit along with a transistor Q14. In addition, a collector of the transistor Q14 is coupled to an input terminal 38 which is supplied with an output current Io of the Fo control circuit 1. On the other hand, collectors of the transistors Q3 and Q4 are coupled to collectors and bases of transistors Q15 and Q17 constitute current mirror circuits along with transistors Q16 and Q18, respectively, and a collector of the transistor Q16 is coupled to a collector and a base of a transistor Q19 which constitutes a current mirror circuit along with a transistor Q20, and a collector of the transistor Q18 is coupled to a collector of the transistor Q20 and an output terminal 39. The bias circuit 42 includes a PNP transistor Q7 having a base supplied with a fixed reference voltage Vr, an emitter connected to a voltage source line through a resistor 43, and a collector connected to the ground. The emitter of the transistor Q7 is coupled to a base of an NPN transistor Q8 having a collector coupled to a collector and a base of a transistor Q21. Bases of the transistor Q21 and a transistor Q22 are coupled to each other to constitute a current mirror circuit. A collector of the transistor Q22 is coupled to a collector and a base of a transistor Q12. In addition, a resistor R A is inserted between an emitter of the transistor Q8 and the ground, and a base of the transistor Q12 is coupled to the bases of the transistors Q10 and Q11 as described above to constitute a current mirror circuit. Next, a description will be made on an operation of the VCA 2 having the above described circuit configuration. First, in the bias circuit 42, since the transistor Q7 is a PNP type and the transistor Q8 is an NPN type, and both the transistors are formed in the same monolithic IC, if a base-emitter voltage of the transistor Q7 is V BE , a base-emitter voltage of the transistor Q8 becomes - V BE which has the same absolute value and a reverse polarity as that of V BE . Therefore, since both the base-emitter voltages are canceled with each other, and the emitter voltage of the transistor Q8 becomes the reference voltage Vr and a current Io′ flowing through the resistor R A is represented by the following equation (35). Io′ = Vr/R A The current Io′ is equal to a collector current of the transistor Q8, according to a current mirror effect of the transistors Q21 and Q22, a collector current of the transistor Q12 is also equal to the current Io′, and further, according to a current mirror effect of the transistors Q10, Q11 and Q12, a collector current of each of the transistors Q10 and Q11 also becomes Io′. On the other hand, when the output current Io from the Fo control circuit 1 is supplied to the input terminal 38, according to a current mirror effect of the transistors Q14 and Q13, a collector current of the transistor Q13 also become Io. Next, a description will be made on a gain of each differential pair when the differential pairs 40 and 41 operate in this state. A gain of a differential pair is generally given by dividing a collector resistor (load) of transistors constituting the differential pair by an emitter resistor (load), that is, the collector resistor/the emitter resistor. Then, noting the differential pair 40, an input voltage is the modulation signal Δ v and an output voltage is collector voltages of the transistors Q1 and Q2 (respective collector voltages have reverse polarities to each other). Assuming that a differential resistor of the differential pair 40 is re3, an emitter load becomes 2re3 + R E . In addition, since each of the emitter currents of the transistors Q5 and Q6 is equal to Io′, a differential resistor of the transistors Q5 and Q6 is equal to re3, and since the differential resistor of the transistors Q5 and Q6 serves as the collector load of the differential pair 40, a voltage gain A1 of the differential pair 40 with respect to the input voltage and output voltage is given by the following equations (27). A1 = re3/(2re3 + R E ) where, re3 = (1/Io′)·(KT/q) Then, the deferential resistor re3 is extremely smaller than the resistor R E , that is, a relationship of re3 « R E is obtained, and therefore, the above described equation (27) is modified as follows: A1 = re3/R E Next, noting the differential pair 41, an input voltage is equal to each of the collector voltages of the transistors Q1 and Q2 which is the output voltage of the differential pair 40, and an output voltage is a voltage generated between the output terminal 39 and the line 36, and thus, if a load resistor Rf is inserted between the output terminal 39 and the line 36 as shown by a dotted line in Fig. 5, the output voltage becomes equal to a voltage generated between both ends of the load resistor Rf. Assuming that a differential resistor of the differential pair 41 is re4, an emitter load becomes 2re4. On the other hand, the transistors Q3 and Q4 function as a push-pull circuit, and therefore, a collector current of the transistor Q3 becomes a collector current of the transistor Q19 according to a current mirror effect of the transistors Q15 and Q16, and further, according to a current mirror effect of the transistors Q19 and Q20, the collector current of the transistor Q3 becomes a collector current of the transistor Q20. In addition, a collector current of the transistor Q4 becomes a collector current of the transistor Q18 according to a current mirror effect of the transistors Q17 and Q18. When the collector current of the transistor Q4 increases, the collector current of the transistor Q3 decreases, and the collector current of the transistor Q18 becomes larger than the collector current of the transistor Q20, and thus a current amount due to an increase of the collector current of the transistor Q20 is outputted as an output current Δ i. In reverse, when the collector current of the transistor Q3 increases, the collector current of the transistor Q4 decreases, the collector current of the transistor Q18 becomes smaller than the collector current of the transistor Q20, and thus, a current amount for compensating a lack due to a decrease of the collector current of the transistor Q20 flows into the terminal 39 inversely. Therefore, the load resistor Rf contributes to the collector load of the transistors Q3 and Q4, and therefore, the collector load of the differential pair 41 becomes 2Rf. Then, a voltage gain A2 of the differential pair 41 is given by the following equation (29). A2 = 2Rf/2re4 = Rf/re4 where, re4 = (1/Io)·(KT/q) Since the output voltage is Rf·Δ i, in accordance with the equation (29), a gain A3 of voltage-current (V-I) conversion in the differential pair 41 is given by the following equation (31). A3 = A2/Rf = (Rf/re4)/Rf = 1/re4 Then, the VCA 2 of this embodiment shown is actually a V-I converter of a current controlled gain type, and therefore, a gain A of the V-I converter is a product of a voltage gain A1 by the V-I gain A3, and therefore, represented by the following equation (32). A = Δ i/Δ v = A1·A3 = (re3/R E )·(1/re4) Furthermore, if the equations (33) and (30) are substituted for the equation (32), the following equation (34) is obtainable. A = (1/Io′)·(KT/q)/ { R E ·(1/Io)·(KT/q)} = Io/(Io′·R E ) In addition, if the equation (35) is substituted for the equation (34), the following equation (36) is obtainable. Δ i/Δ v = Io/ { (Vr/R A )·R E } Δ i = Δ v·Io/ { Vr·(R E /R A )} Since a relative accuracy of resistors is very good in a monolithic IC, R E /R A becomes a constant value, and thus, since the reference voltage Vr is also a constant voltage, it is possible to consider that the equation 1/{Vr·(R E /R A )} = m (m is a constant value). Therefore, the above described equation (36) is represented by the following equation (37). Δ i = m·Io· Δ v In accordance with the equation (26), the following equation (39) is obtainable, and therefore, if the equations (38) and (37) are substituted for the equation (39), the following equation (40) is obtainable. Δ f = (π q/KT)(Δ i/C) Δ f = (π q/KT)·(m·Io·Δ v/C) = m·Fo·Δ v The equation (40) is the same as the equation (8), and therefore, by constructing the VCA 2 as shown in Fig. 5 and setting m to be coincident with a target value, a frequency modulated signal having a frequency deviation amount Δ f which is not dependent upon variations of capacitors of VCO and a temperature drift thereof can be outputted. In other words, in a case where a temperature dependency exists in an oscillation frequency as represented by the above described equation (25), as represented by the equation (26), the center frequency Fo as well as a frequency deviation amount Δ f are dependent on a temperature; however, in accordance with this embodiment shown, it becomes unnecessary to apply an adjustment taking into consideration of such a temperature dependency to the input of the VCO. In addition, a combination of the VCO 3 and VCA 2 of Fig. 4 can be regarded as a sort of a VCO, and therefore, if such a VCO is used as a PLL (Phase Locked Loop) circuit, an FM demodulator in which a demodulation sensitivity is determined by the above described equation (8) is obtained. Especially, in a sound signal recording circuit of an 8mm VTR or the like, an FM modulator becomes necessary in recording and an FM demodulator becomes necessary in playing, and therefore, by applying the above described embodiment to such an FM demodulator, it is possible to obtain an FM modulation and demodulation system of adjustment free.

Claims: A frequency modulator comprising: an oscillator (3) the oscillation frequency of which is variable in response to a control signal inputted to a first control input thereof; first means (1) for generating a direct current signal (I o ) which determines a center frequency of said oscillator; second means (2) for generating an alternating current signal which has the amplitude in proportion to a modulation signal and determines a frequency deviation amount of said oscillator, said second means having a second control input; first voltage applying means (300: Fig. 4) for applying said direct current signal and said alternating current signal to said first input of said oscillator; and second voltage applying means (1) for applying said direct current signal to said second control input of said second means so that said amplitude of said alternating current signal can be controlled by said direct current signal, characterized in that said first means includes a variable all-pass filter (6) which receives a clock signal, a phase comparator (7) which compares the phase of an output of said variable all-pass filter with the phase of said clock signal, and a low-pass filter (8) which receives an output of said phase comparator, the output signal of said low-pass filter being applied to said first control input of said oscillator and said second control input of said second means. A frequency modulator in accordance with claim 1, wherein said first means (1) includes a variable resistor the output voltage of which is applied to said first input of said oscillator (3) and said second control input of said second means (2). A frequency modulator in accordance with claim 1, wherein said first means (1) includes a phase-locked loop constituted by including said oscillator (3), an output signal of said phase-locked loop is applied to said first control input of said oscillator (3) and said second control input of said second means (2). A frequency modulator in accordance with claim 1, wherein said oscillator (3) includes an amplifier (5) and a variable band-pass filter (4) for feeding-back an output of said amplifier (5) to an input thereof, and an output of said variable band-pass filter (4) is outputted as a frequency-modulated signal.

Inventors: MIURA KATSUNORI, MIURA, KATSUNORI
Applicants: SANYO ELECTRIC CO, SANYO ELECTRIC CO., LTD.
Application year: 1990
Main classification: H03C3
IPC codes: H03L7, H03C3